**Evaluation of the Distortion and Unbalance Emission Levels in Electric Networks**

Patricio Salmerón Revuelta and Alejandro Pérez Vallés

Additional information is available at the end of the chapter

http://dx.doi.org/10.5772/53373

### **1. Introduction**

[9] Thorp, J. S, Phadke, A. G, & Karimi, K. J. Real-time voltage phasor measurements for static-state estimation, *IEEE Trans. Power App. Syst.*, Nov. (1985). , PAS-104(11),

[11] Bollen, M. H. J, Zhong, J, Zavoda, F, Meyer, J, Mceachern, A, & Opez, F. C. L. Power Quality aspects of Smart Grids, International Conference on Renewable Energies and

[12] Bollen, M. H. J, Ribeiro, P. F, Larsson, E. O. A, & Lundmark, C. M. Limits for voltage distortion in the frequency range 2-9 kHz, *IEEE Transactions on Power Delivery*, July

[13] Tentzerakis, S. T, & Papathanassiou, S. A. An Investigation of the Harmonic Emis‐ sions of Wind Turbines, *IEEE Trans. Energy Convers.*, March (2007). , 22(1), 150-158.

[14] Papathanassiou, S. A, & Papadopoulos, M. P. Harmonic analysis in a power system with wind generation, *IEEE Trans. Power Delivery*, pgs. 2006-2016, October 2006. In‐ stantaneous phase tracking in power networks by demodulation, *IEEE Trans. On In‐*

*strumentation and Measurement*, vol. 41, no. 6, December (1992). , 21(4), 963-967. [15] Djuric, P. M, Begovic, M. M, & Doroslova, M. ki, Instantaneous phase tracking in power networks by demodulation, *IEEE Trans. on Instrumentation and Measurement*,

[16] Marques, C. A. G, Ribeiro, M. V, Duque, C. A, & Ribeiro, P. F. and E. A. B. da Silva, A Controlled Filtering Method for Estimating Harmonics of Off-Nominal Frequencies,

[17] Goertzel, G. An algorithm for the evaluation of finite trigonometric series, *The Ameri‐*

[10] Computer Relaying for Power SystemsNew York: John Wiley and Sons, (1988).

Power Quality, Granada (Spain), 23th to 25th March, (2010).

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*can Mathematical Monthly*, (1958). , 65(1), 34-35.

3099-3106.

248 Power Quality Issues

(2008). , 23(3), 1481-1487.

Dec. (1992). , 41(6), 963-967.

Electrical disturbances have important economic consequences for the consumer and the utilities, a fact which increases from the new electricity regulatory framework. Thus, Electric Power Quality, EPQ, has now become a priority within the field of electrical engineering. Power-quality deterioration is due to transient disturbances (voltage sags, voltage swells, impulses, etc.) and steady state disturbances (harmonic distortion, unbalance, and flicker). Among these are the so-called periodic disturbances such as distortion of the voltage and current waveforms, or unbalanced three-phase systems, [1-2]. This chapter is focused specif‐ ically on harmonic and unbalance phenomena.

These quality problems have entailed the need for measuring equipment to monitor the installation at the user side such as electric power quality analyzers, [3-7]. This equipment has a great number of quantities available relating to the harmonic distortion for each phase. Each measurement is usually composed of the voltage and current total harmonic distortion (THD) index, and RMS values of the total waveforms and the fundamental component. One problem with characterization of these data is representation of harmon‐ ic distortion when the installation has very different distortion levels in each phase. There are two choices: to consider the distortion level of each phase separately, managing three times more information, or to characterize the installation distortion using a global pa‐ rameter which considers the whole three-phase system, [5, 7]. The first approach is more interesting for analyzing the cause of the problems in an installation. The second is more

© 2013 Revuelta and Vallés; licensee InTech. This is an open access article distributed under the terms of the Creative Commons Attribution License (http://creativecommons.org/licenses/by/3.0), which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited. © 2013 Revuelta and Vallés; licensee InTech. This is a paper distributed under the terms of the Creative Commons Attribution License (http://creativecommons.org/licenses/by/3.0), which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

suited to characterizing the distortion level of the whole installation. This point of view is adopted in this chapter.

**2. Assessment of harmonic distortion and unbalance in power systems**

ize the load impact on the power system are deduced.

**2.1. Preliminary definitions**

effective current value, Ie, is

voltages are equal. Thus, the expression for Ve:

*e*

*V*

Where ξ is the power ratio,

In any system of measurement for power system, is usual to introduce a number of quanti‐ ties characterizing the waveforms of voltage and current. This requiere to define the effec‐ tive values of voltage, Ve, and current, Ie; here the definitions adopted in the IEEE Standard 1459-2000 (Std 1459), [26], are introduced. The definitions of these quantities are directly re‐ lated to the definition of apparent power. Thus, in the 1459 Std apparent power is the maxi‐ mum power that can be transmitted under ideal conditions (sinusoidal single phase or balanced three-phase sinusoidal systems) with the same impact of voltage (on the insulation and on the no-load losses) and the same impact of current (or line losses) from the PCC on the network. From this definition equivalent values of voltage and current which character‐

Evaluation of the Distortion and Unbalance Emission Levels in Electric Networks

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251

The explicit expression of the apparent power depends on how are characterized these volt‐ age and current impacts. To determine the apparent power, we introduce an equivalent voltage and an equivalent current of a balanced system of positive sequence to produce the same impact on the network voltages and currents present in the system. In the following

A three-phase system consisting of an unbalanced load is supplied by a four-wire system wherein each of the lines has a resistance r and the neutral conductor has a resistance rn. The

The 1459 Std is ρ = 1. On the premises of medium and low voltage typical ρ = 0.2 - 4. Today,

The next step is to find an effective voltage Ve. This will take into account the non load pow‐ er losses in magnetic cores of transformers and insulation 'upstream' of the load. Standard means that losses (non load losses voltage-dependent), PY, which are due to the line-neutral voltages and losses (non load losses voltage-dependent), PΔ, which are due to the line-line

> ( ) ( ) ( ) 222 222 3 9 1 *an bn cn ab bc ca*

++ + ++

x

x

*VVV VVV*

*n*

(1)

(2)

*r*

 r

are determined equivalent quantities, effective voltage, Ve, and effective current, Ie.

( ) <sup>1</sup> 222 2 ; <sup>3</sup>

digital instrumentation can develop equipment that can adjust ρ for any default.

*<sup>r</sup> I III I*

= +++ = r

*e abc n*

<sup>=</sup> <sup>+</sup>

On the other hand, it is necessary to know the responsible for the production of periodic perturbations. That is, first, identification of distortion sources, and secondly, unbalances emission. Regarding on localization of sources producing distortion two different ap‐ proaches can be distinguished: a) those based on measurements taken on the point of com‐ mon coupling, PCC, [9-21], b) those based one measurement taken and processed simultaneously on different metering sections placed on the line connected to the same PCC, [22-24]. This chapter is developed within the first group. Thus, the objective to localization of sources producing distortion is to measure instantaneous values of current and voltage in each of the branches of the PCC, and from these measurements, establish which consumers are responsible for generating the distortion and quantify the distortion generated by each consumer. Regarding the issue of unbalance emission, it is measurement and evaluating the negative and zero sequence currents injected by loads of unbalanced structure at the PCC.

Originally, the problem was analyzed through the harmonic power sign with the objective of knowing the sense of harmonic power flow between source and one load in distorted sys‐ tems. Nowadays, it has already been established in the technical literature that an analysis of this kind does not solve the problem, [10-11]. Recently, new indices have been introduced to evaluate a specific consumer distortion and unbalance level, [12, 15, 19]. In this chapter, a comparative analysis of these indices is carried out, having as reference different practical cases. The results obtained show that, in fact, these indices can help to valuate the periodic perturbation, although none of them solve the question definitively.

More recently, it has been found that the measure of quality indices of EPQ presents addi‐ tional difficulties in the presence of capacitors. The capacitor do not produce harmonic but their presence contributes to the amplification of the harmonics existing in the electrical net‐ work. The capacitor behaviour makes that the indices proposed up now to identify distor‐ tion sources fail in the presence of this element, [25]. However, in [21] has proposed a new method that resolves the situation.

The chapter is structured as follows. Second section begins with the definitions of effective voltage and current contained in the IEEE Standard 1459 and continuous with the most suit‐ ed distortion and unbalance indices for three-phase four-wire networks for characterizing the quality of the waveforms present in the PCC. In third section presents the theoretical ba‐ sis of the main methods to identify sources of unbalance and distortion: harmonic powers, conforming and nonconforming currents, balanced linear currents and unbalanced non-line‐ ar currents. A comparative analysis of different PQ indices based on digital simulations has been performed. The fourth section analyzes the problems that present PQ indices in the presence of installed capacitor banks for power factor correction. The fifth section describes an experimental setup for measuring the PQ indices of a three-phase nonlinear load con‐ nected to the mains. Finally, a discussion of the results and conclusions are extracted.

### **2. Assessment of harmonic distortion and unbalance in power systems**

In any system of measurement for power system, is usual to introduce a number of quanti‐ ties characterizing the waveforms of voltage and current. This requiere to define the effec‐ tive values of voltage, Ve, and current, Ie; here the definitions adopted in the IEEE Standard 1459-2000 (Std 1459), [26], are introduced. The definitions of these quantities are directly re‐ lated to the definition of apparent power. Thus, in the 1459 Std apparent power is the maxi‐ mum power that can be transmitted under ideal conditions (sinusoidal single phase or balanced three-phase sinusoidal systems) with the same impact of voltage (on the insulation and on the no-load losses) and the same impact of current (or line losses) from the PCC on the network. From this definition equivalent values of voltage and current which character‐ ize the load impact on the power system are deduced.

### **2.1. Preliminary definitions**

suited to characterizing the distortion level of the whole installation. This point of view is

On the other hand, it is necessary to know the responsible for the production of periodic perturbations. That is, first, identification of distortion sources, and secondly, unbalances emission. Regarding on localization of sources producing distortion two different ap‐ proaches can be distinguished: a) those based on measurements taken on the point of com‐ mon coupling, PCC, [9-21], b) those based one measurement taken and processed simultaneously on different metering sections placed on the line connected to the same PCC, [22-24]. This chapter is developed within the first group. Thus, the objective to localization of sources producing distortion is to measure instantaneous values of current and voltage in each of the branches of the PCC, and from these measurements, establish which consumers are responsible for generating the distortion and quantify the distortion generated by each consumer. Regarding the issue of unbalance emission, it is measurement and evaluating the negative and zero sequence currents injected by loads of unbalanced structure at the PCC.

Originally, the problem was analyzed through the harmonic power sign with the objective of knowing the sense of harmonic power flow between source and one load in distorted sys‐ tems. Nowadays, it has already been established in the technical literature that an analysis of this kind does not solve the problem, [10-11]. Recently, new indices have been introduced to evaluate a specific consumer distortion and unbalance level, [12, 15, 19]. In this chapter, a comparative analysis of these indices is carried out, having as reference different practical cases. The results obtained show that, in fact, these indices can help to valuate the periodic

More recently, it has been found that the measure of quality indices of EPQ presents addi‐ tional difficulties in the presence of capacitors. The capacitor do not produce harmonic but their presence contributes to the amplification of the harmonics existing in the electrical net‐ work. The capacitor behaviour makes that the indices proposed up now to identify distor‐ tion sources fail in the presence of this element, [25]. However, in [21] has proposed a new

The chapter is structured as follows. Second section begins with the definitions of effective voltage and current contained in the IEEE Standard 1459 and continuous with the most suit‐ ed distortion and unbalance indices for three-phase four-wire networks for characterizing the quality of the waveforms present in the PCC. In third section presents the theoretical ba‐ sis of the main methods to identify sources of unbalance and distortion: harmonic powers, conforming and nonconforming currents, balanced linear currents and unbalanced non-line‐ ar currents. A comparative analysis of different PQ indices based on digital simulations has been performed. The fourth section analyzes the problems that present PQ indices in the presence of installed capacitor banks for power factor correction. The fifth section describes an experimental setup for measuring the PQ indices of a three-phase nonlinear load con‐

nected to the mains. Finally, a discussion of the results and conclusions are extracted.

perturbation, although none of them solve the question definitively.

method that resolves the situation.

adopted in this chapter.

250 Power Quality Issues

The explicit expression of the apparent power depends on how are characterized these volt‐ age and current impacts. To determine the apparent power, we introduce an equivalent voltage and an equivalent current of a balanced system of positive sequence to produce the same impact on the network voltages and currents present in the system. In the following are determined equivalent quantities, effective voltage, Ve, and effective current, Ie.

A three-phase system consisting of an unbalanced load is supplied by a four-wire system wherein each of the lines has a resistance r and the neutral conductor has a resistance rn. The effective current value, Ie, is

$$I\_c = \sqrt{\frac{1}{3} \left( I\_a^2 + I\_b^2 + I\_c^2 + \rho \, I\_n^2 \right)} \quad ; \quad \rho = \frac{r\_n}{r} \tag{1}$$

The 1459 Std is ρ = 1. On the premises of medium and low voltage typical ρ = 0.2 - 4. Today, digital instrumentation can develop equipment that can adjust ρ for any default.

The next step is to find an effective voltage Ve. This will take into account the non load pow‐ er losses in magnetic cores of transformers and insulation 'upstream' of the load. Standard means that losses (non load losses voltage-dependent), PY, which are due to the line-neutral voltages and losses (non load losses voltage-dependent), PΔ, which are due to the line-line voltages are equal. Thus, the expression for Ve:

$$V\_e = \sqrt{\frac{3\left(V\_{an}^2 + V\_{bn}^2 + V\_{cn}^2\right) + \xi\left(V\_{ab}^2 + V\_{bc}^2 + V\_{ca}^2\right)}{9\left(1 + \xi\right)}}\tag{2}$$

Where ξ is the power ratio,

$$\xi = \frac{P\_{\Delta}}{P\_{Y}}\tag{3}$$

22 2 22 2 VV V ; II I e e1 eH e e1 eH = + = + (8)

Evaluation of the Distortion and Unbalance Emission Levels in Electric Networks

ah bh ch nh

http://dx.doi.org/10.5772/53373

253

è ø

where the subscript '1 'refers to the RMS values of the fundamental component,

<sup>3</sup> II II <sup>V</sup> ; I <sup>18</sup> <sup>3</sup>

e1 e1

eH eH

f f

f

f f

f

*VVV VVV anh bnh cnh abh bch cah*

h 1 h 1

¹ ¹

<sup>3</sup> II II <sup>V</sup> ;I <sup>18</sup> <sup>3</sup>

mental,

**2.2. Power quality indexes**

tortion, TDD. For voltage,

*VTHD*

and the current total harmonic distortion is,

*ITHD*

f

f

( ) ( ) 222 222 <sup>222</sup> 1 11 111 a1 b1 c1 n1

and the subscript 'H' refers to the whole of the harmonic components other than the funda‐

( ) ( ) 2 2 2 222 2 2 22

The use of effective voltage and current values helps characterize the harmonic content of the three-phase system by using the so-called total harmonic distortion (THD) rates of volt‐ age and current, [4]. Thus, for any phase *ϕ* (*a, b, c*) the voltage total harmonic distortion is,

> 1 234 1 1

*V V VVV V*

2 2

1 234 1 1

where the second subscript represents the order of the harmonic. These indices THD, har‐ monic content of the waveform are compared with the fundamental harmonic. This is a defi‐ nition in the standard IEC 61000 and is common in commercial network analyzers. However, a second definition is introduced where the harmonic content is compared to the RMS value of the waveform, [8]. Here we refer to this factor as the rate of total demand dis‐

2 2

*I I*

2 2 222 2

fff

 f

*I I III I*

*V V*

2 2 222 2

fff

 f ... *<sup>N</sup>*


... *<sup>N</sup>*


 f  f

å å (10)

+ + + ++ æ ö +++ = = ç ÷

*VVV VVV an bn cn ab bc ca* ++ + ++ +++ = = (9)

Later, the concept of losses which depend on the voltage was abandoned in favor of which‐ ever of loads that consume an equivalent active power, so that to determine the equivalent voltage Ve is assumed that the load is formed by a group resistors connected in Y, which consume a power PY and a group connected in Δ, which consume a power PΔ. In any case the St 1459 considers ξ = 1. To a three-wire three-phase system where ln = 0, the standard recommended simplified expressions,

$$V\_e = \sqrt{\frac{V\_{ab}^2 + V\_{bc}^2 + V\_{ca}^2}{9}} \qquad ; \qquad I\_e = \sqrt{\frac{I\_a^2 + I\_b^2 + I\_c^2}{3}} \tag{4}$$

referred to as the Buchholz-Goodhue, and original works proposed by the IEEE working group on nonsinusoidal situations.

As already stated above, the definition Std 1459 takes as apparent power or effective appa‐ rent power of the system, Se, that originally suggested by F. Buchholz in 1922 and clarified by W. M. Goodhue in 1933,

$$\mathbf{S}\_{\mathbf{e}} = \mathbf{3} \,\mathrm{V}\_{\mathbf{e}} \,\mathrm{I}\_{\mathbf{e}} \tag{5}$$

Similarly for a total active power consumed by a load, P, the power factor is defined as,

$$\text{PF} = \frac{\text{P}}{\text{S}\_{\text{e}}} \tag{6}$$

relating the minimum power loss and the current power loss.

The RMS values of the magnitudes of phase voltage and line current are determined as,

$$\begin{aligned} \mathbf{V}\_{\text{j}}^{2} &= \mathbf{V}\_{\text{j}1}^{2} + \sum\_{\forall \mathbf{h} \neq 1} \mathbf{V}\_{\text{j}\mathbf{h}}^{2} \\ \mathbf{I}\_{\text{j}}^{2} &= \mathbf{I}\_{\text{j}1}^{2} + \sum\_{\forall \mathbf{h} \neq 1} \mathbf{I}\_{\text{j}\mathbf{h}}^{2} \quad ; \quad \text{j=a,b,c} \end{aligned} \tag{7}$$

Likewise, it is desirable to split the effective voltage and current into two terms, one for the fundamental harmonic and the other for the remainder of the harmonics,

Evaluation of the Distortion and Unbalance Emission Levels in Electric Networks http://dx.doi.org/10.5772/53373 253

$$\mathbf{V}\_{\rm e}^{2} = \mathbf{V}\_{\rm e1}^{2} + \mathbf{V}\_{\rm eH}^{2} \qquad ; \qquad \mathbf{I}\_{\rm e}^{2} = \mathbf{I}\_{\rm e1}^{2} + \mathbf{I}\_{\rm eH}^{2} \tag{8}$$

where the subscript '1 'refers to the RMS values of the fundamental component,

$$\mathbf{V}\_{\rm e1} = \sqrt{\frac{\mathbf{3}\left(V\_{\rm am1}^2 + V\_{\rm bm1}^2 + V\_{\rm cn1}^2\right) + \left(V\_{\rm ab1}^2 + V\_{\rm bc1}^2 + V\_{\rm ca1}^2\right)}{18}} \qquad ; \qquad \mathbf{I}\_{\rm e1} = \sqrt{\frac{\mathbf{I}\_{\rm a1}^2 + \mathbf{I}\_{\rm b1}^2 + \mathbf{I}\_{\rm c1}^2 + \mathbf{I}\_{\rm n1}}{3}} \tag{9}$$

and the subscript 'H' refers to the whole of the harmonic components other than the funda‐ mental,

$$\mathbf{V}\_{\mathrm{eH}} = \sqrt{\sum\_{\mathrm{h} \neq 1} \frac{3\left(V\_{\mathrm{a}\mathrm{h}\hbar}^{2} + V\_{\mathrm{b}\mathrm{m}\mathrm{h}}^{2} + V\_{\mathrm{c}\mathrm{h}\mathrm{h}}^{2}\right) + \left(V\_{\mathrm{a}\mathrm{b}\mathrm{h}}^{2} + V\_{\mathrm{b}\mathrm{c}\mathrm{h}}^{2} + V\_{\mathrm{c}\mathrm{h}}^{2}\right)}{18}}; \mathrm{I}\_{\mathrm{eH}} = \sqrt{\sum\_{\mathrm{h} \neq 1} \left(\frac{\mathbf{I}\_{\mathrm{a}\mathrm{h}}^{2} + \mathbf{I}\_{\mathrm{b}\mathrm{h}}^{2} + \mathbf{I}\_{\mathrm{c}\mathrm{h}}^{2} + \mathbf{I}\_{\mathrm{n}\mathrm{h}}^{2}}{3}\right)}\tag{10}$$

### **2.2. Power quality indexes**

*P P Y*

Later, the concept of losses which depend on the voltage was abandoned in favor of which‐ ever of loads that consume an equivalent active power, so that to determine the equivalent voltage Ve is assumed that the load is formed by a group resistors connected in Y, which consume a power PY and a group connected in Δ, which consume a power PΔ. In any case the St 1459 considers ξ = 1. To a three-wire three-phase system where ln = 0, the standard

> 222 222 ; 9 3 *ab bc ca abc*

referred to as the Buchholz-Goodhue, and original works proposed by the IEEE working

As already stated above, the definition Std 1459 takes as apparent power or effective appa‐ rent power of the system, Se, that originally suggested by F. Buchholz in 1922 and clarified

Similarly for a total active power consumed by a load, P, the power factor is defined as,

e <sup>P</sup> PF=

The RMS values of the magnitudes of phase voltage and line current are determined as,

I I I ; j=a,b,c " ¹

Likewise, it is desirable to split the effective voltage and current into two terms, one for the

22 2 j j1 jh h 1

å

" ¹

22 2 j j1 jh h 1

fundamental harmonic and the other for the remainder of the harmonics,

VV V

= +

= +

relating the minimum power loss and the current power loss.

*VVV III V I* + + + + = = (4)

e ee S 3V I = (5)

<sup>S</sup> (6)

å (7)

*e e*

<sup>D</sup> <sup>=</sup> (3)

x

recommended simplified expressions,

252 Power Quality Issues

group on nonsinusoidal situations.

by W. M. Goodhue in 1933,

The use of effective voltage and current values helps characterize the harmonic content of the three-phase system by using the so-called total harmonic distortion (THD) rates of volt‐ age and current, [4]. Thus, for any phase *ϕ* (*a, b, c*) the voltage total harmonic distortion is,

$$\text{VITHD}\_{\phi} = \sqrt{\frac{V\_{\phi}^{2} - V\_{\phi\_{1}}^{2}}{V\_{\phi\_{1}}^{2}}} = \sqrt{\frac{V\_{\phi\_{2}}^{2} + V\_{\phi\_{3}}^{2} + V\_{\phi\_{4}}^{2} + \dots + V\_{\phi\_{N}}^{2}}{V\_{\phi\_{1}}^{2}}}\tag{11}$$

and the current total harmonic distortion is,

$$\text{ITHD}\_{\phi} = \sqrt{\frac{I\_{\phi}^{2} - I\_{\phi\_{1}}^{2}}{I\_{\phi\_{1}}^{2}}} = \sqrt{\frac{I\_{\phi\_{2}}^{2} + I\_{\phi\_{3}}^{2} + I\_{\phi\_{4}}^{2} + \dots + I\_{\phi\_{N}}^{2}}{I\_{\phi\_{1}}^{2}}} \tag{12}$$

where the second subscript represents the order of the harmonic. These indices THD, har‐ monic content of the waveform are compared with the fundamental harmonic. This is a defi‐ nition in the standard IEC 61000 and is common in commercial network analyzers. However, a second definition is introduced where the harmonic content is compared to the RMS value of the waveform, [8]. Here we refer to this factor as the rate of total demand dis‐ tortion, TDD. For voltage,

$$\left| VTDD \right|\_{\phi} = \sqrt{\frac{V\_{\phi}^{2} - V\_{\phi}^{2}}{V\_{\phi}^{2}}} = \sqrt{\frac{V\_{\phi\_{2}}^{2} + V\_{\phi\_{3}}^{2} + V\_{\phi\_{4}}^{2} + ... + V\_{\phi\_{N}}^{2}}{V\_{\phi}^{2}}} \tag{13}$$

111 1 2222 2222

= +++ (17)

Evaluation of the Distortion and Unbalance Emission Levels in Electric Networks

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255

*abc n abcn eee e VVVV*

111 1 2222 2222

= +++ (18)

*abc n abcn eee e IIII*

*IIII*

*VVVV*

3 222 2

3 222 2

To evaluate the unbalance conditions, a reference waveform may be established [2, 23]. In this paper a reference voltage waveform and a reference current waveform are defined in a similar way: they are sinusoidal and positive sequence waveforms whose RMS values, Ve1+ and Ie1+, are the effective voltage and current defined in similar form as (16), respectively.

> 2 2 2 2 1 1

*V V I I*

*e e*

 f

+ + + + - - = = (19)

*V I*

3 3 2 2 ; *e e e e*

These new factors act as indices of non-conformity of voltage and current waveforms with respect to sinusoidal waveforms of positive phase sequence of voltage and current, respec‐ tively. A comparison between the values obtained by applying the expressions (16) and (19) would determine whether the periodic disturbances are mainly due to the presence of dis‐ tortion or the presence of unbalance. Finally, in [8] a weighted distortion index has been pro‐ posed. Their calculation is based on the RMS values of each phase. However, usually, the three-phase power system is not balanced. So, the power transferred by each phase differs considerably from the other phases. It affects the information supplied by the current indi‐ ces in a relevant manner. For that reason, the definition of a new distortion index which

However, the indices defined in (17), (18), and (19) are not appropriated for establishing re‐

The identification of the loads they produce distortion has been addressed by analyzing the direction of active harmonic power flow. Therefore, this section begins with the analysis of active harmonic power. Other indices are introduced with the aim of overcoming the limita‐ tions of the method of harmonic powers. Several practical cases using a simulation environ‐

sponsibility, between customer and supplier, for the lack of electric power quality.

*VTDD ITDD*

f

takes this new effect into account may be interesting.

**3. Localization of sources producing distortion**

ment will be studied and a comparative analysis is performed.

*VTDD VTHD VTHD VTHD VTHD*

*ITDD ITHD ITHD ITHD ITHD*

f

f

and to the current

and to the current,

$$\text{ITDD}\_{\ \phi} = \sqrt{\frac{I\_{\phi}^{2} - I\_{\phi\_{1}}^{2}}{I\_{\phi}^{2}}} = \sqrt{\frac{I\_{\phi\_{2}}^{2} + I\_{\phi\_{3}}^{2} + I\_{\phi\_{4}}^{2} + \dots + I\_{\phi\_{N}}^{2}}{I\_{\phi}^{2}}} \tag{14}$$

The values provided by THD and TDD factors are often very similar to waveforms with low distortion, yet their differences are more significant for high distortions. THD factors indi‐ cate a very high value, even infinite, when the waveform has a very small or zero value of the fundamental harmonic. Moreover, TDD values are always below 100% and this is some‐ what larger errors in measurement instrumentation versus normal situations THD distor‐ tion.

The distortion characterization of the global systems requires extending the definition of harmonic distortion rates to three-phase systems. The rate of three-phase voltage total har‐ monic distortion, VTHD3ϕ, and the rate of three-phase current, ITHD3ϕ, is defined as,

$$\text{ITHD}\_{\text{-3\#}} = \sqrt{\frac{I\_{\epsilon}^{2} - I\_{\epsilon 1}^{2}}{I\_{\epsilon 1}^{2}}} \; ; \text{VTHD}\_{\text{-3\#}} = \sqrt{\frac{V\_{\epsilon}^{2} - V\_{\epsilon 1}^{2}}{V\_{\epsilon 1}^{2}}} \tag{15}$$

Similarly, is possible to define the three-phase total demand distortion of voltage, VTDD3ϕ, and the three-phase total demand distortion of current, ITDD3ϕ,

$$\text{MTDD}\_{\
u\_{\theta}} = \sqrt{\frac{I\_{\epsilon}^{2} - I\_{\epsilon 1}^{2}}{I\_{\epsilon}^{2}}} \; ; \text{VTDD}\_{\
u\_{\theta}} = \sqrt{\frac{V\_{\epsilon}^{2} - V\_{\epsilon 1}^{2}}{V\_{\epsilon}^{2}}} \tag{16}$$

According to their definition, the three-phase total demand distortion indices measure the lack of conformity of the line voltage and current waveforms with respect to sinusoidal waveforms, because of the harmonic content; without considering possible unbalances.

It is important to point out that these new indices may be calculated in a simple way with the harmonic measurements available from a commercial device. Usually, a power quality Analyzer supplies THD values, RMS values and fundamental component RMS values corre‐ sponding to each harmonic in each phase. So, the defined indices can be calculated for the measurements of each phase. For instance, the three-phase distortion indices can be calculat‐ ed by means of the following expressions: to the voltage,

$$\text{VTDD}\_{\text{ }3\neq} = \sqrt{\text{VHD}^2 \frac{V\_{a\_1}^2}{\
u\_\epsilon} + \text{VHD}^2 \frac{V\_{b\_1}^2}{\
u\_\epsilon} + \text{VHD}^2 \frac{V\_{c\_1}^2}{\
u\_\epsilon} + \text{VHD}^2 \frac{V\_{c\_1}^2}{\
u\_\epsilon} + \text{VHD}^2 \frac{V\_{n\_1}^2}{\
u\_\epsilon}}\tag{17}$$

and to the current

1 234 2 2 222 2

*V V VVV V*

fff

 f

 f ... *<sup>N</sup>*


... *<sup>N</sup>*


 f



 f

2 2

1 234 2 2 222 2

The values provided by THD and TDD factors are often very similar to waveforms with low distortion, yet their differences are more significant for high distortions. THD factors indi‐ cate a very high value, even infinite, when the waveform has a very small or zero value of the fundamental harmonic. Moreover, TDD values are always below 100% and this is some‐ what larger errors in measurement instrumentation versus normal situations THD distor‐

The distortion characterization of the global systems requires extending the definition of harmonic distortion rates to three-phase systems. The rate of three-phase voltage total har‐

> 2 2 2 2 1 1

*I I V V*

*I V*

Similarly, is possible to define the three-phase total demand distortion of voltage, VTDD3ϕ,

3 3 2 2 ; *e e e e e e*

1 1 ; *e e e e e e*

2 2 2 2 1 1

> f

*I I V V*

*I V*

According to their definition, the three-phase total demand distortion indices measure the lack of conformity of the line voltage and current waveforms with respect to sinusoidal waveforms, because of the harmonic content; without considering possible unbalances.

It is important to point out that these new indices may be calculated in a simple way with the harmonic measurements available from a commercial device. Usually, a power quality Analyzer supplies THD values, RMS values and fundamental component RMS values corre‐ sponding to each harmonic in each phase. So, the defined indices can be calculated for the measurements of each phase. For instance, the three-phase distortion indices can be calculat‐

 f

monic distortion, VTHD3ϕ, and the rate of three-phase current, ITHD3ϕ, is defined as,

*ITHD VTHD*

*ITDD VTDD*

f

and the three-phase total demand distortion of current, ITDD3ϕ,

f

ed by means of the following expressions: to the voltage,

3 3 2 2

*I I III I*

fff

2 2

*I I*

*V V*

*VTDD*

*ITDD*

f

and to the current,

254 Power Quality Issues

tion.

f

f f

f

f f

f

$$\text{ITDD}\_{\text{-3}\phi} = \sqrt{\text{ITHD}^2 \frac{I\_{a\_1}^2}{\text{I}\_e^2} + \text{ITHD}^2 \frac{\text{I}\_{b\_1}^2}{\text{b}} + \text{ITHD}^2 \frac{\text{I}\_{c\_1}^2}{\text{c}} + \text{ITHD}^2 \frac{\text{I}\_{c\_1}^2}{\text{s}} + \text{ITHD}^2 \frac{\text{I}\_{n\_1}^2}{\text{s}}} \tag{18}$$

To evaluate the unbalance conditions, a reference waveform may be established [2, 23]. In this paper a reference voltage waveform and a reference current waveform are defined in a similar way: they are sinusoidal and positive sequence waveforms whose RMS values, Ve1+ and Ie1+, are the effective voltage and current defined in similar form as (16), respectively.

$$\text{VTDD}\_{\text{-3\#}} \stackrel{+}{=} \sqrt{\frac{V\_{\epsilon}^{2} - V\_{\epsilon 1+}^{2}}{V\_{\epsilon}^{2}}} \quad ; \quad \text{ITDD}\_{\text{-3\#}} \stackrel{+}{=} \sqrt{\frac{I\_{\epsilon}^{2} - I\_{\epsilon 1+}^{2}}{I\_{\epsilon}^{2}}} \tag{19}$$

These new factors act as indices of non-conformity of voltage and current waveforms with respect to sinusoidal waveforms of positive phase sequence of voltage and current, respec‐ tively. A comparison between the values obtained by applying the expressions (16) and (19) would determine whether the periodic disturbances are mainly due to the presence of dis‐ tortion or the presence of unbalance. Finally, in [8] a weighted distortion index has been pro‐ posed. Their calculation is based on the RMS values of each phase. However, usually, the three-phase power system is not balanced. So, the power transferred by each phase differs considerably from the other phases. It affects the information supplied by the current indi‐ ces in a relevant manner. For that reason, the definition of a new distortion index which takes this new effect into account may be interesting.

However, the indices defined in (17), (18), and (19) are not appropriated for establishing re‐ sponsibility, between customer and supplier, for the lack of electric power quality.

### **3. Localization of sources producing distortion**

The identification of the loads they produce distortion has been addressed by analyzing the direction of active harmonic power flow. Therefore, this section begins with the analysis of active harmonic power. Other indices are introduced with the aim of overcoming the limita‐ tions of the method of harmonic powers. Several practical cases using a simulation environ‐ ment will be studied and a comparative analysis is performed.

### **3.1. Analisys of active harmonic powers**

In a first approximation to the problem, balanced three-phase system are considered with several non-linear loads connected to PCC. Figure 1 shows the equivalent single-phase cir‐ cuit, which includes n+ 1 branch, n corresponding to the loads and 1 to the supply. The grid is represented by the Thevenin circuit constituted by a voltage source Vs in series with in‐ ductive impedance Zs. Certainly, PCC in figure 1 represents a bus of a distribution system.

linear and nonlinear loads are connected. Sections of measurements on M, M1 and M2 are

Evaluation of the Distortion and Unbalance Emission Levels in Electric Networks

http://dx.doi.org/10.5772/53373

257

A non-linear or time-varying load (measuring section M1) and linear load (measuring sec‐ tion M2) are considered to M. In M, bus voltage is non-sinusoidal due to the simultaneous effects of distorted caused by non-linear loads upstream and downstream M. The analysis of power systems which include non-linear loads can be carried out two subsystems. There is a power flow between them corresponding to each harmonic, [1, 9]. The system analysis in frequency domain needs the consideration of an equivalent circuit for each relevant har‐ monic. Thus, the system is simplified through a Thevenin equivalent circuit from the meas‐ uring section: a nonsinusoidal Thevenin voltage and frequency dependent Thevenin

In general, there are harmonics common to Thevenin voltage and current incoming non-lin‐ ear loads. So, for each common harmonic there is a harmonic active power value corre‐ sponding to grid and consumer. Its sign depends on the subsystem responsible of the prevalent contribution. According to this, a harmonic analysis can not identify the distortion source from the active powers addition, but it only can identify the source which presents the prevalent contribution. It is because both harmonic currents as harmonic powers are due to the addition of two opposite contributions. Nevertheless, harmonic active and reactive powers measurements were the approach mainly adopted to identify the pollution generat‐

The analysis presented in above section suggests the necessity of finding an index which al‐ lows the evaluation of distortion generated by a specific load in the supply voltage system. According to this approach, the index should be based on the measurements of harmonic active powers corresponding to each load is needed. Several proposals within this approach have appeared in last years. Among them, named harmonic phase index, ξHPI, [15], defined as follows. A 3n current vector I is introduced where n is the maximum harmonic order con‐ sidered. Vector I is built with RMS values of each phase of each harmonic load current. This is broken in two components, IS and IL whose elements corresponding to each harmonic are

0 0

*k k*

ìï £ <sup>=</sup> <sup>í</sup>

*si P <sup>I</sup> I si P*

ïî

ïî

*si P <sup>I</sup> I si P*

*k k*

The harmonic phase index here introduced is lightly different from the presented in [15],

ìï <sup>³</sup> <sup>=</sup> <sup>í</sup>

*k*

f

*k*

0 0

0

(20)

0

p

considered.

equivalent impedance.

defined as follows;

ed by the consumer to the supply waveform quality.

*3.1.1. An index to identify distorted loads based in harmonic powers*

*Sk*

*Lk*

**Figure 1.** Non linear balanced three-phase system equivalent circuit.

Consumers are supplied by single impedances, where each load is modelled as impedance ZLj connected in parallel to a harmonic source ILj, for j branch. Due to the system topology, it is necessary the measurement of voltage and current in each branch connected to the PCC. From these measurements, the consumers responsible of distortion are established. Besides, distortion generated by each one is quantified. Thus, figure 1 can be reduced to figure 2.

Consumers are supplied by single impedances, where each load is modelled as impedance ZLj connected in parallel to a harmonic source ILj, for j branch. Due to the system topology, it is necessary the measurement of voltage and current in each branch connected to the PCC. From these measurements, the consumers responsible of distortion are established. Besides, distortion generated by each one is quantified. Thus, figure 1 can be reduced to figure 2.

**Figure 2.** Sections of measurements in a power system simplified diagram with two loads connected to PCC.

From now on, diagram presented in figure 2 is considered as reference. There is a PCC where a sinusoidal voltage source is connected through source impedance. Besides, several linear and nonlinear loads are connected. Sections of measurements on M, M1 and M2 are considered.

A non-linear or time-varying load (measuring section M1) and linear load (measuring sec‐ tion M2) are considered to M. In M, bus voltage is non-sinusoidal due to the simultaneous effects of distorted caused by non-linear loads upstream and downstream M. The analysis of power systems which include non-linear loads can be carried out two subsystems. There is a power flow between them corresponding to each harmonic, [1, 9]. The system analysis in frequency domain needs the consideration of an equivalent circuit for each relevant har‐ monic. Thus, the system is simplified through a Thevenin equivalent circuit from the meas‐ uring section: a nonsinusoidal Thevenin voltage and frequency dependent Thevenin equivalent impedance.

In general, there are harmonics common to Thevenin voltage and current incoming non-lin‐ ear loads. So, for each common harmonic there is a harmonic active power value corre‐ sponding to grid and consumer. Its sign depends on the subsystem responsible of the prevalent contribution. According to this, a harmonic analysis can not identify the distortion source from the active powers addition, but it only can identify the source which presents the prevalent contribution. It is because both harmonic currents as harmonic powers are due to the addition of two opposite contributions. Nevertheless, harmonic active and reactive powers measurements were the approach mainly adopted to identify the pollution generat‐ ed by the consumer to the supply waveform quality.

### *3.1.1. An index to identify distorted loads based in harmonic powers*

**3.1. Analisys of active harmonic powers**

256 Power Quality Issues

**Figure 1.** Non linear balanced three-phase system equivalent circuit.

In a first approximation to the problem, balanced three-phase system are considered with several non-linear loads connected to PCC. Figure 1 shows the equivalent single-phase cir‐ cuit, which includes n+ 1 branch, n corresponding to the loads and 1 to the supply. The grid is represented by the Thevenin circuit constituted by a voltage source Vs in series with in‐ ductive impedance Zs. Certainly, PCC in figure 1 represents a bus of a distribution system.

Consumers are supplied by single impedances, where each load is modelled as impedance ZLj connected in parallel to a harmonic source ILj, for j branch. Due to the system topology, it is necessary the measurement of voltage and current in each branch connected to the PCC. From these measurements, the consumers responsible of distortion are established. Besides, distortion generated by each one is quantified. Thus, figure 1 can be reduced to figure 2.

Consumers are supplied by single impedances, where each load is modelled as impedance ZLj connected in parallel to a harmonic source ILj, for j branch. Due to the system topology, it is necessary the measurement of voltage and current in each branch connected to the PCC. From these measurements, the consumers responsible of distortion are established. Besides, distortion generated by each one is quantified. Thus, figure 1 can be reduced to figure 2.

**Figure 2.** Sections of measurements in a power system simplified diagram with two loads connected to PCC.

From now on, diagram presented in figure 2 is considered as reference. There is a PCC where a sinusoidal voltage source is connected through source impedance. Besides, several The analysis presented in above section suggests the necessity of finding an index which al‐ lows the evaluation of distortion generated by a specific load in the supply voltage system. According to this approach, the index should be based on the measurements of harmonic active powers corresponding to each load is needed. Several proposals within this approach have appeared in last years. Among them, named harmonic phase index, ξHPI, [15], defined as follows. A 3n current vector I is introduced where n is the maximum harmonic order con‐ sidered. Vector I is built with RMS values of each phase of each harmonic load current. This is broken in two components, IS and IL whose elements corresponding to each harmonic are defined as follows;

$$\begin{aligned} I\_{Sk} &= \begin{cases} 0 & \text{si} \qquad P\_k \le 0 \\ I\_k & \text{si} \quad P\_k \succ 0 \end{cases} \\\\ I\_{Lk} &= \begin{cases} 0 & \text{si} \qquad P\_k \ge 0 \\ I\_k & \text{si} \quad P\_k \prec 0 \end{cases} \end{aligned} \tag{20}$$

The harmonic phase index here introduced is lightly different from the presented in [15],

$$\ln(t) = \sum\_{k=1}^{n} \sqrt{2} \,\mathrm{LI}\_k \sin\left(ka\_\mathrm{l}t + \theta\_k\right) \quad ; \quad i(t) = \sum\_{k=1}^{n} \sqrt{2} \,\mathrm{I}\_k \sin\left(ka\_\mathrm{l}t + \phi\_k\right) \tag{21}$$

Expressions in time domain for each line current are:

where Id is *id*(t) RMS value.

**3.3. Linear and nonlinear current**

not responsible of the distortion.

problems.

( ) dI NC 100 %

1 1

*V I*

*a*

**1**

**1**

**Z**

**Z**

=

*a*

*a*

Ð=-=

Where V1 and I1 are fundamental voltage and current RMS values in PCC, *θ1* and *ϕ1* are volt‐ age and current fundamental phases, *θk* is the k order harmonic phase of voltage and *i*(t) is the load current. The index of distortion proposed en [12] is the non collinear index, NC,

11 1

The problem of separating the contributions to the distortion of the supply and the consum‐ er was approached was reasoned in [19] as follows. The deterioration of EPQ due to har‐ monics can be caused simultaneously in several points of network. Voltage and current waveforms measured in PCC are due to the combined effect of several polluting equipment connected in different places in the network. It is possible the determination of the specific load contribution to harmonic distortion, whereas all other is considered in the supply side which includes the rest of loads. The first step is fixing the ideal load conditions. Any load which shows a linear and balanced behavior represents and ideal load condition. In fact, if specific load is balanced and linear, the supply is the only responsible of harmonic distor‐ tion in PCC. Initially, it is necessary the identification of waveform of incoming current if an equivalent linear and balanced load is presented instead of the actual incoming load current. This load can be defined as the linear load that requires a fundamental active power equal to the fundamental active power actually flow by PCC. It requires a distorted current but it is

In order to model the three-phase balanced linear ideal load, three identical RL branches have been considered. Through the evaluation of R, L parameters, the part of load that rep‐ resents the equivalent ideal load can be identified. So, from the consumer side, it is always possible the estimation of the linear load. This part of the actual load requires a balanced and linear which constitute an ideal current and represents one component of the load cur‐ rent in PCC. If ideal current is almost total current, the load is not responsible of distortion

Equivalent balanced and linear load parameters R and L are estimated in phase 'a' accord‐ ing to the procedure indicated as follow, (the same method can be applied to phases 'b' and

 j

*a aa a*

qf

<sup>I</sup> = ´ (24)

http://dx.doi.org/10.5772/53373

Evaluation of the Distortion and Unbalance Emission Levels in Electric Networks

(25)

259

This index has the following significant characteristics for the purpose for which it is intro‐ duced. First, it is defined from the ratio of current RMS values that are the actual cause of disturbances generated by loads in the grid. Second, different harmonic values are not add‐ ed, but in quadratic sum way. It avoids mutual cancellation between different harmonics.

### **3.2. Conforming and non-conforming currents**

In [12], authors distinguish two kinds of loads, conforming loads and non-conforming loads. A conforming load does not cause a change in voltage waveform distortion or in symmetry of the phases. Any other load that changes the voltage waveform or symmetry is a non-con‐ forming load. Thus, from the harmonic point of view, the author considers that a conform‐ ing load presents a current collinear to the voltage. A typical load will be constituted by a conforming part and a non-conforming part which may be modelled in a simple way by means of two parallel elements. Current measured in the input *i*(t) will be the sum of cur‐ rents incoming to the conforming part *in*(t) and the non-conforming part *id*(t). The conform‐ ing current is the part of the current that presents the same distortion level as supply voltage. The rest of current is the non wished part of current; the incoming in non-conform‐ ing load. The split of power flow is obtained from the components established by the cur‐ rent.

Voltage and current measured in load terminals are expressed as the addition of fundamen‐ tal harmonic and other components multiple of fundamental.

$$\mathbf{Y}\left(j k w\_{1}\right) = \left|\mathbf{Y}\left(j o\_{1}\right)\right| \angle k(\varphi\_{1} - \theta\_{1}) \quad ; \quad \mathbf{Y}\left(j o\_{1}\right) = \left|\frac{\mathbf{I}\_{1}}{\mathbf{V}\_{1}}\right| \angle (\varphi\_{1} - \theta\_{1}) \tag{22}$$

The conforming current presents the same variation as voltage waveform and its phase may be lower or higher. On the other hand, due to the fact that the load can not generate power at fundamental frequency, conforming current evolves the complete fundamental active and reactive powers. Conforming current at fundamental frequency In1 is equal to the total cur‐ rent at fundamental frequency, I1. The rest of components to the conforming current for dif‐ ferent frequencies are proportional to the corresponding harmonic voltage components. The proportional constant is a complex ratio:

$$\begin{aligned} i\_n(t) &= \sum\_{k=1}^n \frac{I\_1}{V\_1} \sqrt{2} \, V\_k \sin \left( k a\_1 t + \theta\_k + k \left( \phi\_1 - \theta\_1 \right) \right) \\ i\_d(t) &= i(t) - i\_n(t) \end{aligned} \tag{23}$$

Expressions in time domain for each line current are:

$$\text{NCC} = \frac{\text{I}\_{\text{d}}}{\text{I}} \times 100 \text{(\%)}\tag{24}$$

Where V1 and I1 are fundamental voltage and current RMS values in PCC, *θ1* and *ϕ1* are volt‐ age and current fundamental phases, *θk* is the k order harmonic phase of voltage and *i*(t) is the load current. The index of distortion proposed en [12] is the non collinear index, NC,

$$\begin{aligned} \left| \mathbf{Z\_{1a}} \right| &= \frac{V\_{1a}}{I\_{1a}}\\ \angle \mathbf{Z\_{1a}} &= \left| \boldsymbol{\theta\_{1a}} - \boldsymbol{\phi\_{1a}} \right| = \boldsymbol{\varphi\_{1a}} \end{aligned} \tag{25}$$

where Id is *id*(t) RMS value.

( ) ( ) 1 1

= += + å å (21)

w f

*kk kk*

This index has the following significant characteristics for the purpose for which it is intro‐ duced. First, it is defined from the ratio of current RMS values that are the actual cause of disturbances generated by loads in the grid. Second, different harmonic values are not add‐ ed, but in quadratic sum way. It avoids mutual cancellation between different harmonics.

In [12], authors distinguish two kinds of loads, conforming loads and non-conforming loads. A conforming load does not cause a change in voltage waveform distortion or in symmetry of the phases. Any other load that changes the voltage waveform or symmetry is a non-con‐ forming load. Thus, from the harmonic point of view, the author considers that a conform‐ ing load presents a current collinear to the voltage. A typical load will be constituted by a conforming part and a non-conforming part which may be modelled in a simple way by means of two parallel elements. Current measured in the input *i*(t) will be the sum of cur‐ rents incoming to the conforming part *in*(t) and the non-conforming part *id*(t). The conform‐ ing current is the part of the current that presents the same distortion level as supply voltage. The rest of current is the non wished part of current; the incoming in non-conform‐ ing load. The split of power flow is obtained from the components established by the cur‐

Voltage and current measured in load terminals are expressed as the addition of fundamen‐

The conforming current presents the same variation as voltage waveform and its phase may be lower or higher. On the other hand, due to the fact that the load can not generate power at fundamental frequency, conforming current evolves the complete fundamental active and reactive powers. Conforming current at fundamental frequency In1 is equal to the total cur‐ rent at fundamental frequency, I1. The rest of components to the conforming current for dif‐ ferent frequencies are proportional to the corresponding harmonic voltage components. The

( ) <sup>1</sup>

w q

() 2 ( )

= ++ -

1 11

 fq

å (23)

 w

( ); ( ) *j* = Ð- **<sup>1</sup>**

 jq

**<sup>V</sup>** (22)

**1**

( ) () ( ) 1 1 11 1 11 *jkw j k* = Ð-

 jq

**<sup>I</sup> Y Y <sup>Y</sup>**

tal harmonic and other components multiple of fundamental.

w

1 1

*V i t it i t*

*n kk*

*<sup>I</sup> i t V sin k t k*

() () ()

*n*

*k d n*

=

= -

proportional constant is a complex ratio:

1 1 () 2 ; () 2 *n n*

= =

*u t U sin k t i t I sin k t*

*k k*

w q

**3.2. Conforming and non-conforming currents**

rent.

258 Power Quality Issues

### **3.3. Linear and nonlinear current**

The problem of separating the contributions to the distortion of the supply and the consum‐ er was approached was reasoned in [19] as follows. The deterioration of EPQ due to har‐ monics can be caused simultaneously in several points of network. Voltage and current waveforms measured in PCC are due to the combined effect of several polluting equipment connected in different places in the network. It is possible the determination of the specific load contribution to harmonic distortion, whereas all other is considered in the supply side which includes the rest of loads. The first step is fixing the ideal load conditions. Any load which shows a linear and balanced behavior represents and ideal load condition. In fact, if specific load is balanced and linear, the supply is the only responsible of harmonic distor‐ tion in PCC. Initially, it is necessary the identification of waveform of incoming current if an equivalent linear and balanced load is presented instead of the actual incoming load current. This load can be defined as the linear load that requires a fundamental active power equal to the fundamental active power actually flow by PCC. It requires a distorted current but it is not responsible of the distortion.

In order to model the three-phase balanced linear ideal load, three identical RL branches have been considered. Through the evaluation of R, L parameters, the part of load that rep‐ resents the equivalent ideal load can be identified. So, from the consumer side, it is always possible the estimation of the linear load. This part of the actual load requires a balanced and linear which constitute an ideal current and represents one component of the load cur‐ rent in PCC. If ideal current is almost total current, the load is not responsible of distortion problems.

Equivalent balanced and linear load parameters R and L are estimated in phase 'a' accord‐ ing to the procedure indicated as follow, (the same method can be applied to phases 'b' and 'c'). If phase 'a' equivalent linear impedance is named by Z1a, the R-L series circuit at funda‐ mental frequency is:

$$\begin{aligned} \mathbf{Z}\_a &= \left| \mathbf{Z}\_{1a} \right| \cos \varphi\_{1a} \\ X\_{1a} &= \left| \mathbf{Z}\_{1a} \right| \sin \varphi\_{1a} \\ L\_a &= \frac{X\_{1a}}{2\pi f\_1} \end{aligned} \tag{26}$$

100 %( ) *nLa*

The non-linear current indicates how much the actual load current in phase 'a' differs from the ideal linear load in terms of harmonic distortion. Thus, an index of non-linear current is defined with the intention to provide reliable information about distortion caused by the

> ( ) <sup>2</sup> + ab c <sup>1</sup> V V +aV +a V

where InLa and Ia are the RMS values corresponding to non-linear and actual current, respec‐

Harmonic powers and indices for assessing the harmonic distortion introduced in the previ‐ ous sections have been applied to the system shown in Figure 3. This is a balanced system consisting of two AC / DC converters controlled firing angles 25° (Rectifier 1) and 45° (Recti‐

In the first situation has been considered a sinusoidal Thevenin voltage upstream of M and network parameters given by R = 0.005 Ω and L = 9,5x10-5 H. Under these conditions, the

*<sup>I</sup>* = ´ (31)

http://dx.doi.org/10.5772/53373

261

Evaluation of the Distortion and Unbalance Emission Levels in Electric Networks

= (32)

*a*

*<sup>I</sup> NL*

3

consumer:

tively.

fier 2).

**3.4. Practical cases: Digital simulations**

**Figure 3.** Circuit topology for the practical cases.

measuring point M, the VTDD is 15.06%.

*3.4.1. Case 1: Sinusoidal voltage*

where V1a and I1a are voltage and current RMS values of fundamental frequency, respective‐ ly, in PCC, and *θ1a* and *ϕ1a* are phase angle of those magnitudes. So,

$$X\_{\rm ka} = 2\pi k f\_1 \mathcal{L}\_a \quad , \quad k = 1, 2, \cdots n \tag{27}$$

where X1a represents reactance of R-L series combination at fundamental frequency, f1, and Ra and La are the corresponding parameters. Reactance values to voltage harmonic compo‐ nents are,

$$\begin{aligned} \left| \mathbf{Z\_{ka}} \right| &= \sqrt{\mathbf{R}\_a^2 + \mathbf{X}\_{\mathbf{a}\_a}^2} \\ \varphi\_{ka} &= \text{tag} \, ^{-1} \frac{\mathbf{X\_{ka}}}{\mathbf{R}\_a} \quad , \quad k = 1, 2, \cdots \text{m} \end{aligned} \tag{28}$$

The skin effect is neglected, that is, the resistance is assumed to be constant for all frequen‐ cies, and hence,

$$\dot{i}\_{La}(t) = \sum\_{k=1}^{n} \frac{\mathbf{V}\_{ka}}{\left| \mathbf{Z}\_{ka} \right|} \sqrt{2} \operatorname{sen} \left( 2\pi k f\_1 t + (\boldsymbol{\theta}\_{ka} - \boldsymbol{\phi}\_{ka}) \right) \tag{29}$$

where n is the most significant order of harmonic. As a consequence, current in the ideal lin‐ ear load in phase 'a' is,

$$i\_{nLa}(t) = i\_a(t) - i\_{La}(t) \tag{30}$$

This is the equivalent linear current and the supply system is the only responsible of its dis‐ tortion. The difference between measured current and calculated ideal current is defined as non-linear current:

Evaluation of the Distortion and Unbalance Emission Levels in Electric Networks http://dx.doi.org/10.5772/53373 261

$$\text{NL} = \frac{I\_{nLa}}{I\_a} \times 100 \left(\% \right) \tag{31}$$

The non-linear current indicates how much the actual load current in phase 'a' differs from the ideal linear load in terms of harmonic distortion. Thus, an index of non-linear current is defined with the intention to provide reliable information about distortion caused by the consumer:

$$\mathbf{V\_{+}} = \frac{1}{3} \left( \mathbf{V\_{a}} + \mathbf{a} \mathbf{V\_{b}} + \mathbf{a}^{2} \mathbf{V\_{c}} \right) \tag{32}$$

where InLa and Ia are the RMS values corresponding to non-linear and actual current, respec‐ tively.

### **3.4. Practical cases: Digital simulations**

'c'). If phase 'a' equivalent linear impedance is named by Z1a, the R-L series circuit at funda‐

1

j

where V1a and I1a are voltage and current RMS values of fundamental frequency, respective‐

where X1a represents reactance of R-L series combination at fundamental frequency, f1, and Ra and La are the corresponding parameters. Reactance values to voltage harmonic compo‐

<sup>1</sup> , 1, 2,

*<sup>X</sup> tag k n <sup>R</sup>*

The skin effect is neglected, that is, the resistance is assumed to be constant for all frequen‐

p

where n is the most significant order of harmonic. As a consequence, current in the ideal lin‐

This is the equivalent linear current and the supply system is the only responsible of its dis‐ tortion. The difference between measured current and calculated ideal current is defined as

<sup>V</sup> () 2 2 ( )

=å + -

() () () *nLa a La*

*La ka ka*

( ) <sup>1</sup>

 qj

*i t it i t* = - (30)

L (27)

<sup>L</sup> (28)

(26)

(29)

j

1 1 1 1

*f*

<sup>1</sup> 2 , 1, 2, *X kf L k n ka <sup>a</sup>* = =

2 2

*R X*

*ka*

= =

*a*

*ka a a*

= +

*ka*

1

=

*k a*

**Zk**

*<sup>n</sup> ka*

*i t sen kf t*

**Zk**

j-

*X sen X*

**1 1**

**Z Z**

*aa a aa a a*

2

p

*a*

=

*L*

ly, in PCC, and *θ1a* and *ϕ1a* are phase angle of those magnitudes. So,

p

*R*

= = cos

mental frequency is:

260 Power Quality Issues

nents are,

cies, and hence,

ear load in phase 'a' is,

non-linear current:

Harmonic powers and indices for assessing the harmonic distortion introduced in the previ‐ ous sections have been applied to the system shown in Figure 3. This is a balanced system consisting of two AC / DC converters controlled firing angles 25° (Rectifier 1) and 45° (Recti‐ fier 2).

**Figure 3.** Circuit topology for the practical cases.

### *3.4.1. Case 1: Sinusoidal voltage*

In the first situation has been considered a sinusoidal Thevenin voltage upstream of M and network parameters given by R = 0.005 Ω and L = 9,5x10-5 H. Under these conditions, the measuring point M, the VTDD is 15.06%.


Table 1 lists the powers of the main harmonics in the three measurement points M, M1, M2, Figure 3. The same table includes the values of total active power, fundamental and har‐ monic power in the three sections of measurement.

HPI index account the current values prevailing at the measuring point. HPI indices in the three measuring points indicate currents prevalent from consumer to source direction, and are suitable for assessing the contribution of both loads. The same table 2 also includes the indices NC and NL. For measures in M, the three indices have consistent values. However, for each individual load, the HPI index assigns greater responsibility for the distortion to the load 1 before to the load 2, while NC and NL rates assigned greater responsibility to the

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Tables 3 and 4 present the results for the same system of figure 3 but this time the TDD voltage at point M is 12.67%. In this case, the Thevenin voltage network is not sinusoidal but includes harmonics of order 5 and 7. Harmonic powers PH are positive in all measurement points.

> PT(W) 1.54371·105 9.7743·104 5.6623·104 P1 (W) 1.4796·105 9.5058·104 5.2907·104 PH (W) 6.4011·103 2.6845·103 3.7166·103

The indices NC and NL, Table 4, have values consistent with those obtained in the previous situation. But not so with HPI indices showing less stability against variations in network conditions. This time the HPI index shows an allocation of responsibility for the distortion between charges 1 and 2 contrary to case 1. By contrast, the results table further shows ade‐

> ITDD 23.62 30.78 38.25 HPI 6.78 2.28 20.83 NC 30.67 35.57 42.97 NL 25.46 33.00 38.82

**Table 4.** Current Total Demand Distortion, Harmonic Phase Index, Non Collinear Index and Non Linear Index values in

**4. On the measurement of PQ indices in the presence of capacitor bank**

In [21, 25] has shown experimentally that the presence of equipment power factor compen‐ sation capacitors based on amplified the distortion existing in the network. Moreover, as

**Two loads Load 1 Load 2**

**Two load Load 1 Load 2**

load 2 before to the load 1. The values obtained by the latter two are consistent.

**Table 3.** Active powers of the main harmonics and global results for the case 2.

quate stability of NL and NC indices versus distortion variations network.

*3.4.2. Case 2: Non-sinusoidal voltage*

the case 2.

**Table 1.** Active powers of the main harmonics and global results for the case 1.

The total harmonic power (point M) is -14.68 W in the direction of power flow from consumer to network. This is because the harmonic powers of certain orders are negative and larger abso‐ lute value than those of the harmonics with positive powers. Harmonic power measuring sec‐ tion M becomes a indicator of consumption nonlinear produced downstream of M. However, the presence of two non-linear loads of different consumption changes the situation and the harmonic power fail when their values are obtained in the measuring sections M1 and M2. In‐ deed, in the section of the M2 measure harmonic power PH2 is 107.69 W in the direction from network to load, while in M1, the harmonic power PH1 is -12.37 W in the direction from load to network. That is, the method of direction of power flow, when more than one source of distor‐ tion, determines the prevalent power for each harmonic, corresponding to the power flows in opposite directions, load to network versus network to load, into measuring point. Therefore, when more than one source of distortion, it is not possible to reliably identify the responsible of the disturbance through only the harmonic power. Table 2 presents four indices to assess the distortion. The first ITDD characterized the harmonic content of the current waveforms. The remaining three are defined to identify sources of distortion.


**Table 2.** Current Total Demand Distortion, Harmonic Phase Index, Non Collinear Index and Non Linear Index values for the case 1.

HPI index account the current values prevailing at the measuring point. HPI indices in the three measuring points indicate currents prevalent from consumer to source direction, and are suitable for assessing the contribution of both loads. The same table 2 also includes the indices NC and NL. For measures in M, the three indices have consistent values. However, for each individual load, the HPI index assigns greater responsibility for the distortion to the load 1 before to the load 2, while NC and NL rates assigned greater responsibility to the load 2 before to the load 1. The values obtained by the latter two are consistent.

### *3.4.2. Case 2: Non-sinusoidal voltage*

Table 1 lists the powers of the main harmonics in the three measurement points M, M1, M2, Figure 3. The same table includes the values of total active power, fundamental and har‐

> P1 (W) 1.9129·105 1.1377·105 7.7512·104 P5 (W) -3.4427·102 -1.2706·103 9.2632·102 P7 (W) -1.2238·101 -2.1575·101 9.3370·100 P11 (W) 3.7115·101 1.5520·102 -1.1809·102 P13 (W) 1.1830·102 2.7183·102 -1.6761·102 P17 (W) 4.7315·101 2.7183·102 -2.2452·102 PT (W) 1.9127·105 1.1365·105 7.7620·104 PH (W) -1.4683·101 -1.2237·102 1.0769·102

The total harmonic power (point M) is -14.68 W in the direction of power flow from consumer to network. This is because the harmonic powers of certain orders are negative and larger abso‐ lute value than those of the harmonics with positive powers. Harmonic power measuring sec‐ tion M becomes a indicator of consumption nonlinear produced downstream of M. However, the presence of two non-linear loads of different consumption changes the situation and the harmonic power fail when their values are obtained in the measuring sections M1 and M2. In‐ deed, in the section of the M2 measure harmonic power PH2 is 107.69 W in the direction from network to load, while in M1, the harmonic power PH1 is -12.37 W in the direction from load to network. That is, the method of direction of power flow, when more than one source of distor‐ tion, determines the prevalent power for each harmonic, corresponding to the power flows in opposite directions, load to network versus network to load, into measuring point. Therefore, when more than one source of distortion, it is not possible to reliably identify the responsible of the disturbance through only the harmonic power. Table 2 presents four indices to assess the distortion. The first ITDD characterized the harmonic content of the current waveforms. The

**Two loads Load 1 Load 2**

ITDD 23.59 31.14 37.68 HPI 22.08 26.37 16.70 NC 29.76 34.92 41.30 NL 25.92 33.17 38.97

**Table 2.** Current Total Demand Distortion, Harmonic Phase Index, Non Collinear Index and Non Linear Index values for

**Two loads Load 1 Load 2**

monic power in the three sections of measurement.

262 Power Quality Issues

**Table 1.** Active powers of the main harmonics and global results for the case 1.

remaining three are defined to identify sources of distortion.

the case 1.

Tables 3 and 4 present the results for the same system of figure 3 but this time the TDD voltage at point M is 12.67%. In this case, the Thevenin voltage network is not sinusoidal but includes harmonics of order 5 and 7. Harmonic powers PH are positive in all measurement points.


**Table 3.** Active powers of the main harmonics and global results for the case 2.

The indices NC and NL, Table 4, have values consistent with those obtained in the previous situation. But not so with HPI indices showing less stability against variations in network conditions. This time the HPI index shows an allocation of responsibility for the distortion between charges 1 and 2 contrary to case 1. By contrast, the results table further shows ade‐ quate stability of NL and NC indices versus distortion variations network.


**Table 4.** Current Total Demand Distortion, Harmonic Phase Index, Non Collinear Index and Non Linear Index values in the case 2.

### **4. On the measurement of PQ indices in the presence of capacitor bank**

In [21, 25] has shown experimentally that the presence of equipment power factor compen‐ sation capacitors based on amplified the distortion existing in the network. Moreover, as discussed later, the techniques proposed for assigning responsibility for harmonic distortion penalize capacitors like nonlinear loads. This is in clear contradiction with the vast majority of standards that require the use of capacitors for power factor correction to the fundamen‐ tal frequency.

**Two loads Load 1 Load 2**

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ITDD 17.43 2.46 18.94 HPI 0.00 0.00 0.00 NC 7.34 12.74 20.58 NL 7.34 0.00 18.08

Analysis of Table 6 shows how, in this case, only HPI rate indices identify the presence of linear loads in each measuring point. Although the HPI index identifies linear loads, howev‐ er, then you will see that this index does not succeed when the system is unbalanced. The NL index can identify the RL load as linear but fails with RC load. The NC index fails to

Secondly, we have been considered a six-pulse controlled rectifier (load 1) in parallel with a linear load RC (load 2). This case is the same as above was used to obtain the waveforms presented in Figure 4. The table 7 includes the values obtained for the deferent indexes. In this case none of the identified indexes load 2 as linear load. The ITDD is the amplification of harmonics due to the presence of the capacitive load. Rates of identification of nonlinear

**Two loads Load 1 Load 2**

ITDD 28.90 33.78 56.49

HPI 28.56 32.32 40.37

NC 31.95 34.84 56.04

NL 30.48 34.82 53.80

From the point of view of electromagnetic compatibility we distinguish between immunity and emission of a particular disturbance. The emission of imbalance consists of measuring the current phase sequence different from the positive sequence injected by an unbalanced

**Table 6.** PQ indices in the case 1.

identify any such linear loads.

**4.2. Case 2: Non linear load and capacitive load**

**Table 7.** Index values with the presence of capacitor banks.

**5. Assessment of unbalance emission**

loads HPI, NC, and NL, have high values for linear RC load.

Indeed, an electronic load of the type power converter absorbs a current obtained through the sudden switching of electronic devices according to the on-off states. This current pro‐ duces voltage drops in the inductive impedance of the grid, causing voltage peaks in the voltage waveform at the PCC. As a result, the current drawn by the linear load has a peak and RMS values higher because the load capacitors which tend to emphasize the high har‐ monics at the facility. This would be the case, for example, a set of discharge lamps (com‐ pensated) connected to the same PCC that a nonlinear load. The simplified equivalent circuit comprises an ohmic-inductive branch and a capacitive branch. High current harmon‐ ics are almost completely absorbed by the capacitive branch, since its impedance at these frequencies is very small compared with that of the other branch. This contributes to the in‐ creased distortion of the current absorbed by the linear load. Therefore, although the capaci‐ tors do not introduce new harmonics on the network, if they can dramatically amplify existing distortion produced by nearby non-linear loads.

To illustrate the situation has been considered a system consisting of a six-pulse rectifier controlled with a consumption of 91.77 kW in parallel with a line load consisting of 4 Ω re‐ sistor in parallel with a capacitor of 0.1 mF. The figure a) shows the waveform of the phase voltage at the PCC and figure b) the waveform of the current drawn by the RC load.

This has consequences for the effectiveness of the various indices introduced to identify sources of distortion. The situation is illustrated through two practical cases of simulation.

### **4.1. Case 1: Inductive and capacitive linear loads**

Consider two linear loads for the same topology of Figure 3, the first consisting of a R = 2 Ω in series with an L = 0.01 H, and the second one R = 2 Ω in series with a C = 0.001 F; the supply voltage includes harmonics of orders 5 and 7. Tables 5 and 6 present the results.


**Table 5.** Harmonic and total powers in the case 1.


**Table 6.** PQ indices in the case 1.

discussed later, the techniques proposed for assigning responsibility for harmonic distortion penalize capacitors like nonlinear loads. This is in clear contradiction with the vast majority of standards that require the use of capacitors for power factor correction to the fundamen‐

Indeed, an electronic load of the type power converter absorbs a current obtained through the sudden switching of electronic devices according to the on-off states. This current pro‐ duces voltage drops in the inductive impedance of the grid, causing voltage peaks in the voltage waveform at the PCC. As a result, the current drawn by the linear load has a peak and RMS values higher because the load capacitors which tend to emphasize the high har‐ monics at the facility. This would be the case, for example, a set of discharge lamps (com‐ pensated) connected to the same PCC that a nonlinear load. The simplified equivalent circuit comprises an ohmic-inductive branch and a capacitive branch. High current harmon‐ ics are almost completely absorbed by the capacitive branch, since its impedance at these frequencies is very small compared with that of the other branch. This contributes to the in‐ creased distortion of the current absorbed by the linear load. Therefore, although the capaci‐ tors do not introduce new harmonics on the network, if they can dramatically amplify

To illustrate the situation has been considered a system consisting of a six-pulse rectifier controlled with a consumption of 91.77 kW in parallel with a line load consisting of 4 Ω re‐ sistor in parallel with a capacitor of 0.1 mF. The figure a) shows the waveform of the phase

This has consequences for the effectiveness of the various indices introduced to identify sources of distortion. The situation is illustrated through two practical cases of simulation.

Consider two linear loads for the same topology of Figure 3, the first consisting of a R = 2 Ω in series with an L = 0.01 H, and the second one R = 2 Ω in series with a C = 0.001 F; the supply voltage includes harmonics of orders 5 and 7. Tables 5 and 6 present the results.

P1 (W) 4.4590·104 2.2504·104 2.2086·104

P5 (W) 7.4478·102 1.2859·101 7.3192·102

P7 (W) 9.0580·101 7.7483·101 8.9805·101

PT (W) 4.5425·104 2.2518·104 2.2908·104

PH (W) 8.3536·102 1.3634·101 8.2172·102

**Two loads Load 1 Load 2**

voltage at the PCC and figure b) the waveform of the current drawn by the RC load.

existing distortion produced by nearby non-linear loads.

**4.1. Case 1: Inductive and capacitive linear loads**

**Table 5.** Harmonic and total powers in the case 1.

tal frequency.

264 Power Quality Issues

Analysis of Table 6 shows how, in this case, only HPI rate indices identify the presence of linear loads in each measuring point. Although the HPI index identifies linear loads, howev‐ er, then you will see that this index does not succeed when the system is unbalanced. The NL index can identify the RL load as linear but fails with RC load. The NC index fails to identify any such linear loads.

### **4.2. Case 2: Non linear load and capacitive load**

Secondly, we have been considered a six-pulse controlled rectifier (load 1) in parallel with a linear load RC (load 2). This case is the same as above was used to obtain the waveforms presented in Figure 4. The table 7 includes the values obtained for the deferent indexes. In this case none of the identified indexes load 2 as linear load. The ITDD is the amplification of harmonics due to the presence of the capacitive load. Rates of identification of nonlinear loads HPI, NC, and NL, have high values for linear RC load.


**Table 7.** Index values with the presence of capacitor banks.

### **5. Assessment of unbalance emission**

From the point of view of electromagnetic compatibility we distinguish between immunity and emission of a particular disturbance. The emission of imbalance consists of measuring the current phase sequence different from the positive sequence injected by an unbalanced load into the PCC. This section introduces the most common index to assess the imbalance emission.

### **5.1. Conforming and nonconforming unbalance current**

Regarding the issue unbalance, for three-phase phase voltages Va, Vb, and Vc, and line cur‐ rents Ia, Ib, and Ic, symmetrical components at the fundamental frequency are considered, V +, V-, V0, I+, I- and I0. These are defined for the voltages by the following expressions:

$$\mathbf{V\_{\cdot}} = \frac{1}{3} \left( \mathbf{V\_{a}} + \mathbf{a}^{2} \mathbf{V\_{b}} + \mathbf{a} \mathbf{V\_{c}} \right) \tag{33}$$

The non conforming current is the current balance. In terms of symmetrical components,

( ) 2 sin 2 ( )

= + -

p

Finally, the three phase values (Ida, Idb, Idc) are obtained from the inverse transformation of Fortescue. Although the author does not indicate a specific index of unbalance, we have con‐ sidered the ratio of norm of non-conforming currents with respect to the norm of the real

To define an index that takes into account the charge imbalance, be chosen as the reference phase current phase extracted with the minimum RMS value. For further analysis this phase will be considered as phase 'a'. According to the procedure developed by the authors, [19], for estimating the parameters, it is assumed that the equivalent linear and balanced load is made up by three linear loads, balanced, equal to the estimated linear load for the phase 'a'. Thus, the current absorbed by the phases 'b' and 'c' for the same RL series load, estimated on

These currents are called "balanced linear currents" and only responsible for the unbalance and distortion is the delivery system. The difference between the measured actual current in

These currents expresses how the phases 'b' and 'c' differ from ideal reference conditions in terms of phase unbalance and distortion. On the other hand, it is possible to calculate non‐ linear currents *inlj* (t) (j = b, c) for phases 'b' and 'c' in the manner provided in the previous

each phase and the calculated ideal current is called "unbalanced non-linear current",

*blj kj kj*

1 a

**5.2. Balanced linear currents and unbalanced non-linear currents**

*k*

current, NC\_unb.

phase 'a', are

=

V

*i t kf t*

*<sup>n</sup> kj*

d- - n- I =I -I (40)

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Evaluation of the Distortion and Unbalance Emission Levels in Electric Networks

d0 0 n0 I =I -I (41)

<sup>å</sup> **Zk** (42)

() () () ; , *unlj j blj i t i t i t j bc* =- = (43)

() () () ; , *uj unlj nlj i t i t i t j bc* =- = (44)

( <sup>1</sup> )

 qj

*j bc*

=

,

$$\mathbf{V\_0 = \frac{1}{3}(V\_\mathrm{a} + V\_\mathrm{b} + V\_\mathrm{c})} \tag{34}$$

$$\mathbf{I}\_{\mathbf{n}^\*} = \mathbf{I}\_\* \tag{35}$$

Where complex number a=exp(j2π/3). Similarly symmetrical components of currents are de‐ fined. The conforming current is the current that retains the same level of unbalance that the three-phase voltages, and coincides with the positive sequence current of the load current. Thus, the conforming current accomplishes all the active power and reactive power of posi‐ tive sequence.

$$\mathbf{Z}\_{+} = \frac{\mathbf{V}\_{+}}{\mathbf{I}\_{+}} \tag{36}$$

The ratio between V + and I + determines the impedance to the positive sequence current

$$\mathbf{I}\_{\rm n-} = \frac{\mathbf{V}\_{\rm \cdot}}{\mathbf{Z}\_{\rm \cdot}} = \mathbf{I}\_{\rm \cdot} \frac{\mathbf{V}\_{\rm \cdot}}{\mathbf{V}\_{\rm \cdot}} \tag{37}$$

The negative sequence component and zero sequence component of the conforming current will be in the same proportion as the sequence components of voltage, that is,

$$\mathbf{I}\_{\rm r0} = \frac{\mathbf{V}\_0}{\mathbf{Z}\_\star} = \mathbf{I}\_\star \frac{\mathbf{V}\_0}{\mathbf{V}\_\star} \tag{38}$$

$$\mathbf{I}\_{\mathbf{d}\star} = \mathbf{0} \tag{39}$$

The non conforming current is the current balance. In terms of symmetrical components,

load into the PCC. This section introduces the most common index to assess the imbalance

Regarding the issue unbalance, for three-phase phase voltages Va, Vb, and Vc, and line cur‐ rents Ia, Ib, and Ic, symmetrical components at the fundamental frequency are considered, V +,

> ( ) <sup>2</sup> - a bc <sup>1</sup> V = V +a V +aV

( ) 0 abc <sup>1</sup> V = V +V +V

Where complex number a=exp(j2π/3). Similarly symmetrical components of currents are de‐ fined. The conforming current is the current that retains the same level of unbalance that the three-phase voltages, and coincides with the positive sequence current of the load current. Thus, the conforming current accomplishes all the active power and reactive power of posi‐

> + + + <sup>V</sup> Z =

The ratio between V + and I + determines the impedance to the positive sequence current

V V I = =I

will be in the same proportion as the sequence components of voltage, that is,


The negative sequence component and zero sequence component of the conforming current

0 0 n0 + + +

V V I = =I

<sup>3</sup> (33)

<sup>3</sup> (34)

n+ + I =I (35)

<sup>I</sup> (36)

Z V (37)

Z V (38)

d+ I 0 = (39)

V-, V0, I+, I- and I0. These are defined for the voltages by the following expressions:

**5.1. Conforming and nonconforming unbalance current**

emission.

266 Power Quality Issues

tive sequence.

$$\mathbf{I}\_{\mathbf{d}\_{\text{-}}} = \mathbf{I}\_{\text{-}} \mathbf{-I}\_{\text{n-}} \tag{40}$$

$$\mathbf{I}\_{\rm d0} = \mathbf{I}\_0 \cdot \mathbf{I}\_{\rm r0} \tag{41}$$

$$\dot{H}\_{kj}(t) = \sum\_{k=1}^{n} \frac{\mathbf{V}\_{kj}}{\left| \mathbf{Z}\_{ka} \right|} \sqrt{2} \sin \left( 2\pi k f\_1 t + (\theta\_{kj} - \phi\_{kj}) \right) \tag{42}$$

$$j = b\_r c$$

Finally, the three phase values (Ida, Idb, Idc) are obtained from the inverse transformation of Fortescue. Although the author does not indicate a specific index of unbalance, we have con‐ sidered the ratio of norm of non-conforming currents with respect to the norm of the real current, NC\_unb.

### **5.2. Balanced linear currents and unbalanced non-linear currents**

To define an index that takes into account the charge imbalance, be chosen as the reference phase current phase extracted with the minimum RMS value. For further analysis this phase will be considered as phase 'a'. According to the procedure developed by the authors, [19], for estimating the parameters, it is assumed that the equivalent linear and balanced load is made up by three linear loads, balanced, equal to the estimated linear load for the phase 'a'. Thus, the current absorbed by the phases 'b' and 'c' for the same RL series load, estimated on phase 'a', are

$$\dot{i}\_{umlj}(t) = \dot{i}\_j(t) - \dot{i}\_{blj}(t) \quad ; \qquad j = b, c \tag{43}$$

These currents are called "balanced linear currents" and only responsible for the unbalance and distortion is the delivery system. The difference between the measured actual current in each phase and the calculated ideal current is called "unbalanced non-linear current",

$$i\_{uj}(t) = i\_{umlj}(t) - i\_{nlj}(t) \quad ; \qquad j = b, c \tag{44}$$

These currents expresses how the phases 'b' and 'c' differ from ideal reference conditions in terms of phase unbalance and distortion. On the other hand, it is possible to calculate non‐ linear currents *inlj* (t) (j = b, c) for phases 'b' and 'c' in the manner provided in the previous section. Assuming that it is possible to separate the contribution of the distortion only by subtracting the nonlinear current *inlj* (t) of *iunlj* (t) in the corresponding phase, then,

$$\frac{\left\|\bar{i}\_{\mu}\right\|}{\left\|\bar{i}\_{nl}\right\|} \times 100 \left(\%\right) \tag{45}$$

tively, for each of the loads and for the whole of them. This time the harmonic power identi‐

PT(W) 3.5433x104 1.2740x104 4.2502x103 1.8443x104 PH(W) -3.4792 -2.4387 -3.7266 2.6861

Table 9 presents the usual distortion indices. They identify the sources of distortion except index HPI. This is based on the direction of power flows for each harmonic between net‐ work and load, and masks the power unbalance due to it. However, no information is pro‐

On the other hand, NC and NL indices identify the load 1 and the load 2 as non-linear, and

ITDD 25.86 59.53 86.35 1.27 HPI 25.97 39.67 86.56 35.59 NC 18.75 40.72 73.64 0.50 NL 16.80 34.02 83.41 0.20

characterized the conformity of the current waveform of each load with the balanced sinus‐ oidal waveform. The remaining indices identify unbalance responsability. Both identify the

> ITDD+ 46.16 59.53 89.21 64.67 NC\_unb 26.71 0.27 30.27 47.14 UC 41.19 0.29 25.38 68.99

One issue to note is that NC\_unb index is obtained by applying the symmetrical compo‐ nents, while the UC not, this could lead to it not identify a supply voltage of negative se‐

**Three loads Load 1 Load 2 Load 3**

**Three loads Load 1 Load 2 Load 3**

, NC\_unb and UC. The first

**Three loads Load 1 Load 2 Load 3**

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269

fies the first two loads as non-linear and third load as linear.

**Table 8.** Harmonic and total active powers for unbalance loads.

**Table 9.** PQ indices in the practical case with unbalance loads.

Table 10 presents the values of the unbalance indices ITDD+

balanced load (load 1) and assign a value to unbalance loads.

**Table 10.** Indices of unbalance in the practical case with asymmetrical conditions.

vided on the issue of unbalance.

the load 3 as linear.

quence.

These currents expresses how the phases 'b' and 'c' differ from ideal reference conditions on‐ ly in terms of phase unbalance.

Once they have been introduced all these current components, it is possible to determine the degree of unbalance of a three phase load through the following definition of "unbalance current index",

$$\begin{aligned} \left\| \dot{i}\_u \right\| &= \sqrt{\sum\_{j=b,c} I\_{uj}^2} \quad \left\| \dot{i}\_{nl} \right\| = \sqrt{\sum\_{j=a,b,c} I\_{nl\_j}^2} \\\ I\_{uj} &= \sqrt{\sum\_{\forall k} I\_{kuj}^2} \quad I\_{nlj} = \sqrt{\sum\_{\forall k} I\_{kul\_j}^2} \end{aligned} \tag{46}$$

Where RMS values Iuj and Ij and norms of the set phase currents are defined as follow,

$$V\_e = \sqrt{\frac{V\_{ab}^2 + V\_{bc}^2 + V\_{ca}^2}{9}}\tag{47}$$

Ikuj and Iknlj are the RMS values of corresponding harmonic components of *iuj* (t) and *inlj*(t). Defined (46) has the disadvantage that for linear unbalanced loads takes very high values, even infinite. So, here has changed their definition by making the rate against the norm of the real current.

Finally it is also possible to evaluate the harmonic distortion on a three-phase basis by com‐ bining the values of the three different rates of each phase in a single index defined as the ratio between the norm of non-linear currents and the norm of the load currents.

### **5.3. Practical case: Digital simulation**

As a case study a three-phase nonlinear unbalanced system is considered. A set of three loads are connected at the PCC. The load 1 is a balanced three-phase topology formed by three single-phase rectifier with a RL branch into DC side. The load 2 is an unbalanced nonlinear load constituted by a single-phase rectifier with a RC branch into DC side in one phase and two resistors of different values in the remaining phases. Finally, the load 3 is a linear inductive and unbalanced load. Table 8 shows the total and harmonic powers, respec‐


tively, for each of the loads and for the whole of them. This time the harmonic power identi‐ fies the first two loads as non-linear and third load as linear.

**Table 8.** Harmonic and total active powers for unbalance loads.

section. Assuming that it is possible to separate the contribution of the distortion only by

These currents expresses how the phases 'b' and 'c' differ from ideal reference conditions on‐

Once they have been introduced all these current components, it is possible to determine the degree of unbalance of a three phase load through the following definition of "unbalance

> 2 2 , , , 2 2

> > 222 9 *ab bc ca*

Ikuj and Iknlj are the RMS values of corresponding harmonic components of *iuj* (t) and *inlj*(t). Defined (46) has the disadvantage that for linear unbalanced loads takes very high values, even infinite. So, here has changed their definition by making the rate against the norm of

Finally it is also possible to evaluate the harmonic distortion on a three-phase basis by com‐ bining the values of the three different rates of each phase in a single index defined as the

As a case study a three-phase nonlinear unbalanced system is considered. A set of three loads are connected at the PCC. The load 1 is a balanced three-phase topology formed by three single-phase rectifier with a RL branch into DC side. The load 2 is an unbalanced nonlinear load constituted by a single-phase rectifier with a RC branch into DC side in one phase and two resistors of different values in the remaining phases. Finally, the load 3 is a linear inductive and unbalanced load. Table 8 shows the total and harmonic powers, respec‐

ratio between the norm of non-linear currents and the norm of the load currents.

*VVV*

*u uj nl nl j bc j abc*

å å

= =

*i Ii I*

*uj kuj nlj kul k k*

" "

å å

*I II I*

= =

*e*

*V*

= =

*j*

and norms of the set phase currents are defined as follow,

+ + <sup>=</sup> (47)

*j*

*<sup>i</sup>* ´ (45)

(46)

subtracting the nonlinear current *inlj* (t) of *iunlj* (t) in the corresponding phase, then,

*nl i*

ly in terms of phase unbalance.

Where RMS values Iuj and Ij

**5.3. Practical case: Digital simulation**

the real current.

current index",

268 Power Quality Issues

100 %( ) *<sup>u</sup>*

Table 9 presents the usual distortion indices. They identify the sources of distortion except index HPI. This is based on the direction of power flows for each harmonic between net‐ work and load, and masks the power unbalance due to it. However, no information is pro‐ vided on the issue of unbalance.

On the other hand, NC and NL indices identify the load 1 and the load 2 as non-linear, and the load 3 as linear.


**Table 9.** PQ indices in the practical case with unbalance loads.

Table 10 presents the values of the unbalance indices ITDD+ , NC\_unb and UC. The first characterized the conformity of the current waveform of each load with the balanced sinus‐ oidal waveform. The remaining indices identify unbalance responsability. Both identify the balanced load (load 1) and assign a value to unbalance loads.


**Table 10.** Indices of unbalance in the practical case with asymmetrical conditions.

One issue to note is that NC\_unb index is obtained by applying the symmetrical compo‐ nents, while the UC not, this could lead to it not identify a supply voltage of negative se‐ quence.

### **6. Practical cases: Experimental results**

In the order to perform a validation of the results of simulations and verify the stability of the indices, has been built an experimental platform consists of three single-phase rectifiers connected in star and fed directly from the supply network. On the DC side of each rectifier has been connected a parallel RC branch, composed of a variable resistor and a capacitor 2200 μF, thus forming a nonlinear load, see Figure 5.

Due to variations in the supply voltage throughout the day, small variations are produced in the active power consumed by the load. Analysis of Table 11, it follows that, as corre‐ sponding to the nonlinearity of the load, the total active harmonic power is negative. Fur‐ thermore. it can be seen as the values of total active harmonic power (PH) are very small compared to the active power of fundamental harmonic. Moreover, as expected, there was a small value of VTDD throughout the day, about 3%, while the value of ITDD is considerably higher, around 78%. Figure 7 (a) shows the variations of VTDD throughout the day, where‐ as in Figure 7 (b) shows the variations of ITDD along test system and includes the results of

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271

For unbalancing the load has changed the value of the resistances of each rectifier DC side, so that R1 = 80 Ω, R2=120 Ω and R3 = 484 Ω, while the capacitor is the same in the three loads, 2200 μF. In Figure 8 (a) shows the waveforms of voltages (supply network) whereas the figure 8 (b) shows the waveforms of currents resulting from the measurements taken.

Table 12 shows the values of total active power (PT) consumed by the load on the three measurements made throughout the session, as well as the values of total active harmonic

Figure 9 shows how the measurement system includes all of the daily variation harmonic content and unbalance of the supply network voltage, whereas in Figure 9 (b) shows the dai‐

P1 (W) 993.43 714.46 194.32 1041.80 752.64 202.11 1037.50 751.76 200.94

PTH (W) -30.46 1958.80 1951.10

PT (W) 1871.80 1996.60 1990.20

PT1 (W) 1902.20 -37.82 -39.13

**Table 12.** Active powers of the main harmonics of the test system in Figure 4 with Non lineal and unbalanced load

The experimental results confirm the simulation results on the information provided by the PQ indices. The measurements show that for a typical load balanced/unbalanced nonlinear connected to the supply network, all the indices analyzed included some variations to changes of TDD voltage within a reasonable range. In any case, the index NC\_unb respect the degree of unbalance, is the index experienced less variations. This index is defined from

**M3 M15 M21** Phase L1 Phase L2 Phase L3 Phase L1 Phase L2 Phase L3 Phase L1 Phase L2 Phase L3

the different rates to be evaluated.

(Case B).

**6.2. Case B: Non lineal and unbalanced load**

power (PTH), and active power for the fundamental (PT1).

ly trend of results unbalanced indices calculated for the same period.

The measurement system consists of a data acquisition card (dspace-CP1104) and a signal conditioning system formed by three voltage sensors (LEM LV25-P) and three current sen‐ sors (LEM LA35-NP), thus the voltage and current signals are taken simultaneously, with‐ out introducing any phase change that could affect the accuracy of measurements. For data acquisition and processing, has developed a virtual instrument using Matlab and Control‐ Desk. This instrument stores the instantaneous values of each phase voltage and line cur‐ rent. The configuration of the virtual instrument was made following the recommendations EN 61 000-4-7 and EN 61 000-4-30, so that has been used window equal to five cycles of the fundamental component and a sampling frequency of 6400 Hz, thus avoiding problems of aliasing and leakage errors.

To evaluate the theory and the results obtained in simulations has been carried out daily measurements along a day at regular intervals of one hour. In this way has been possible to evaluate the changes into indices for two different cases, a non lineal balanced load(case A) and another case with non lineal unbalanced load (case B). In both cases the supply system network was used for feeding the loads.

### **6.1. Case A: Non linear and balanced load**

In this case the load connected to the DC side of the three rectifiers consists of a resistance of 120 Ω in parallel with a capacitor 2200 μF. In Figure 6 (a) displays the voltage waveforms of the three phases whereas the Figure 6 (b) shows the waveforms of the currents taken from one of the measurements performed on the test system.

Table 11 shows the values of total active power (PT) consumed by the load on the three dif‐ ferent measurements made throughout the session, as well as fundamental harmonic (P1) and the values of total active harmonic power (PH).


**Table 11.** Active powers of the main harmonics of the test system in Figure 4 with Non linear and balanced load (Case A).

Due to variations in the supply voltage throughout the day, small variations are produced in the active power consumed by the load. Analysis of Table 11, it follows that, as corre‐ sponding to the nonlinearity of the load, the total active harmonic power is negative. Fur‐ thermore. it can be seen as the values of total active harmonic power (PH) are very small compared to the active power of fundamental harmonic. Moreover, as expected, there was a small value of VTDD throughout the day, about 3%, while the value of ITDD is considerably higher, around 78%. Figure 7 (a) shows the variations of VTDD throughout the day, where‐ as in Figure 7 (b) shows the variations of ITDD along test system and includes the results of the different rates to be evaluated.

### **6.2. Case B: Non lineal and unbalanced load**

**6. Practical cases: Experimental results**

270 Power Quality Issues

2200 μF, thus forming a nonlinear load, see Figure 5.

aliasing and leakage errors.

A).

network was used for feeding the loads.

**6.1. Case A: Non linear and balanced load**

one of the measurements performed on the test system.

and the values of total active harmonic power (PH).

In the order to perform a validation of the results of simulations and verify the stability of the indices, has been built an experimental platform consists of three single-phase rectifiers connected in star and fed directly from the supply network. On the DC side of each rectifier has been connected a parallel RC branch, composed of a variable resistor and a capacitor

The measurement system consists of a data acquisition card (dspace-CP1104) and a signal conditioning system formed by three voltage sensors (LEM LV25-P) and three current sen‐ sors (LEM LA35-NP), thus the voltage and current signals are taken simultaneously, with‐ out introducing any phase change that could affect the accuracy of measurements. For data acquisition and processing, has developed a virtual instrument using Matlab and Control‐ Desk. This instrument stores the instantaneous values of each phase voltage and line cur‐ rent. The configuration of the virtual instrument was made following the recommendations EN 61 000-4-7 and EN 61 000-4-30, so that has been used window equal to five cycles of the fundamental component and a sampling frequency of 6400 Hz, thus avoiding problems of

To evaluate the theory and the results obtained in simulations has been carried out daily measurements along a day at regular intervals of one hour. In this way has been possible to evaluate the changes into indices for two different cases, a non lineal balanced load(case A) and another case with non lineal unbalanced load (case B). In both cases the supply system

In this case the load connected to the DC side of the three rectifiers consists of a resistance of 120 Ω in parallel with a capacitor 2200 μF. In Figure 6 (a) displays the voltage waveforms of the three phases whereas the Figure 6 (b) shows the waveforms of the currents taken from

Table 11 shows the values of total active power (PT) consumed by the load on the three dif‐ ferent measurements made throughout the session, as well as fundamental harmonic (P1)

> PT (W) 2134.00 2245.00 2210.00 P1 (W) 2169.00 2288.90 2254.40 PH (W) -35.02 -43.85 -44.41

**Table 11.** Active powers of the main harmonics of the test system in Figure 4 with Non linear and balanced load (Case

**M 3 M 15 M 21**

For unbalancing the load has changed the value of the resistances of each rectifier DC side, so that R1 = 80 Ω, R2=120 Ω and R3 = 484 Ω, while the capacitor is the same in the three loads, 2200 μF. In Figure 8 (a) shows the waveforms of voltages (supply network) whereas the figure 8 (b) shows the waveforms of currents resulting from the measurements taken.

Table 12 shows the values of total active power (PT) consumed by the load on the three measurements made throughout the session, as well as the values of total active harmonic power (PTH), and active power for the fundamental (PT1).

Figure 9 shows how the measurement system includes all of the daily variation harmonic content and unbalance of the supply network voltage, whereas in Figure 9 (b) shows the dai‐ ly trend of results unbalanced indices calculated for the same period.


**Table 12.** Active powers of the main harmonics of the test system in Figure 4 with Non lineal and unbalanced load (Case B).

The experimental results confirm the simulation results on the information provided by the PQ indices. The measurements show that for a typical load balanced/unbalanced nonlinear connected to the supply network, all the indices analyzed included some variations to changes of TDD voltage within a reasonable range. In any case, the index NC\_unb respect the degree of unbalance, is the index experienced less variations. This index is defined from the fundamental harmonic symmetrical components, and therefore undergone fewer changes for a given load.

with respect to the balanced sinusoidal waveform positive sequence. This index, as the ITDD, characterized the set of waveforms of a three phase system but will not identify un‐ balanced loads. Two indexes to locate unbalance are introduced: Current Unbalance index, UC and Non-Conforming to the unbalance, NC\_unb. Both identify the loads that are sources of unbalance, however, the UC would not detect the case of a supply voltage of negative se‐

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273

In conclusion, in the text above have reviewed the potential problems associated with the assessment of power quality in electrical installations. In particular, we have introduced har‐ monic distortion and unbalanced to characterize the voltage and current waveforms. A com‐ parative analysis of the most common indices was made. Thus, to determine responsible for the generation of distortion through measurements made in a single measurement section, none of the indexes given is capable of resolving the issue reliably. However, since in prac‐ tice all loads are nonlinear, the NL is an appropriate index for assessing the distortion source because it is little affected by the imbalance and distortion. For the determination of

> *V<sup>ϕ</sup>* <sup>2</sup> <sup>−</sup> *<sup>V</sup>ϕ*<sup>1</sup> 2

*Iϕ* <sup>2</sup> <sup>−</sup> *<sup>I</sup>ϕ*<sup>1</sup> 2

*V<sup>ϕ</sup>* <sup>2</sup> <sup>−</sup> *<sup>V</sup>ϕ*<sup>1</sup> 2

*Iϕ* <sup>2</sup> <sup>−</sup> *<sup>I</sup>ϕ*<sup>1</sup> 2

Three-Phase Total Harmonic Distortion of Current and Voltage,

*Iϕ* <sup>2</sup> =

*Iϕ*1 <sup>2</sup> =

*V<sup>ϕ</sup>* <sup>2</sup> =

*Vϕ*<sup>1</sup> <sup>2</sup> = *Vϕ*<sup>2</sup> <sup>2</sup> <sup>+</sup> *<sup>V</sup>ϕ*<sup>3</sup>

*Iϕ*2 <sup>2</sup> <sup>+</sup> *<sup>I</sup>ϕ*<sup>3</sup>

*Vϕ*<sup>2</sup> <sup>2</sup> <sup>+</sup> *<sup>V</sup>ϕ*<sup>3</sup>

*Iϕ*2 <sup>2</sup> <sup>+</sup> *<sup>I</sup>ϕ*<sup>3</sup> <sup>2</sup> <sup>+</sup> *<sup>V</sup>ϕ*<sup>4</sup>

<sup>2</sup> <sup>+</sup> *<sup>I</sup>ϕ*<sup>4</sup>

<sup>2</sup> <sup>+</sup> *<sup>I</sup>ϕ*<sup>4</sup>

*Iϕ* 2

*Iϕ*1 2

<sup>2</sup> <sup>+</sup> *<sup>V</sup>ϕ*<sup>4</sup>

*V<sup>ϕ</sup>* 2

<sup>2</sup> + ... + *<sup>I</sup>ϕ<sup>N</sup>*

*Vϕ*<sup>1</sup> 2

<sup>2</sup> + ... + *<sup>I</sup>ϕ<sup>N</sup>*

<sup>2</sup> + ... + *<sup>V</sup>ϕ<sup>N</sup>*

2

<sup>2</sup> + ... + *<sup>V</sup>ϕ<sup>N</sup>*

2

2

2

the issue of unbalance NC\_unb index has shown a good performance.

<sup>2</sup> <sup>+</sup> *Vca* 2

<sup>2</sup> <sup>+</sup> *Vbc*

3

<sup>2</sup> <sup>+</sup> *Ib*

Voltage Total Harmonic Distortion, *VTHD <sup>ϕ</sup>* <sup>=</sup>

Current Total Harmonic Distortion, *ITHD <sup>ϕ</sup>* <sup>=</sup>

Voltage Total Demand Distortion, *VTDD <sup>ϕ</sup>* <sup>=</sup>

Current Total Demand Distortion, *ITDD <sup>ϕ</sup>* <sup>=</sup>

<sup>2</sup> ; *VTHD*

<sup>3</sup>*<sup>ϕ</sup>* <sup>=</sup> *Ve*

<sup>2</sup> <sup>−</sup> *Ve* <sup>1</sup> 2

*Ve* <sup>1</sup> 2

<sup>2</sup> <sup>−</sup> *Ie* <sup>1</sup> 2

*Ie* 1

9

<sup>2</sup> <sup>+</sup> *Ic* 2

quence.

**Summary of indices**

Effective Voltage, *Ve* <sup>=</sup> *Vab*

Effective Current, *Ie* <sup>=</sup> *Ia*

*ITHD* <sup>3</sup>*<sup>ϕ</sup>* <sup>=</sup> *Ie*

### **7. Discussion of the results and conclusions**

The strong presence of waveforms of voltage and current distorted and/or unbalanced in electric power systems has driven the need to determine the contribution to the deteriora‐ tion of the PQ of consumers connected to supply networks. The method of the direction of power flow has been widely used to identify the locations of harmonic sources. However, this method is unable to solve this task in all situations. This procedure does not locate a source of distortion in the case that there are multiple harmonics sources connected to the PCC. To overcome this situation, other procedures have been introduced under the con‐ straint of seeking a solution, based on the realization of measures in only one section of the PCC. These methods have introduced new indices as they are, HPI, NC and NL, that ad‐ vance but which do not solve the problem in all situations. Thus:


Respect to the issues of unbalance loads produced by asymmetrical operation has been in‐ troduced ITDD+ index as a measure of non-conformity of the waveform of actual current with respect to the balanced sinusoidal waveform positive sequence. This index, as the ITDD, characterized the set of waveforms of a three phase system but will not identify un‐ balanced loads. Two indexes to locate unbalance are introduced: Current Unbalance index, UC and Non-Conforming to the unbalance, NC\_unb. Both identify the loads that are sources of unbalance, however, the UC would not detect the case of a supply voltage of negative se‐ quence.

In conclusion, in the text above have reviewed the potential problems associated with the assessment of power quality in electrical installations. In particular, we have introduced har‐ monic distortion and unbalanced to characterize the voltage and current waveforms. A com‐ parative analysis of the most common indices was made. Thus, to determine responsible for the generation of distortion through measurements made in a single measurement section, none of the indexes given is capable of resolving the issue reliably. However, since in prac‐ tice all loads are nonlinear, the NL is an appropriate index for assessing the distortion source because it is little affected by the imbalance and distortion. For the determination of the issue of unbalance NC\_unb index has shown a good performance.

### **Summary of indices**

the fundamental harmonic symmetrical components, and therefore undergone fewer

The strong presence of waveforms of voltage and current distorted and/or unbalanced in electric power systems has driven the need to determine the contribution to the deteriora‐ tion of the PQ of consumers connected to supply networks. The method of the direction of power flow has been widely used to identify the locations of harmonic sources. However, this method is unable to solve this task in all situations. This procedure does not locate a source of distortion in the case that there are multiple harmonics sources connected to the PCC. To overcome this situation, other procedures have been introduced under the con‐ straint of seeking a solution, based on the realization of measures in only one section of the PCC. These methods have introduced new indices as they are, HPI, NC and NL, that ad‐

**•** The method of direction of harmonic power flow fails when there is more than a nonlin‐ ear load connected to the same PCC. The measurement of PH can be positive at the termi‐ nals of a nonlinear load. This is because the harmonic powers up the sum of PH are the contribution of power flow of two opposing, in the sense from load to network and an‐ other from network to load. The result for each harmonic corresponds to the prevailing power flow. Therefore, for the identification of sources of distortion, PH is a not suitable indicator and would have to resort the study of the individual harmonics powers. How‐ ever, this method is the only one that unambiguously identifies the linear loads, including

**•** The index of harmonic phase, HPI, overcomes the drawbacks mentioned for the method of harmonic power direction, using the RMS values of current in one direction or another in the PCC. Moreover presents an adequate stability to changes in network distortion. However, result in errors for linear loads on systems with unbalanced and with the pres‐

**•** The non-conforming current index, NC, while indicating the current component of the load presented to the voltage distortion front, is not useful from the practical point of view since it does not discriminate linear loads. In the case of the presence of capacitors is identified as distortion source. Moreover, this index shows more variation compared to

**•** The non-linear current index, NL, it seems appropriate to characterize the current of a nonlinear load distorted. It also presents few variations to changes in the distortion of the mains voltage. However, the rate can result in errors in linear loads with different topolo‐

Respect to the issues of unbalance loads produced by asymmetrical operation has been in‐ troduced ITDD+ index as a measure of non-conformity of the waveform of actual current

other indices variations in the conditions of distortion of the mains.

gies including the RL parallel and/or capacitive branches.

changes for a given load.

272 Power Quality Issues

**7. Discussion of the results and conclusions**

vance but which do not solve the problem in all situations. Thus:

those with capacitor banks for compensation.

ence of the capacitor bank.

Effective Voltage, *Ve* <sup>=</sup> *Vab* <sup>2</sup> <sup>+</sup> *Vbc* <sup>2</sup> <sup>+</sup> *Vca* 2 9 Effective Current, *Ie* <sup>=</sup> *Ia* <sup>2</sup> <sup>+</sup> *Ib* <sup>2</sup> <sup>+</sup> *Ic* 2 3 Voltage Total Harmonic Distortion, *VTHD <sup>ϕ</sup>* <sup>=</sup> *V<sup>ϕ</sup>* <sup>2</sup> <sup>−</sup> *<sup>V</sup>ϕ*<sup>1</sup> 2 *Vϕ*<sup>1</sup> <sup>2</sup> = *Vϕ*<sup>2</sup> <sup>2</sup> <sup>+</sup> *<sup>V</sup>ϕ*<sup>3</sup> <sup>2</sup> <sup>+</sup> *<sup>V</sup>ϕ*<sup>4</sup> <sup>2</sup> + ... + *<sup>V</sup>ϕ<sup>N</sup>* 2 *Vϕ*<sup>1</sup> 2 Current Total Harmonic Distortion, *ITHD <sup>ϕ</sup>* <sup>=</sup> *Iϕ* <sup>2</sup> <sup>−</sup> *<sup>I</sup>ϕ*<sup>1</sup> 2 *Iϕ*1 <sup>2</sup> = *Iϕ*2 <sup>2</sup> <sup>+</sup> *<sup>I</sup>ϕ*<sup>3</sup> <sup>2</sup> <sup>+</sup> *<sup>I</sup>ϕ*<sup>4</sup> <sup>2</sup> + ... + *<sup>I</sup>ϕ<sup>N</sup>* 2 *Iϕ*1 2 Voltage Total Demand Distortion, *VTDD <sup>ϕ</sup>* <sup>=</sup> *V<sup>ϕ</sup>* <sup>2</sup> <sup>−</sup> *<sup>V</sup>ϕ*<sup>1</sup> 2 *V<sup>ϕ</sup>* <sup>2</sup> = *Vϕ*<sup>2</sup> <sup>2</sup> <sup>+</sup> *<sup>V</sup>ϕ*<sup>3</sup> <sup>2</sup> <sup>+</sup> *<sup>V</sup>ϕ*<sup>4</sup> <sup>2</sup> + ... + *<sup>V</sup>ϕ<sup>N</sup>* 2 *V<sup>ϕ</sup>* 2 Current Total Demand Distortion, *ITDD <sup>ϕ</sup>* <sup>=</sup> *Iϕ* <sup>2</sup> <sup>−</sup> *<sup>I</sup>ϕ*<sup>1</sup> 2 *Iϕ* <sup>2</sup> = *Iϕ*2 <sup>2</sup> <sup>+</sup> *<sup>I</sup>ϕ*<sup>3</sup> <sup>2</sup> <sup>+</sup> *<sup>I</sup>ϕ*<sup>4</sup> <sup>2</sup> + ... + *<sup>I</sup>ϕ<sup>N</sup>* 2 *Iϕ* 2 Three-Phase Total Harmonic Distortion of Current and Voltage, *ITHD* <sup>3</sup>*<sup>ϕ</sup>* <sup>=</sup> *Ie* <sup>2</sup> <sup>−</sup> *Ie* <sup>1</sup> 2 *Ie* 1 <sup>2</sup> ; *VTHD* <sup>3</sup>*<sup>ϕ</sup>* <sup>=</sup> *Ve* <sup>2</sup> <sup>−</sup> *Ve* <sup>1</sup> 2 *Ve* <sup>1</sup> 2

$$\begin{aligned} & \text{True-Phase} \quad \text{Total} \quad \text{Demand} \quad \text{Distortion} \quad \text{of} \quad \text{Current} \quad \text{and} \quad \text{Voltage}, \\ & \text{ITIDD}\_{3\phi} \neq \sqrt{\frac{I\_s^2 - I\_{c1}^2}{I\_c^2}} : \text{YIDD}\_{3\phi} \neq \sqrt{\frac{V\_s^2 - V\_{c1}^2}{I\_c^2}} \\ & \text{Unbalanced} \quad \text{True-Phase} \quad \text{Total} \quad \text{Demand} \quad \text{Distortion} \quad \text{of} \quad \text{Voltage} \quad \text{and} \quad \text{Current} \\ & \text{VIDD}\_{3\phi} \neq \sqrt{\frac{V\_s^2 - V\_{c1+}^2}{I\_c^2}} : \quad \text{:} \quad \text{IIDD}\_{3\phi} \neq \sqrt{\frac{I\_s^2 - I\_{c1+}^2}{I\_c^2}} \\ & \text{The Harmonic Phase Index, } HPI = \frac{\mathbb{I}\\_\text{L}}{\mathbb{I}\\_\text{L}} \times 100 \text{ (\%)} \\ & \text{Non Collinear Index, } N\text{C} = \frac{\mathbb{I}\\_\text{L}}{\text{T}} \times 100 \text{ (\%)} \\ & \text{Unbalanced NonCollinear Index, } N\text{C}\_\text{-} \text{ and } \quad \text{\%} \quad \text{-} \quad \text{\%} \quad \text{-} \\ & \text{Non Linear Index, } NL = \frac{\mathbb{I}\\_\text{L}}{\mathbb{I}\\_\text{L}} \times 100 \text{ (\%)} \\ & \text{Update Curment Index, } MC = \frac{\mathbb{I}\\_\text{L}}{\mathbb{I}\\_\text{L}} \times 100 \text{ (\%)} \end{aligned}$$

[3] G.T. Heydt, E. Gunther, 1996 "Post-measurement processing of electric power quali‐

Evaluation of the Distortion and Unbalance Emission Levels in Electric Networks

http://dx.doi.org/10.5772/53373

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### **Acknowledgments**

This work is part of the project "Measurements system to assessment the sources of imbal‐ ance and harmonic distortion in electric distribution networks", DPI2010-17709, sponsored by the Ministry of economy and competitiveness, Government of Spain.

### **Author details**

Patricio Salmerón Revuelta and Alejandro Pérez Vallés

Departament of Electrical Engineering, E.T.S.I, Huelva University, Spain

### **References**


[3] G.T. Heydt, E. Gunther, 1996 "Post-measurement processing of electric power quali‐ ty data", IEEE Trans. on Power Delivery, Vol. 11, No. 4.

Three-Phase Total Demand Distortion of Current and Voltage,

Unbalance Three-Phase Total Demand Distortion of Voltage and Current,

× 100 (*%*)

*d*

× 100 (*%*)

This work is part of the project "Measurements system to assessment the sources of imbal‐ ance and harmonic distortion in electric distribution networks", DPI2010-17709, sponsored

[1] A. Menchetti, R. Sasdelli, *Measurement Problems in Power Quality Improvement*, ETEP,

[2] A. Ferrero, A. Menchetti, R. Sasdelli, *Measurement of the Electric Power Quality and Re‐*

*<sup>i</sup>* × 100 (*%*)

<sup>2</sup> <sup>−</sup> *Ie*1 + 2

> *Ie* 2

*ITDD* <sup>3</sup>*<sup>ϕ</sup>* <sup>=</sup> *Ie*

274 Power Quality Issues

3*ϕ* <sup>+</sup> <sup>=</sup> *Ve*

*VTDD*

<sup>2</sup> <sup>−</sup> *Ie* <sup>1</sup> 2

> <sup>2</sup> <sup>−</sup>*Ve*1 + 2

The Harmonic Phase Index, *HPI* <sup>=</sup> *IL*

Unbalanced Non Collinear Index, *NC* \_*unb* <sup>=</sup> *<sup>i</sup>*

*Ve*

Non Collinear Index, *NC* <sup>=</sup> *Id*

Non Linear Index, *NL* <sup>=</sup> *InLa*

**Acknowledgments**

**Author details**

**References**

Unbalanced Current Index, *UC* <sup>=</sup> *<sup>i</sup>*

<sup>2</sup> ; *VTDD*

<sup>3</sup>*<sup>ϕ</sup>* <sup>=</sup> *Ve*

<sup>2</sup> ; *ITDD* <sup>3</sup>*<sup>ϕ</sup>*

<sup>2</sup> <sup>−</sup> *Ve* <sup>1</sup> 2

*Ve* 2

<sup>+</sup> <sup>=</sup> *Ie*

*IS*

*<sup>I</sup>* × 100 (*%*)

*<sup>I</sup> <sup>a</sup>* × 100 (*%*)

*u i nl*

by the Ministry of economy and competitiveness, Government of Spain.

Departament of Electrical Engineering, E.T.S.I, Huelva University, Spain

*lated Problems*, ETEP, Vol. 6, No. 6, November/December 1996.

Patricio Salmerón Revuelta and Alejandro Pérez Vallés

vol. 4, No. 6, Nov/Dec, 1994.

*Ie*


[17] W. Xu, X. Liu y Y. Liu. *An Investigation on the Validity of Power-Direction Method for Harmonic Source Determination.* IEEE Transations on Power Delivery, Vol. 18, No. 1, January 2003.

**Chapter 11**

**Provisional chapter**

**High Frequency Harmonics Emission in Smart Grids**

**High Frequency Harmonics Emission in Smart Grids**

The term 'smart grid', is nowadays very often used in many publications and so far has not been explicitly defined, however it refers mainly to such an operation of electricity delivery process that allows to optimize energy efficiency by flexible interconnection of central and distributed generators through transmission and distribution system to industrial and consumer end-users [1], [3], [11], [13], [15], [17]. This functionality of power delivery system requires the use of power electronic converters at generation, consumer and grid operation levels. Harmonic pollution generated by power electronics converters is one of the key problems of integrating them compatibly with the power grid, especially when its rated power is high with relation to the grid's short-circuit power at connection point [18], [19], [20]. Contemporary power electronics converters has already reached rated power of several MW and are integrated even at the distribution level directly to medium voltage (MV) grid. Power electronics technologies used nowadays in high power and MV static converter increase the switching frequency significantly due to the availability of faster power electronic switches which allows to increase power conversion efficiency and decrease harmonic and inter-harmonic current distortion in frequency range up to 2 *kHz*. This trend significantly increases harmonic emission spectrum towards higher frequencies correlated with modulation frequency of switching conversion of power. Therefore typical harmonic analysis up to 2 *kHz* in many power electronics application requires to be extended up to frequency of 9 *kHz* which is the lowest frequency of typical electromagnetic interference analysis interest. Numerous problems related to current and voltage harmonic effects on contemporary power systems are commonly observed nowadays, also in frequency range 2 − 9 *kHz*. Levels and spectral content of current distortions injected into electric power grids are tending to increase despite the fact that the acceptable levels are determined by numerous

In recent years many of grid-side PWM boost converters of relatively high rated power have been introduced into power grid because of many advantages, like for example:

> ©2012 Luszcz, licensee InTech. This is an open access chapter distributed under the terms of the Creative Commons Attribution License (http://creativecommons.org/licenses/by/3.0), which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited. © 2013 Luszcz; licensee InTech. This is an open access article distributed under the terms of the Creative Commons Attribution License (http://creativecommons.org/licenses/by/3.0), which permits unrestricted use,

© 2013 Luszcz; licensee InTech. This is a paper distributed under the terms of the Creative Commons Attribution License (http://creativecommons.org/licenses/by/3.0), which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

distribution, and reproduction in any medium, provided the original work is properly cited.

Jaroslaw Luszcz

**1. Introduction**

Jaroslaw Luszcz

http://dx.doi.org/10.5772/52874

regulations [2], [3], [7], [9], [12], [14], [16].

Additional information is available at the end of the chapter

Additional information is available at the end of the chapter


**Provisional chapter**
