**Hybrid Gas Atomization for Powder Production**

Udo Fritsching and Volker Uhlenwinkel

*University of Bremen Germany* 

#### **1. Introduction**

98 Powder Metallurgy

Zhang, D., Zhou, D., Jiang, S., Wang, X. and Gong, S. (2004). Effects of porosity on the

Zhou, L. (2000). Processing Effects on Core-Shell Grain Formation in ZrO2 Modified BaTiO3

Aalto University, Department of Micro and Nanosciences, Research Groups Gas sensors,

http://nano.tkk.fi/en/research\_groups/electron\_physics/research/gas\_sensors/

Springer Science+Business Media, Available from: http://www.springerimages.com/ Electronic Circuits and Projects Forum, Available from: http://www.electro-tech-

electrode, *Sensors and Actuators A,* 112, pp. 94-100.

Ceramics, Ph.D Thesis, University of Cincinati.

online.com/

Available from:

electrical characteristics of current-limiting BaTiO3-based positive-temperaturecoefficient (PTC) ceramic thermistors coated with electroless nickel-phosphorus

> Atomization of a molten liquid melt is a versatile method for powder production. Main operational parameters and physical conditions for a suitable atomization process for different applications in powder production are:


Most atomization processes e.g. for metal powder production are gas atomization processes using twin fluid atomizers. For these applications, besides the use of standard atomizer types, relevant developments are ongoing to derive advanced atomizer concepts for improved powder products and energy and resources effective atomization processes.

Main aims of atomizer developments are:


In this contribution the development of gas atomization units is described, which utilize characteristic flow effects of a molten metal stream in relation to the flow of compressed gases for efficient fragmentation of liquids and melts. The interaction of gas and liquid melt in the twin-fluid atomization process is used for understanding and optimization of melt fragmentation processes.

#### **2. Atomization of liquids and melts**

Atomization of liquids (e.g., pure liquids, solutions, suspensions and emulsions, or melts) is a classic process engineering unit operation. The process of liquid atomization has applications in numerous industrial branches, for example, in chemical, mechanical, aerospace, and civil engineering as well as in material science and technology and metallurgy, food processing, pharmaceuticals, agriculture and forestry, environmental protection, medicine, and others.

Within atomization, the bulk fluid (continuous liquid phase) is transformed into a spray system (dispersed phase: droplets). The disintegration process itself is caused either by

Hybrid Gas Atomization for Powder Production 101

A common characteristic of the used variations of twin-fluid atomizers for molten metal atomisation is the vertical exit of the melt jet from the tundish via the (in most cases cylindrical) melt nozzle in the direction of gravity. Also in most cases the central melt jet stream is surrounded by a gas flow from a single (slit) jet configuration or a set of discrete gas jets, which are flowing in parallel direction to the melt flow or within an inclination angle of attack towards the melt stream. The coaxial atomizer gas usually exits the atomizer

Two main configurations and types of twin-fluid atomizers need to be distinguished within molten metal atomisation. The first kind is called the confined or close-coupled atomizer and the second kind is called the free-fall atomizer. Both concepts are illustrated in Figure 1.

Fig. 1. Gas atomization principles of melts: Close coupled atomizer (left) and free-fall

The gas flow in the close-coupled atomizer immediately covers the exiting melt jet. Within the confined atomizer the distance between gas exit and melt stream is much smaller than in the free-fall arrangement, where the melt jet moves a certain distance in the direction of gravity before the gas flow impinges onto the central melt jet. The close-coupled configuration generally tends to yield higher atomisation efficiencies (in terms of smaller particles at identical energy consumption) due to the lower distance between the gas and melt exits. But the confined atomizer type is more susceptible for freezing problems of the melt at the nozzle tip. This effect is due to the extensive cooling of the melt by the expanding gas flow, which exits in the close-coupled type nearby to the melt stream. During isentropic gas expansion the atomisation gas temperature is lowered (sometimes well below 0°C). Because of the close spatial coupling between gas and melt flow fields, this contributes to a rapid cooling of the melt at the tip of the melt nozzle. The freezing problem is relevant especially for spray forming applications. In this process, in all technical applications a discontinuous batch operation is performed (e.g. due to the batchwise melt preparation or the limited preform extend to be spray formed). The operational times of spray forming processes are ranging from several minutes up to approximately one hour. The thermal related freezing problem is most important in the initial phase of the process directly when the melt stream exits the nozzle for the first time. At that point the nozzle tip is still cool and needs to be heated first e.g. by the hot melt flow. This heating process lasts a certain time. Therefore, thermal related freezing problems are often to be observed in the first few

at high pressures with high kinetic energy.

atomizer (right)

seconds of a melt atomisation process.

intrinsic (e.g., potential) or extrinsic (e.g., kinetic) energy, where the liquid, which is typically fed into the process in the form of a liquid jet or sheet, is atomized either due to the kinetic energy contained in the liquid itself, by the interaction of the liquid sheet or jet with a (high-velocity) gas, or by means of mechanical energy delivered externally, e.g., by rotating devices.

The main purpose of technical atomization processes is the generation of a significantly increased gas–liquid interface in the dispersed multiphase system. All transfer processes across the gas–liquid phase boundary directly depend on the driving potential difference of the exchange property (heat, mass, or momentum) and the size of the exchange surface. This gas–liquid contact area in a dispersed spray system is correlated with the integral sum of the surfaces of all individual droplets within the spray. An increase in the relative interphase area in a dispersed system intensifies momentum, heat, and mass-transfer processes between the gas and liquid. The total flux of exchange within spray systems is thereby increased by several orders of magnitude.

Within the atomization process typically a liquid stream (jet or sheet) is disintegrated into a large number of droplets of various sizes. As all of the solid state materials as minerals, ceramics, glass and metals may be converted into the liquid state by melting, powders from all of these materials may be produced via atomization of the liquid melt and consecutive solidification of the droplets in the spray to achieve a powder.

The area of melt atomization differs in several ways and properties from a conventional atomization process (lets say from water or fuel atomization) due to the physical melt conditions as:


The general physics, devices and application of (conventional) atomization and spray processes have been reviewed and intensively published as e.g. in (Lefebvre, 1989; Bayvel & Orzechowski, 1993; Fritsching; 2006; Ashgriz, 2011).

#### **2.1 Gas atomization of liquid melts**

Several principle atomisation mechanisms and devices exist for disintegration of molten metals. An overview on molten metal atomisation techniques and devices is given e.g. by (Lawley, 1992; Bauckhage, 1992; Yule & Dunkley, 1994, and Nasr et al., 2002). In the area of metal powder production by atomisation of molten metals typically twin-fluid atomisation by means of inert gases is used. Main reasons for using this specific atomisation technique are:


intrinsic (e.g., potential) or extrinsic (e.g., kinetic) energy, where the liquid, which is typically fed into the process in the form of a liquid jet or sheet, is atomized either due to the kinetic energy contained in the liquid itself, by the interaction of the liquid sheet or jet with a (high-velocity) gas, or by means of mechanical energy delivered externally, e.g., by rotating

The main purpose of technical atomization processes is the generation of a significantly increased gas–liquid interface in the dispersed multiphase system. All transfer processes across the gas–liquid phase boundary directly depend on the driving potential difference of the exchange property (heat, mass, or momentum) and the size of the exchange surface. This gas–liquid contact area in a dispersed spray system is correlated with the integral sum of the surfaces of all individual droplets within the spray. An increase in the relative interphase area in a dispersed system intensifies momentum, heat, and mass-transfer processes between the gas and liquid. The total flux of exchange within spray systems is thereby

Within the atomization process typically a liquid stream (jet or sheet) is disintegrated into a large number of droplets of various sizes. As all of the solid state materials as minerals, ceramics, glass and metals may be converted into the liquid state by melting, powders from all of these materials may be produced via atomization of the liquid melt and consecutive

The area of melt atomization differs in several ways and properties from a conventional atomization process (lets say from water or fuel atomization) due to the physical melt

The general physics, devices and application of (conventional) atomization and spray processes have been reviewed and intensively published as e.g. in (Lefebvre, 1989; Bayvel &

Several principle atomisation mechanisms and devices exist for disintegration of molten metals. An overview on molten metal atomisation techniques and devices is given e.g. by (Lawley, 1992; Bauckhage, 1992; Yule & Dunkley, 1994, and Nasr et al., 2002). In the area of metal powder production by atomisation of molten metals typically twin-fluid atomisation by means of inert gases is used. Main reasons for using this specific atomisation technique





devices.

conditions as:

are:

the particles

by use of inert gases.

increased by several orders of magnitude.

solidification of the droplets in the spray to achieve a powder.


Orzechowski, 1993; Fritsching; 2006; Ashgriz, 2011).

**2.1 Gas atomization of liquid melts** 

substrate/deposit for compaction

A common characteristic of the used variations of twin-fluid atomizers for molten metal atomisation is the vertical exit of the melt jet from the tundish via the (in most cases cylindrical) melt nozzle in the direction of gravity. Also in most cases the central melt jet stream is surrounded by a gas flow from a single (slit) jet configuration or a set of discrete gas jets, which are flowing in parallel direction to the melt flow or within an inclination angle of attack towards the melt stream. The coaxial atomizer gas usually exits the atomizer at high pressures with high kinetic energy.

Two main configurations and types of twin-fluid atomizers need to be distinguished within molten metal atomisation. The first kind is called the confined or close-coupled atomizer and the second kind is called the free-fall atomizer. Both concepts are illustrated in Figure 1.

Fig. 1. Gas atomization principles of melts: Close coupled atomizer (left) and free-fall atomizer (right)

The gas flow in the close-coupled atomizer immediately covers the exiting melt jet. Within the confined atomizer the distance between gas exit and melt stream is much smaller than in the free-fall arrangement, where the melt jet moves a certain distance in the direction of gravity before the gas flow impinges onto the central melt jet. The close-coupled configuration generally tends to yield higher atomisation efficiencies (in terms of smaller particles at identical energy consumption) due to the lower distance between the gas and melt exits. But the confined atomizer type is more susceptible for freezing problems of the melt at the nozzle tip. This effect is due to the extensive cooling of the melt by the expanding gas flow, which exits in the close-coupled type nearby to the melt stream. During isentropic gas expansion the atomisation gas temperature is lowered (sometimes well below 0°C). Because of the close spatial coupling between gas and melt flow fields, this contributes to a rapid cooling of the melt at the tip of the melt nozzle. The freezing problem is relevant especially for spray forming applications. In this process, in all technical applications a discontinuous batch operation is performed (e.g. due to the batchwise melt preparation or the limited preform extend to be spray formed). The operational times of spray forming processes are ranging from several minutes up to approximately one hour. The thermal related freezing problem is most important in the initial phase of the process directly when the melt stream exits the nozzle for the first time. At that point the nozzle tip is still cool and needs to be heated first e.g. by the hot melt flow. This heating process lasts a certain time. Therefore, thermal related freezing problems are often to be observed in the first few seconds of a melt atomisation process.

Hybrid Gas Atomization for Powder Production 103

Fig. 2. Main components and areas of a conventional free-fall atomizer (From Czisch &

During operation of the free-fall atomizer, the gas mass flow rates of both gas nozzle systems are controlled by the primary and secondary gas pressures respectively (pressure levels are given as of overpressure) (Czisch & Fritsching, 2004). Problems may occur during atomizer operation if the pressure ratio between the primary and the secondary nozzle is improperly adjusted and an intense recirculation flow is generated. The applicable maximum gas pressure of the primary gas nozzle is limited by initial disturbances that may be generated on the liquid jet before reaching the atomization area. Therefore, the secondary gas pressure is limited also because the secondary gas mass flow rate determines the necessary primary gas mass flow rate for prevention of recirculation. This coupling of the two nozzle systems limits the applicability of the free-fall atomizer (Fritsching, 2004; Heck et

To improve the operating conditions of the free-fall atomizer it is intended to increase the gas pressures while the recirculation flow is still suppressed. In this case the recirculation gas flow underneath the secondary gas nozzle must be prevented in a different way. It is proposed here that a cylindrical ring device installed into the gas flow of the secondary gas nozzle can improve the atomization performance. The applied device utilizes the Coanda effect (Wille & Fernholz, 1965) and the injector principle to influence the local atomization gas direction. Within the confined flow device (called here the Coanda-ring) an underpressure zone is generated which deflects the gas flow downwards and increases the pressure difference between the inner zone and the ambient gas pressure. This downward reflection of the gas stream effectively increases the gas entrainment from outside the main flow and therefore increases the total gas mass flow rate. This effect increase becomes important because the liquid jet interaction within the secondary nozzle is increased and the

The improvement of the atomizer design and operating conditions is based on numerical investigations of the gas flow field of a conventional free-fall atomizer (primary and secondary gas nozzle; see figure 2). Nitrogen is used througout this study as atomizer gas. By applying a axisymmetric two-dimensional flow simulation it is assumed that the gas exit

x

Fritsching, 2008a, with permission)

al., 2000; Bergmann et al., 2001).

recirculation gas flow is suppressed.

**3.1 Numerical simulation of free-fall atomizer gas flow** 

primary gas nozzle

liquid/melt supply

primary gas

secondary gas nozzle secondary gas flow

recirculation gas flow

atomization zone

In addition to the thermal related freezing problem within the melt nozzle, also chemical or metallurgical related problems in melt delivery systems are found frequently. Not all of these problems are solved yet in melt atomisation applications. A range of problems arises from the possible change of material composition of the melt, or that of the tundish or nozzle material, due to possible melt/tundish reactions or melt segregational effects from diffusion. This reaction process kinetics is somewhat slower than the thermal freezing process kinetics mentioned before and may contribute to operational problems at a later temporal state of process operation.

Free-fall atomizers are much less problematic than close-coupled atomizers in terms of thermal freezing processes, as the melt jet stream and the gas stream are well separated at the exit of the melt from the delivery system (tundish exit). Therefore, the cooling of the melt due to the cold gas occurs at a later position than within close-coupled atomizers. The freefall atomizer obeys as an additional advantage in the frame of spray forming the possibility of controlled mechanical or pneumatic scanning and therefore oscillating the gas atomizer with respect to one axis. Also concepts of spatial/temporal distribution of segments of gas jets within the nozzle can be used for atomisation. By doing so, the free-fall atomizer gives the operator an additional degree of freedom with respect to the control and regulation of the mass flux distribution of droplets in the spray. This most important physical property of the spray within other atomizer nozzle systems can (within a running process) only be influenced by changing the atomizer gas pressure. By controlled scanning of the nozzle, the mass flux can also be distributed over a certain area (necessary e.g. for flat product spray forming).

### **3. Free-fall atomizer design for melts**

The design of a conventional free-fall atomizer is simple, robust and very reliable. Thus the free-fall atomizer concept has several applications in liquid processing. Free-fall atomizers are applied e.g. in spray drying facilities, in powder production devices, or in spray forming processes (Yule & Dunkley, 1994; Fritsching, 2008). Figure 1 shows a sketch of a conventional external mixing free-fall atomizer. The design is based on the combination of two gas nozzle systems, namely a primary and a secondary gas nozzle (Fritsching, & Bauckhage, 1992). The secondary nozzle is the main atomization unit. The concentric gas jets from the secondary nozzle impinge onto the central liquid jet that is disintegrated due to instabilities from the shearing action of the secondary gas flow and its relative velocity (Markus et al., 2002). The disintegration process of the liquid jet in the atomization zone is located underneath the secondary gas nozzle (Lohner et al., 2003; Heck, 1998). Due to this separation of the atomization area and the atomizer body, the free-fall atomizer is mainly used for atomization of viscous or high temperature liquids and melts.

Due to the inclination of the secondary gas flow, underneath the secondary gas nozzle a recirculation gas flow area may occur depending on the atomizer design and operation conditions. If the intensity of the recirculation flow is reasonably high, liquid ligaments or droplets are transported back to the atomizer body. Here, these sticking fragments may clog the gas and/or liquid orifices and negatively influence or even stop the atomization process. In common free-fall atomizer designs the recirculation gas flow is suppressed by the use of a primary gas nozzle. The primary gas flow is coflowing to the liquid jet thereby guiding the liquid into the atomization area without recirculation.

In addition to the thermal related freezing problem within the melt nozzle, also chemical or metallurgical related problems in melt delivery systems are found frequently. Not all of these problems are solved yet in melt atomisation applications. A range of problems arises from the possible change of material composition of the melt, or that of the tundish or nozzle material, due to possible melt/tundish reactions or melt segregational effects from diffusion. This reaction process kinetics is somewhat slower than the thermal freezing process kinetics mentioned before and may contribute to operational problems at a later

Free-fall atomizers are much less problematic than close-coupled atomizers in terms of thermal freezing processes, as the melt jet stream and the gas stream are well separated at the exit of the melt from the delivery system (tundish exit). Therefore, the cooling of the melt due to the cold gas occurs at a later position than within close-coupled atomizers. The freefall atomizer obeys as an additional advantage in the frame of spray forming the possibility of controlled mechanical or pneumatic scanning and therefore oscillating the gas atomizer with respect to one axis. Also concepts of spatial/temporal distribution of segments of gas jets within the nozzle can be used for atomisation. By doing so, the free-fall atomizer gives the operator an additional degree of freedom with respect to the control and regulation of the mass flux distribution of droplets in the spray. This most important physical property of the spray within other atomizer nozzle systems can (within a running process) only be influenced by changing the atomizer gas pressure. By controlled scanning of the nozzle, the mass flux can also be distributed over a certain area (necessary e.g. for flat product spray

The design of a conventional free-fall atomizer is simple, robust and very reliable. Thus the free-fall atomizer concept has several applications in liquid processing. Free-fall atomizers are applied e.g. in spray drying facilities, in powder production devices, or in spray forming processes (Yule & Dunkley, 1994; Fritsching, 2008). Figure 1 shows a sketch of a conventional external mixing free-fall atomizer. The design is based on the combination of two gas nozzle systems, namely a primary and a secondary gas nozzle (Fritsching, & Bauckhage, 1992). The secondary nozzle is the main atomization unit. The concentric gas jets from the secondary nozzle impinge onto the central liquid jet that is disintegrated due to instabilities from the shearing action of the secondary gas flow and its relative velocity (Markus et al., 2002). The disintegration process of the liquid jet in the atomization zone is located underneath the secondary gas nozzle (Lohner et al., 2003; Heck, 1998). Due to this separation of the atomization area and the atomizer body, the free-fall atomizer is mainly

Due to the inclination of the secondary gas flow, underneath the secondary gas nozzle a recirculation gas flow area may occur depending on the atomizer design and operation conditions. If the intensity of the recirculation flow is reasonably high, liquid ligaments or droplets are transported back to the atomizer body. Here, these sticking fragments may clog the gas and/or liquid orifices and negatively influence or even stop the atomization process. In common free-fall atomizer designs the recirculation gas flow is suppressed by the use of a primary gas nozzle. The primary gas flow is coflowing to the liquid jet thereby guiding the

used for atomization of viscous or high temperature liquids and melts.

liquid into the atomization area without recirculation.

temporal state of process operation.

**3. Free-fall atomizer design for melts** 

forming).

Fig. 2. Main components and areas of a conventional free-fall atomizer (From Czisch & Fritsching, 2008a, with permission)

During operation of the free-fall atomizer, the gas mass flow rates of both gas nozzle systems are controlled by the primary and secondary gas pressures respectively (pressure levels are given as of overpressure) (Czisch & Fritsching, 2004). Problems may occur during atomizer operation if the pressure ratio between the primary and the secondary nozzle is improperly adjusted and an intense recirculation flow is generated. The applicable maximum gas pressure of the primary gas nozzle is limited by initial disturbances that may be generated on the liquid jet before reaching the atomization area. Therefore, the secondary gas pressure is limited also because the secondary gas mass flow rate determines the necessary primary gas mass flow rate for prevention of recirculation. This coupling of the two nozzle systems limits the applicability of the free-fall atomizer (Fritsching, 2004; Heck et al., 2000; Bergmann et al., 2001).

To improve the operating conditions of the free-fall atomizer it is intended to increase the gas pressures while the recirculation flow is still suppressed. In this case the recirculation gas flow underneath the secondary gas nozzle must be prevented in a different way. It is proposed here that a cylindrical ring device installed into the gas flow of the secondary gas nozzle can improve the atomization performance. The applied device utilizes the Coanda effect (Wille & Fernholz, 1965) and the injector principle to influence the local atomization gas direction. Within the confined flow device (called here the Coanda-ring) an underpressure zone is generated which deflects the gas flow downwards and increases the pressure difference between the inner zone and the ambient gas pressure. This downward reflection of the gas stream effectively increases the gas entrainment from outside the main flow and therefore increases the total gas mass flow rate. This effect increase becomes important because the liquid jet interaction within the secondary nozzle is increased and the recirculation gas flow is suppressed.

#### **3.1 Numerical simulation of free-fall atomizer gas flow**

The improvement of the atomizer design and operating conditions is based on numerical investigations of the gas flow field of a conventional free-fall atomizer (primary and secondary gas nozzle; see figure 2). Nitrogen is used througout this study as atomizer gas. By applying a axisymmetric two-dimensional flow simulation it is assumed that the gas exit

Hybrid Gas Atomization for Powder Production 105

0.000 MPa 0.009 Mpa 0.025 MPa 0.100 MPa

0 50 100 150 200 distance x [mm] .

Fig. 4. Axial gas velocity on the center line at varying primary gas pressures (secondary gas

In Figure 5 the flow field of the free-fall atomizer without primary gas application is illustrated as streamline distribution (left) and local static pressure distribution (right) at a secondary pressure of 0.5 MPa. A recirculation flow field generated underneath the secondary gas nozzle is visible. The area with highest pressure is located where the atomization gas streams impinge onto the center line. The local static pressure exceeds 50

Fig. 5. Flow field (left) and pressure distribution (right) of a conventional free-fall atomizer generated only by the secondary gas flow (scale indicates pressure level in Pa) (From Czisch

Figure 6 shows the flow situation of a free-fall atomizer without primary gas application but with the installed Coanda-flow ring device at a secondary gas pressure of 0.5 MPa. On the left the flow field is illustrated by its streamline distribution and on the right the static pressure distribution is displayed. No recirculation flow field is generated in this case. On the right it can be seen that at the entrance of the installed Coanda-flow device an underpressure area is generated. Depending on the negative pressure ratio, between the underpressure area close to the atomization zone and the environmental gas pressure, the

secondary gas influence

pressure 0.5 MPa) (From Czisch & Fritsching, 2008a, with permission)


& Fritsching, 2008a, with permission)

kPa in this area.

axial gas velocity [m/s] .

primary gas influence

configuration is that of a circular slit nozzle (Lohner, 2002; Lohner et al., 2005). Compressibility (assuming ideal gas flow) as well as turbulence effects (using the conventional k-eps turbulence model) are taken into account. The gas condition at the nozzle exit is assumed as perfectly expanded (supersonic). Pressure levels are given as overpressure (pressure level exceeding the ambient pressure). The orifice areas of primary and secondary gas are kept constant. Therefore, the gas mass flow rates of the primary and the secondary gas nozzle are varied by changing the stagnation gas pressures for primary and secondary gas, respectively.

In Figure 3 the influence of the primary gas pressure, at constant secondary gas pressure (0.5 MPa), is shown in terms of gas streamlines. Two different operating conditions are to be distinguished, separated by the center line in the figure. On the left of the figure the gas flow field is illustrated with primary and secondary gas flow. One can see a reasonable recirculation flow only close to the primary gas orifice. Entrained gas fom the outside as well as the primary gas stream is flowing with the liquid through the passage of the secondary gas nozzle. No recirculation gas flow underneath the secondary gas nozzle is present. On the right of the figure the gas flow field is illustrated when only the secondary gas (atomization gas) is applied but no primary gas. The shown streamlines illustrate an intensive recirculation flow area located from underneath the secondary gas nozzle up to the primary gas nozzle. Thus, at constant secondary gas pressure the intensity of the gas recirculation underneath the secondary gas nozzle decreases with increasing primary gas pressure. But the intensity of the recirculation gas flow close to the primary gas nozzle increases with increasing primary gas pressure.

Fig. 3. Flow field of a conventional free-fall atomizer at different operating conditions (From Czisch & Fritsching, 2008a, with permission)

In Figure 4 the axial gas flow velocity on the center line of the atomizer at constant secondary gas pressure (0.5 MPa) is plotted for varying primary gas pressures. For primary gas pressures exceeding 0.025 MPa the recirculation gas flow underneath the secondary gas nozzle is suppressed (no negative velocities in that area). The intensity of the recirculation close to the primary gas nozzle increases with increasing primary gas pressure.

configuration is that of a circular slit nozzle (Lohner, 2002; Lohner et al., 2005). Compressibility (assuming ideal gas flow) as well as turbulence effects (using the conventional k-eps turbulence model) are taken into account. The gas condition at the nozzle exit is assumed as perfectly expanded (supersonic). Pressure levels are given as overpressure (pressure level exceeding the ambient pressure). The orifice areas of primary and secondary gas are kept constant. Therefore, the gas mass flow rates of the primary and the secondary gas nozzle are varied by changing the stagnation gas pressures for primary

In Figure 3 the influence of the primary gas pressure, at constant secondary gas pressure (0.5 MPa), is shown in terms of gas streamlines. Two different operating conditions are to be distinguished, separated by the center line in the figure. On the left of the figure the gas flow field is illustrated with primary and secondary gas flow. One can see a reasonable recirculation flow only close to the primary gas orifice. Entrained gas fom the outside as well as the primary gas stream is flowing with the liquid through the passage of the secondary gas nozzle. No recirculation gas flow underneath the secondary gas nozzle is present. On the right of the figure the gas flow field is illustrated when only the secondary gas (atomization gas) is applied but no primary gas. The shown streamlines illustrate an intensive recirculation flow area located from underneath the secondary gas nozzle up to the primary gas nozzle. Thus, at constant secondary gas pressure the intensity of the gas recirculation underneath the secondary gas nozzle decreases with increasing primary gas pressure. But the intensity of the recirculation gas flow close to the primary gas nozzle

Fig. 3. Flow field of a conventional free-fall atomizer at different operating conditions (From

In Figure 4 the axial gas flow velocity on the center line of the atomizer at constant secondary gas pressure (0.5 MPa) is plotted for varying primary gas pressures. For primary gas pressures exceeding 0.025 MPa the recirculation gas flow underneath the secondary gas nozzle is suppressed (no negative velocities in that area). The intensity of the recirculation

close to the primary gas nozzle increases with increasing primary gas pressure.

pprimary = 0 MPa psecondary = 0.5 MPa

and secondary gas, respectively.

increases with increasing primary gas pressure.

pprimary = 0.025 MPa psecondary = 0.5 MPa

Czisch & Fritsching, 2008a, with permission)

Fig. 4. Axial gas velocity on the center line at varying primary gas pressures (secondary gas pressure 0.5 MPa) (From Czisch & Fritsching, 2008a, with permission)

In Figure 5 the flow field of the free-fall atomizer without primary gas application is illustrated as streamline distribution (left) and local static pressure distribution (right) at a secondary pressure of 0.5 MPa. A recirculation flow field generated underneath the secondary gas nozzle is visible. The area with highest pressure is located where the atomization gas streams impinge onto the center line. The local static pressure exceeds 50 kPa in this area.

Fig. 5. Flow field (left) and pressure distribution (right) of a conventional free-fall atomizer generated only by the secondary gas flow (scale indicates pressure level in Pa) (From Czisch & Fritsching, 2008a, with permission)

Figure 6 shows the flow situation of a free-fall atomizer without primary gas application but with the installed Coanda-flow ring device at a secondary gas pressure of 0.5 MPa. On the left the flow field is illustrated by its streamline distribution and on the right the static pressure distribution is displayed. No recirculation flow field is generated in this case. On the right it can be seen that at the entrance of the installed Coanda-flow device an underpressure area is generated. Depending on the negative pressure ratio, between the underpressure area close to the atomization zone and the environmental gas pressure, the

Hybrid Gas Atomization for Powder Production 107

0 50 100 150 200 250 distance x [mm] .

Fig. 7. Axial gas velocity on the center line at varying secondary gas pressures with installed

Coanda-flow device (no primary gas nozzle) (From Czisch & Fritsching, 2008a, with

Fig. 8. Model experiments without (left) and with Coanda-flow device (right) (psec = 0.5 MPa, no primary gas, liquid mass flow rate 435 kg/h) (From Czisch & Fritsching, 2008a,

The derived Coanda-flow device is adapted within a free-fall atomizer for powder generation from viscous mineral melts. In this application, hot atomization gas is used to suppress fibre formation during viscous melt atomization and to produce spherical particles. Results for achieved particle size spectra have been reported in (Lohner, 2002; Lohner et al., 2005). In Figure 9 the particle size distributions of two different atomization runs are compared at similar operating conditions but with and without the installation of the Coanda-flow device. A mineral melt (liquid melt, no solid particles included) is atomized at a liquid mass flow rate of 300 kg/h. The liquid temperature is app. 1873 K and the gas temperature about 1273 K. The viscosity of the melt at the atomization temperature is 0.2 Pas. The secondary gas pressure used in these cases is similar (0.55 MPa and 0.58 MPa respectively). In the case without the flow device, a primary gas flow is applied at a pressure of 0.18 MPa. This relatively high primary gas pressure allows the suppression of major gas recirculation, but the appearance of the spray structure indicated that some instabilities

0.5 MPa 0.7 MPa 0.9 MPa


permission)

with permission)

axial gas velocity [m/s] .

primary gas influence

secondary gas influence

gas flow is deflected downwards. Thus the mass flow rate increases though the liquid passage of the secondary nozzle suppressing the recirculation completely. The maximum underpressure within the Coanda-flow device exceeds –60 kPa for the given secondary gas pressure.

Fig. 6. Flow field (left) and pressure distribution (right) of a free-fall atomizer generated only by the secondary gas flow but with installed Coanda-flow device (scale indicates pressure level in Pa) (From Czisch & Fritsching, 2008a, with permission)

The axial velocity on the center line of the atomizer is plotted in Figure 7 versus the varying secondary gas pressure with usage of the Coanda-flow device. In this investigation no primary gas nozzle is used at all. There is almost no effect on the axial gas velocity with increasing gas pressure until the gas passed the installed flow device. Up to this point the flow is completely dominated by the entrained gas flow from outside. After the gas passed the Coanda-flow device, the axial gas velocity increases with increasing secondary gas pressure. Thus it is possible to achieve a recirculation free flow without applying any primary gas by using the Coanda-flow device.

#### **3.2 Atomization experiments**

Model atomization experiments are used to verify the outlined improvements of the operation of the free-fall atomizer with the installed Coanda-flow device. The main aim in this part of the investigation is the proper adjustment of the gas flow rates (or pressures) to ensure stable atomization conditions. Within these model experiments water is atomized by air at room temperature at various pressures (overpressure above the ambient pressure). In Figure 8 (left) a photograph of the atomization area is shown without the Coanda-flow device at 0.5 MPa secondary gas pressure and without primary gas application. Obviously an unstable atomization occurs where droplets are transported from the atomization area upwards towards the atomizer body due to the generated recirculation flow. The instability of the atomization is visible even as three-dimensional structure (asymmetric). When the Coanda-flow device is installed (Figure 8 right) the atomization at 0.5 MPa secondary gas pressure and without primary gas becomes stable, i.e., no major recirculation in the atomization area occurs at all.

gas flow is deflected downwards. Thus the mass flow rate increases though the liquid passage of the secondary nozzle suppressing the recirculation completely. The maximum underpressure within the Coanda-flow device exceeds –60 kPa for the given secondary gas

Fig. 6. Flow field (left) and pressure distribution (right) of a free-fall atomizer generated only by the secondary gas flow but with installed Coanda-flow device (scale indicates pressure

The axial velocity on the center line of the atomizer is plotted in Figure 7 versus the varying secondary gas pressure with usage of the Coanda-flow device. In this investigation no primary gas nozzle is used at all. There is almost no effect on the axial gas velocity with increasing gas pressure until the gas passed the installed flow device. Up to this point the flow is completely dominated by the entrained gas flow from outside. After the gas passed the Coanda-flow device, the axial gas velocity increases with increasing secondary gas pressure. Thus it is possible to achieve a recirculation free flow without applying any

Model atomization experiments are used to verify the outlined improvements of the operation of the free-fall atomizer with the installed Coanda-flow device. The main aim in this part of the investigation is the proper adjustment of the gas flow rates (or pressures) to ensure stable atomization conditions. Within these model experiments water is atomized by air at room temperature at various pressures (overpressure above the ambient pressure). In Figure 8 (left) a photograph of the atomization area is shown without the Coanda-flow device at 0.5 MPa secondary gas pressure and without primary gas application. Obviously an unstable atomization occurs where droplets are transported from the atomization area upwards towards the atomizer body due to the generated recirculation flow. The instability of the atomization is visible even as three-dimensional structure (asymmetric). When the Coanda-flow device is installed (Figure 8 right) the atomization at 0.5 MPa secondary gas pressure and without primary gas becomes stable, i.e., no major recirculation in the

level in Pa) (From Czisch & Fritsching, 2008a, with permission)

primary gas by using the Coanda-flow device.

**3.2 Atomization experiments** 

atomization area occurs at all.

pressure.

Fig. 8. Model experiments without (left) and with Coanda-flow device (right) (psec = 0.5 MPa, no primary gas, liquid mass flow rate 435 kg/h) (From Czisch & Fritsching, 2008a, with permission)

The derived Coanda-flow device is adapted within a free-fall atomizer for powder generation from viscous mineral melts. In this application, hot atomization gas is used to suppress fibre formation during viscous melt atomization and to produce spherical particles. Results for achieved particle size spectra have been reported in (Lohner, 2002; Lohner et al., 2005). In Figure 9 the particle size distributions of two different atomization runs are compared at similar operating conditions but with and without the installation of the Coanda-flow device. A mineral melt (liquid melt, no solid particles included) is atomized at a liquid mass flow rate of 300 kg/h. The liquid temperature is app. 1873 K and the gas temperature about 1273 K. The viscosity of the melt at the atomization temperature is 0.2 Pas. The secondary gas pressure used in these cases is similar (0.55 MPa and 0.58 MPa respectively). In the case without the flow device, a primary gas flow is applied at a pressure of 0.18 MPa. This relatively high primary gas pressure allows the suppression of major gas recirculation, but the appearance of the spray structure indicated that some instabilities

Hybrid Gas Atomization for Powder Production 109

2003). Certain limits of these existing technologies are to be seen when realizing an appropriate (low) particle size or a low fibre-to-particle ratio at high melt-mass flow rates.

To increase the efficiency and to decrease the resulting particle size of an atomization process, one can increase the specific surface energy before atomization (Lefebvre, 1980). With respect to twin fluid (gas) atomization, the fragmentation must take place in a region where the velocity difference between the atomization gas and the melt is highest. Thus the melt must be transformed and transported into an area where the maximum velocity difference occurs. To increase the specific surface energy before atomization, a rotating device such as a disc can be used, obtaining high efficiency for transformation. To prevent liquid accumulation effects at the rim of the disc and to decrease the film thickness, the rotary device must operate in sheet-formation mode, generating a free-flowing liquid film from the edge of the disc. The generated film is atomized subsequently by a high-speed gas flow emerging from an external mixing gas atomizer. This configuration allows the generation of a high velocity difference between the atomization gas and the melt film. To prevent fibre formation, the atomization gas needs to be heated. The formation of the freeflowing film is influenced by the local gas flow field. The generated gas flow field can be used to support the transport of the free-flowing film into the most efficient atomization zone. Thus the gas flow field has to be determined by an appropriate atomizer design. An

atomizer concept based on the discussed aspects is the prefilming hybrid atomizer.

The aim of the development is an atomizer design for highly viscous liquids and melts at high throughputs that produce a considerably low droplet size. The prefilming hybrid atomizer introduced here is a combination of a single-fluid rotary atomizer and an external mixing twin-fluid atomizer. The advantage of this specific design is that the feed material is first spread out by a spinning disc due to centrifugal forces, thereby increasing the initial liquid surface prior to the gas atomization process. The rotary atomizer is operated in sheet formation mode so that in the vicinity of the rotary disc a free prefilm is formed. This prefilm is subsequently guided into the atomization zone of the external mixing atomizer by means of intrinsic aerodynamic forces in the gas flow field. In Fig. 10 the principle of the prefilming hybrid atomizer is illustrated. To ensure stable atomization, aerodynamic forces are used to protect the atomizer body from coming into contact and being blocked by parts of the liquid (melt). A sufficiently small gas mass flow rate from the inside of the atomizer

The flow field of gas and liquid of the prefilming hybrid atomizer is illustrated in Fig. 11. Different local flow regimes need to be distinguished. The inner entrainment reaches the atomization area through the atomizer liquid stream passage. The outer entrainment reaches the atomization area directly, and the recirculation gas flow reaches the atomization area from below the rotary disc. All flow regimes are initialized be the atomization gas. The film movement mainly depends on the acting aerodynamic and inertial forces caused by the momentum distribution of the inner entrainment flow, the recirculation gas flow momentum, and the film momentum itself. The aim of the prefilming hybrid atomizer design is to generate a maximum recirculation momentum where the liquid film is

**4.1 The prefilming atomizer concept** 

protects the atomizer body.

transported close to the gas outlet.

from the primary gas flow seem to occur. A rather broad particle size distribution results with an indication of a bimodal distribution shape resulting from atomization presumably due to the primary and the secondary gas flows. With the installed Coanda-flow device, a very stable atomizer operation was observed. The resulting mass median droplet diameter (MMD) is app. 280 µm for the conventional free-fall atomizer and app. 140 µm for the freefall atomizer with the installed flow device. Therefore, the droplet diameter was halved when compared to the conventional free-fall atomizer results.

Fig. 9. Particle size distribution with and without applied Coanda-flow device for mineral melt atomization (without Coanda-flow device: psec = 0.55 MPa, pprim = 0.18 MPa; with Coanda-flow device: psec = 0.58 MPa, no primary gas; liquid mass flow rate 300 kg/h, liquid viscosity 0.2 Pas, gas temperature 1273 K, melt temperature 1873 K) (From Czisch & Fritsching, 2008a, with permission)

#### **4. Hybrid atomization: Rotary film formation plus gas jet desintegration**

Viscous melts, for example glass melts or liquid slags, have a comparably high viscosity and low surface tension. Powder production by gas atomization of such viscous melts is a difficult task because of the rapid cooling of the generated ligaments during melt fragmentation that may cause fibre formation instead of a particulate product. In addition, the increasing temperature of the melt within the process increases the melt viscosity that on the other side decreases the dynamic energy transfer rate between gas and liquid. Therefore, the disintegration time-scale increases and the liquid fragments may be transported out of the area where the most effective atomization occurs. Depending on this decreasing energytransfer rate, the resulting particle size increases and the efficiency of the atomization process decreases.

By using external mixing gas atomizers with heated atomization gases, in principle a particle product can be obtained (Lohner, 2002; Lohner et al., 2005; Czisch et al., 2003). The efficiency of the atomization process decreases with increasing viscosity and the minimum particle size is limited by the available energy input (Yule & Dunkley, 1994; Strauss, 1999; Dunkley, 2001). Concepts for atomization of highly viscous liquids or melts have already been developed (Pickering et al, 1985; Fraser & Dombrowski, 1962; Campanile & Azzopardi,

from the primary gas flow seem to occur. A rather broad particle size distribution results with an indication of a bimodal distribution shape resulting from atomization presumably due to the primary and the secondary gas flows. With the installed Coanda-flow device, a very stable atomizer operation was observed. The resulting mass median droplet diameter (MMD) is app. 280 µm for the conventional free-fall atomizer and app. 140 µm for the freefall atomizer with the installed flow device. Therefore, the droplet diameter was halved

> 0 100 200 300 400 500 600 700 particle size [µm]

Fig. 9. Particle size distribution with and without applied Coanda-flow device for mineral melt atomization (without Coanda-flow device: psec = 0.55 MPa, pprim = 0.18 MPa; with Coanda-flow device: psec = 0.58 MPa, no primary gas; liquid mass flow rate 300 kg/h, liquid

viscosity 0.2 Pas, gas temperature 1273 K, melt temperature 1873 K) (From Czisch &

**4. Hybrid atomization: Rotary film formation plus gas jet desintegration** 

Viscous melts, for example glass melts or liquid slags, have a comparably high viscosity and low surface tension. Powder production by gas atomization of such viscous melts is a difficult task because of the rapid cooling of the generated ligaments during melt fragmentation that may cause fibre formation instead of a particulate product. In addition, the increasing temperature of the melt within the process increases the melt viscosity that on the other side decreases the dynamic energy transfer rate between gas and liquid. Therefore, the disintegration time-scale increases and the liquid fragments may be transported out of the area where the most effective atomization occurs. Depending on this decreasing energytransfer rate, the resulting particle size increases and the efficiency of the atomization

By using external mixing gas atomizers with heated atomization gases, in principle a particle product can be obtained (Lohner, 2002; Lohner et al., 2005; Czisch et al., 2003). The efficiency of the atomization process decreases with increasing viscosity and the minimum particle size is limited by the available energy input (Yule & Dunkley, 1994; Strauss, 1999; Dunkley, 2001). Concepts for atomization of highly viscous liquids or melts have already been developed (Pickering et al, 1985; Fraser & Dombrowski, 1962; Campanile & Azzopardi,

conv. free-fall atomizer

free-fall atomizer with flow device

when compared to the conventional free-fall atomizer results.

Fritsching, 2008a, with permission)

process decreases.

Cumulative [%]

2003). Certain limits of these existing technologies are to be seen when realizing an appropriate (low) particle size or a low fibre-to-particle ratio at high melt-mass flow rates.

To increase the efficiency and to decrease the resulting particle size of an atomization process, one can increase the specific surface energy before atomization (Lefebvre, 1980). With respect to twin fluid (gas) atomization, the fragmentation must take place in a region where the velocity difference between the atomization gas and the melt is highest. Thus the melt must be transformed and transported into an area where the maximum velocity difference occurs. To increase the specific surface energy before atomization, a rotating device such as a disc can be used, obtaining high efficiency for transformation. To prevent liquid accumulation effects at the rim of the disc and to decrease the film thickness, the rotary device must operate in sheet-formation mode, generating a free-flowing liquid film from the edge of the disc. The generated film is atomized subsequently by a high-speed gas flow emerging from an external mixing gas atomizer. This configuration allows the generation of a high velocity difference between the atomization gas and the melt film. To prevent fibre formation, the atomization gas needs to be heated. The formation of the freeflowing film is influenced by the local gas flow field. The generated gas flow field can be used to support the transport of the free-flowing film into the most efficient atomization zone. Thus the gas flow field has to be determined by an appropriate atomizer design. An atomizer concept based on the discussed aspects is the prefilming hybrid atomizer.

#### **4.1 The prefilming atomizer concept**

The aim of the development is an atomizer design for highly viscous liquids and melts at high throughputs that produce a considerably low droplet size. The prefilming hybrid atomizer introduced here is a combination of a single-fluid rotary atomizer and an external mixing twin-fluid atomizer. The advantage of this specific design is that the feed material is first spread out by a spinning disc due to centrifugal forces, thereby increasing the initial liquid surface prior to the gas atomization process. The rotary atomizer is operated in sheet formation mode so that in the vicinity of the rotary disc a free prefilm is formed. This prefilm is subsequently guided into the atomization zone of the external mixing atomizer by means of intrinsic aerodynamic forces in the gas flow field. In Fig. 10 the principle of the prefilming hybrid atomizer is illustrated. To ensure stable atomization, aerodynamic forces are used to protect the atomizer body from coming into contact and being blocked by parts of the liquid (melt). A sufficiently small gas mass flow rate from the inside of the atomizer protects the atomizer body.

The flow field of gas and liquid of the prefilming hybrid atomizer is illustrated in Fig. 11. Different local flow regimes need to be distinguished. The inner entrainment reaches the atomization area through the atomizer liquid stream passage. The outer entrainment reaches the atomization area directly, and the recirculation gas flow reaches the atomization area from below the rotary disc. All flow regimes are initialized be the atomization gas. The film movement mainly depends on the acting aerodynamic and inertial forces caused by the momentum distribution of the inner entrainment flow, the recirculation gas flow momentum, and the film momentum itself. The aim of the prefilming hybrid atomizer design is to generate a maximum recirculation momentum where the liquid film is transported close to the gas outlet.

Hybrid Gas Atomization for Powder Production 111

0 20 40 60 **atomization gas angle [0**

D = 124mm

drota120m

Fig. 13. The constructive parameters of the hybrid atomizer design (From Czisch &

In the same way as the gas outlet angle, all constructive parameters of the atomizer have been determined separately by variation runs within the simulation. In Figure 13 the resulting optimum parameter set for the prefilming hybrid atomizer is shown. The design is based for the atomization of mineral melts at a temperature of 1873 K where the liquid viscosity is 1 Pas and the melt mass flow rate is aimed at 300 kg/h. A gas jet spacing of 0 has

In Figures 14 and 15 experimental results of atomization of water and glycerol are illustrated. The mass median droplet size in the spray measured by laser diffraction is plotted against the air-to-liquid mass-flow ratio (ALR). The efficiency of the hybrid atomizer is evaluated in comparison with a conventional free-fall atomizer (Lohner et al, 2003). The free-fall atomizer is a common device for powder production (Bauckhage & Fritsching, 2000) and spray forming applications (Fritsching and Bauckhage, 2006). When low viscous

r

been chosen, therefore a slit nozzle is used as gas-flow exit geometry.

h =10mm

**]**

tnozzle = 0

<sup>x</sup> <sup>t</sup>

Fig. 12. Axial recirculation momentum on the free flowing film (From Czisch & Fritsching,


**recirculation momentum .** 

2008b, with permission)

**4.3 Model experiments** 

Fritsching, 2008b, with permission)

**[kg m/s]**

x r

analyzed area 0.89bar 1.78bar 2.64bar

*d*

*t <sup>t</sup>*

*nozzle* Spacing

p = 0,89bar p = 1,78bar p = 2,64bar

d

Fig. 10. Sketch of the prefilming hybrid atomizer (From Czisch & Fritsching, 2008b, with permission)

Fig. 11. Gas flowfield and effective momentum transfer of the prefilming hybrid atomizer (From Czisch & Fritsching, 2008b, with permission)

#### **4.2 Numerical simulation**

Numerical simulations are used to derive the suitable atomizer design for efficient viscous melt atomization. The aim of the numerical simulations is to derive conditions where a maximum gas momentum on the free flowing liquid film acts against the main axial atomization gas direction. Because the highest velocity difference between gas and liquid and therefore the most efficient atomization area is close to the atomization-gas outlet, the recirculation momentum must be maximized to transport the liquid film towards the outlet of the atomization gas. Within the gas flow simulations the axial momentum of the recirculation gas flow is analyzed at the location of the free-flowing liquid film. In Figure 12 the recirculation momentum depending on the atomization gas outlet angle is shown. The recirculation momentum starts at gas outlet angles above 15°. For outlet angles less than 15° the inner entrainment momentum dominates the interaction with the film. At outlet angles above 15° the recirculation momentum dominates the interaction and it increases with increasing outlet angle. A reasonable high recirculation momentum is reached at outlet angles between 45° to 50°. The atomization gas outlet angle for the design of the hybrid atomizer has therefore been set to 45°.

viscous liquid external mixing

Fig. 10. Sketch of the prefilming hybrid atomizer (From Czisch & Fritsching, 2008b, with

momentum recirculation

Fig. 11. Gas flowfield and effective momentum transfer of the prefilming hybrid atomizer

Numerical simulations are used to derive the suitable atomizer design for efficient viscous melt atomization. The aim of the numerical simulations is to derive conditions where a maximum gas momentum on the free flowing liquid film acts against the main axial atomization gas direction. Because the highest velocity difference between gas and liquid and therefore the most efficient atomization area is close to the atomization-gas outlet, the recirculation momentum must be maximized to transport the liquid film towards the outlet of the atomization gas. Within the gas flow simulations the axial momentum of the recirculation gas flow is analyzed at the location of the free-flowing liquid film. In Figure 12 the recirculation momentum depending on the atomization gas outlet angle is shown. The recirculation momentum starts at gas outlet angles above 15°. For outlet angles less than 15° the inner entrainment momentum dominates the interaction with the film. At outlet angles above 15° the recirculation momentum dominates the interaction and it increases with increasing outlet angle. A reasonable high recirculation momentum is reached at outlet angles between 45° to 50°. The atomization gas outlet angle for the design of the hybrid

gas

(From Czisch & Fritsching, 2008b, with permission)

**4.2 Numerical simulation** 

atomizer has therefore been set to 45°.

permission)

atomizer

rotary disk

inner entrainment

gas flow

atomization

gas

outer entrainment

Fig. 12. Axial recirculation momentum on the free flowing film (From Czisch & Fritsching, 2008b, with permission)

Fig. 13. The constructive parameters of the hybrid atomizer design (From Czisch & Fritsching, 2008b, with permission)

In the same way as the gas outlet angle, all constructive parameters of the atomizer have been determined separately by variation runs within the simulation. In Figure 13 the resulting optimum parameter set for the prefilming hybrid atomizer is shown. The design is based for the atomization of mineral melts at a temperature of 1873 K where the liquid viscosity is 1 Pas and the melt mass flow rate is aimed at 300 kg/h. A gas jet spacing of 0 has been chosen, therefore a slit nozzle is used as gas-flow exit geometry.

#### **4.3 Model experiments**

In Figures 14 and 15 experimental results of atomization of water and glycerol are illustrated. The mass median droplet size in the spray measured by laser diffraction is plotted against the air-to-liquid mass-flow ratio (ALR). The efficiency of the hybrid atomizer is evaluated in comparison with a conventional free-fall atomizer (Lohner et al, 2003). The free-fall atomizer is a common device for powder production (Bauckhage & Fritsching, 2000) and spray forming applications (Fritsching and Bauckhage, 2006). When low viscous

Hybrid Gas Atomization for Powder Production 113

(relative overpressure against ambient pressure) have been realized within hybrid atomization runs. Hot gas is produced by means of a discontinuous heat exchanger (cowper). The ceramic bulk material inside the cowper is heated by a propane burner. After this heating process, compressed gas or steam is blown through the cowper. The preset values of atomization gas temperature and gas pressure are obtained by mixing the heated gas from the cowper with gas at room temperature. The resulting melt droplets in the spray may be quenched and solidified about 2 m below the atomization nozzle. The solidified powder is collected at the bottom of

Fig. 16 shows a Scanning-Electron-Micrograph of the sprayed powder from the mineral melt atomization experiment using the hybrid atomization system. A particle fraction of the as sprayed material in the size range from 110 to 350 µm is shown. Mostly spherical particles are to be seen, the fraction of particles to the fraction of fibers in total is above 90 %. In Fig. 16 (right) particles size results for the atomization of this mineral slag melt at different atomization gas temperatures and gas pressures (relative) are shown. The mass-median particle size of the resulting powder is plotted versus the atomization gas temperature. The

the spray tower, the fine powder fraction is deposited in the cyclone.

gas temperature given in the graph is after expansion (a.e.).

& Fritsching, 2008b, with permission)

**5. Pressure-gas-atomization** 

Fig. 16. Micrograph of hot-gas atomized mineral melt particles (size fraction 110 – 350 µm) and results for atomizing mineral melt at an angular disc speed of 1500/min (From Czisch

The maximum gas temperature before expansion is 1273 K. With increasing gas temperature and increasing atomization gas pressure the particle size decreases. For this set of experimental conditions, the achieved minimum mass median particle size is 210 µm. Compared with the model experiments and the material properties of glycerol the minimum particle size is rather coarse. This results from the limited maximum atomization gas temperature available in the facility. The achieved temperature is still too low in comparison with the melt temperature. Before and within the disintegration process, the melt is cooled

Pressure-gas-atomization is another disintegration process which can be subdivided in two steps: a pre-filming and a gas atomization step. During the pre-filming step, a large molten

down rapidly, so the viscosity increases and the disintegration efficiency is limited.

**mass median particle size .**

**d50,3 [µm]**


**C]**

p0 = 0.42bar p0 = 0.77bar p0 = 1.00bar p0 = 1.55bar p0 = 1.98bar

liquid as e.g. water is atomized, the efficiency of the hybrid atomizer is low. For a constant liquid-mass flow rate, at identical ALR the hybrid atomizer produces coarser particle sizes. In this case the increase of the specific surface energy before atomization is not an advantage. It becomes advantageous only when the viscosity increases. Fig. 15 shows that at constant ALR, the hybrid atomizer produces finer particles than a conventional atomizer for viscous glycerol atomization. In this case, a mass-median particle size of less than 30 µm is achieved.

Fig. 14. Experimental results for atomizing water by air (From Czisch & Fritsching, 2008b, with permission)

Fig. 15. Experimental results for atomizing glycerol by air (From Czisch & Fritsching, 2008b, with permission)

#### **4.4 Melt atomization experiments**

For atomizing viscous melts by the hybrid atomizer concept, a pilot plant for hot-gas atomization has been used (Lohner at al., 2005). The main part of the plant is a spray tower (about 5.5 m in height). On top of the spray tower, the material is melted by an induction heating device. As material to be atomized, a blast-furnace slag is used for the trials. The melt temperature before atomization is measured as 1813-1843 K with a mean temperature of 1826 K. Through the bottom pouring crucible, the melt flows out due to gravity at meltmass flow rates up to 300 kg/h. The hybrid atomizer located underneath the crucible is operated using heated gas. Gas temperatures up to 1273 K and gas pressures up to 2 bar

liquid as e.g. water is atomized, the efficiency of the hybrid atomizer is low. For a constant liquid-mass flow rate, at identical ALR the hybrid atomizer produces coarser particle sizes. In this case the increase of the specific surface energy before atomization is not an advantage. It becomes advantageous only when the viscosity increases. Fig. 15 shows that at constant ALR, the hybrid atomizer produces finer particles than a conventional atomizer for viscous glycerol atomization. In this case, a mass-median particle size of less than 30 µm is

> conv. 400kg/h conv. 700kg/h conv. 1000kg/h hyb. 400kg/h hyb. 700kg/h hyb. 1000kg/h

conv. 395kg/h conv. 710kg/h conv. 1001kg/h hyb. 414kg/h hyb. 696kg/h hyb. 1007kg/h

0 0,5 1 1,5 2 2,5 **ALR [-] .**

Fig. 14. Experimental results for atomizing water by air (From Czisch & Fritsching, 2008b,

0 0,5 1 1,5 2 2,5 **ALR [-] .**

Fig. 15. Experimental results for atomizing glycerol by air (From Czisch & Fritsching, 2008b,

For atomizing viscous melts by the hybrid atomizer concept, a pilot plant for hot-gas atomization has been used (Lohner at al., 2005). The main part of the plant is a spray tower (about 5.5 m in height). On top of the spray tower, the material is melted by an induction heating device. As material to be atomized, a blast-furnace slag is used for the trials. The melt temperature before atomization is measured as 1813-1843 K with a mean temperature of 1826 K. Through the bottom pouring crucible, the melt flows out due to gravity at meltmass flow rates up to 300 kg/h. The hybrid atomizer located underneath the crucible is operated using heated gas. Gas temperatures up to 1273 K and gas pressures up to 2 bar

achieved.

with permission)

with permission)

**mass median particle size .** 

**4.4 Melt atomization experiments** 

**d 50,3 [µm] .**

**mass median particle size .** 

**d 50,3 [µm] .**

(relative overpressure against ambient pressure) have been realized within hybrid atomization runs. Hot gas is produced by means of a discontinuous heat exchanger (cowper). The ceramic bulk material inside the cowper is heated by a propane burner. After this heating process, compressed gas or steam is blown through the cowper. The preset values of atomization gas temperature and gas pressure are obtained by mixing the heated gas from the cowper with gas at room temperature. The resulting melt droplets in the spray may be quenched and solidified about 2 m below the atomization nozzle. The solidified powder is collected at the bottom of the spray tower, the fine powder fraction is deposited in the cyclone.

Fig. 16 shows a Scanning-Electron-Micrograph of the sprayed powder from the mineral melt atomization experiment using the hybrid atomization system. A particle fraction of the as sprayed material in the size range from 110 to 350 µm is shown. Mostly spherical particles are to be seen, the fraction of particles to the fraction of fibers in total is above 90 %. In Fig. 16 (right) particles size results for the atomization of this mineral slag melt at different atomization gas temperatures and gas pressures (relative) are shown. The mass-median particle size of the resulting powder is plotted versus the atomization gas temperature. The gas temperature given in the graph is after expansion (a.e.).

Fig. 16. Micrograph of hot-gas atomized mineral melt particles (size fraction 110 – 350 µm) and results for atomizing mineral melt at an angular disc speed of 1500/min (From Czisch & Fritsching, 2008b, with permission)

The maximum gas temperature before expansion is 1273 K. With increasing gas temperature and increasing atomization gas pressure the particle size decreases. For this set of experimental conditions, the achieved minimum mass median particle size is 210 µm. Compared with the model experiments and the material properties of glycerol the minimum particle size is rather coarse. This results from the limited maximum atomization gas temperature available in the facility. The achieved temperature is still too low in comparison with the melt temperature. Before and within the disintegration process, the melt is cooled down rapidly, so the viscosity increases and the disintegration efficiency is limited.

#### **5. Pressure-gas-atomization**

Pressure-gas-atomization is another disintegration process which can be subdivided in two steps: a pre-filming and a gas atomization step. During the pre-filming step, a large molten

Hybrid Gas Atomization for Powder Production 115

Achelis et al., 2006, 2008, 2009). The hollow cone film/spray is surrounded by the gas-ringatomizer. Due to the high velocity gas flow from the gas-ring-atomizer, the hollow cone spray from the pre-filming process is atomized into small droplets. Simultaneously, the

Fig. 18. Schematic (left) and pressure-gas-atomization of pure tin (right), (Achelis et al.,

Higher pressure yields in a large cone angle as demonstrated in the figure as well.

A pressure difference of about 0.4 MPa is necessary to achieve a fully developed hollow cone if pure tin is used. Fig. 19 shows the effect of the pressure on the cone angle. A fully developed cone is already achieved with a pressure of 0.45 MPa but the cone angle Θ is still small (29°).

Fig. 19. Effect of the pressure pL on the spray cone angle Θ during pressure-atomization of

A high speed video camera was used to investigate the break-up of the liquid metal film. The pictures in fig. 20 represent single images of different alloys. The image section shows the area below the gas-ring-atomizer (not in use). The tin film is hidden by the gas-ringatomizer and only the ligaments of the oscillating film are seen below the gas ring nozzle.

2006a).

**5.2 Pre-filming** 

pure tin (Achelis, 2009).

particles are mainly directed to the centreline of the atomizer axis (Fig. 18).

metal surface is generated to prepare an efficient second disintegration step by gas atomization. In the following, the development, the principle, and the results of the pressure-gas-atomization are described.

#### **5.1 Principle**

Pressure-gas-atomization became possible after the development of the pressure atomizer. The idea of a pressure atomizer for molten metal was born in the 90`s by Sheikhaliev and later published by Dunkley and Sheikhaliev (Dunkley & Sheikhaliev, 1995). Originally, the authors called this atomization technique "Centrifugal Hydraulic Atomization". Here, the metal was melted in a crucible placed in a pressure vessel and the molten metal was tangentially fed into a small swirl chamber where the molten metal starts to rotate. Typically, on the centreline of the swirl chamber a gas core develops due to centrifugal forces. Finally, at the lower end of the conical part of the swirl chamber a hole with a diameter between 1 and 2 mm allows the melt to leave the swirl chamber as a thin film creating a hollow cone inside the spray chamber (fig. 17). Normally, a pressure difference of 0.4 to 1.0 MPa between the pressure vessel and the spray chamber is sufficient to achieve a hollow cone of a molten metal. Commonly, this principle is used for cold liquids as an effective atomization system. For a long time, it was doubted if this principle can be applied to molten metal because of their much higher surface tension and the nozzle heating was another challenge. Finally, the molten melt film becomes instable and disintegrates to ligaments and relatively large droplets (mass median diameter far above 100 µm).

Fig. 17. Schematic (above) and picture (below) of pressure atomization using pure tin (Achelis, 2009).

The pressure-gas-atomization was developed to achieve smaller particles and a narrow size distribution. It combines the pressure atomization as a pre-filming step and the gas atomization. As the second step a gas-ring-atomizer is used to disintegrate the molten metal film, ligaments, and any large droplets. This idea results in a patent published in 2002 (Uhlenwinkel, 2002) and initiated intensive investigations (Lagutkin et al., 2003b, 2004b; Achelis et al., 2006, 2008, 2009). The hollow cone film/spray is surrounded by the gas-ringatomizer. Due to the high velocity gas flow from the gas-ring-atomizer, the hollow cone spray from the pre-filming process is atomized into small droplets. Simultaneously, the particles are mainly directed to the centreline of the atomizer axis (Fig. 18).

Fig. 18. Schematic (left) and pressure-gas-atomization of pure tin (right), (Achelis et al., 2006a).

#### **5.2 Pre-filming**

114 Powder Metallurgy

metal surface is generated to prepare an efficient second disintegration step by gas atomization. In the following, the development, the principle, and the results of the

Pressure-gas-atomization became possible after the development of the pressure atomizer. The idea of a pressure atomizer for molten metal was born in the 90`s by Sheikhaliev and later published by Dunkley and Sheikhaliev (Dunkley & Sheikhaliev, 1995). Originally, the authors called this atomization technique "Centrifugal Hydraulic Atomization". Here, the metal was melted in a crucible placed in a pressure vessel and the molten metal was tangentially fed into a small swirl chamber where the molten metal starts to rotate. Typically, on the centreline of the swirl chamber a gas core develops due to centrifugal forces. Finally, at the lower end of the conical part of the swirl chamber a hole with a diameter between 1 and 2 mm allows the melt to leave the swirl chamber as a thin film creating a hollow cone inside the spray chamber (fig. 17). Normally, a pressure difference of 0.4 to 1.0 MPa between the pressure vessel and the spray chamber is sufficient to achieve a hollow cone of a molten metal. Commonly, this principle is used for cold liquids as an effective atomization system. For a long time, it was doubted if this principle can be applied to molten metal because of their much higher surface tension and the nozzle heating was another challenge. Finally, the molten melt film becomes instable and disintegrates to

ligaments and relatively large droplets (mass median diameter far above 100 µm).

Fig. 17. Schematic (above) and picture (below) of pressure atomization using pure tin

The pressure-gas-atomization was developed to achieve smaller particles and a narrow size distribution. It combines the pressure atomization as a pre-filming step and the gas atomization. As the second step a gas-ring-atomizer is used to disintegrate the molten metal film, ligaments, and any large droplets. This idea results in a patent published in 2002 (Uhlenwinkel, 2002) and initiated intensive investigations (Lagutkin et al., 2003b, 2004b;

10mm

pressure-gas-atomization are described.

**5.1 Principle** 

(Achelis, 2009).

A pressure difference of about 0.4 MPa is necessary to achieve a fully developed hollow cone if pure tin is used. Fig. 19 shows the effect of the pressure on the cone angle. A fully developed cone is already achieved with a pressure of 0.45 MPa but the cone angle Θ is still small (29°). Higher pressure yields in a large cone angle as demonstrated in the figure as well.

Fig. 19. Effect of the pressure pL on the spray cone angle Θ during pressure-atomization of pure tin (Achelis, 2009).

A high speed video camera was used to investigate the break-up of the liquid metal film. The pictures in fig. 20 represent single images of different alloys. The image section shows the area below the gas-ring-atomizer (not in use). The tin film is hidden by the gas-ringatomizer and only the ligaments of the oscillating film are seen below the gas ring nozzle.

Hybrid Gas Atomization for Powder Production 117

**Distance from the gas nozzle z [mm]**

+15 0 -15 0 (ring slit)

Fig. 22. Influence of different atomizer designs on the spray cone of a pressure-gas-atomizer. The central plane of the spray cone is illuminated by a laser light sheet and water is used as

The production rate is an important feature for an atomization processes. Typically the mass flow of the pressure gas atomization can be varied between 70 and 200 kg/h using tin and tin-copper alloys. As expected, the melt flow rate can be adjusted by the pressure difference between the pressure vessel and the spray chamber. The gas pressure in the gas-ring-

Central plane of the spray cone illuminated by a laser light sheet

Fig. 21. Pressure on the surface of a tube placed on the centreline of the gas-ring-atomizer indicates the gas flow field in the vicinity of the atomizer. The effect of different atomizer

**Pressure difference**

designs is shown (Lagutkin et al., 2003a/b).

β

10mm

a liquid (Uhlenwinkel et al., 2003).

atomizer does not influence the melt flow.

**5.4 Melt flow rate** 

z

Gas nozzle exit angle β in °

Pressure gas atomization, fluid: water Bright area = high amount of particles

**Δp [kPa]**

nozzle exit angle +15°, exit area 18.5mm² nozzle exit angle 0°, exit area 18.5mm² nozzle exit angle -15°, exit area 18.5mm² Ring nozzle with 0°, exit area 19.1mm²

Fig. 20. Break-up of liquid metal films using several alloys. Different film length and breakup mechanism (Achelis et al., 2010).

From the ligaments multiple droplets are generated which are clearly visible below the gasring-atomizer. The film break-up of the SnCu30 alloy is totally different. The film can be recognized as the dark area with some bright reflection zones at the surface. The film length is much longer compared to pure tin and the break-up mechanism is dominated by a perforation of the film. The holes in the film grow quickly until only ligaments are left which will break into multiple droplets as well. Finally, the last image (right) shows that the metal film of the AlSi12 alloy is again longer. Bright areas on the surface are just reflections. The spray cone is not fully developed which is indicated by the non-conical shape of the cone. A higher pressure pL is necessary to achieve a fully developed hollow cone for this alloy.

#### **5.3 Gas flow in the vicinity of the gas-ring-atomizer**

The gas flow generated by the gas ring atomizer has been studied carefully for the design of the atomizer. The gas-ring-atomizer can induce strong recirculation zones which can affect the atomization and result in an instable process. Simple pressure measurements on the centreline of the atomizer can help to understand the gas flow in the vicinity of the gas-ringatomizer. Fig. 21 shows the pressure on a tube surface located on the centreline using different gas-ring-atomizer designs. The location and the intensity of the maximum pressure indicate the risk of recirculation zones. The highest risk is given for the ring slit nozzle with a maximum pressure value of 25 kPa just 10 mm below the gas-ring-atomizer. The other atomizers have several discrete holes with different exit angles and same total exit areas of 18.5 mm². An angle of 0° represents the direction straight downwards.

The flow situation was also studied by using water as fluid instead of molten metal. To get an interior view of the spray cone a laser light sheet was used to illuminate the central plane of the spray cone (Fig. 22). White arrows exhibit the exit and direction of the gas jets. Obviously, the ring slit nozzle attacks the water film from the pressure nozzle directly and droplets come very close to the gas nozzle. In case of molten metal this will lead to an instable process. This result corresponds to the pressure measurements in the figure before. Therefore, discrete holes in the ring gas atomizer are preferred for pressure-gas-atomization. An exit angle of 0° was chosen for the atomization of molten metal.

Sn SnCu30 AlSi12

Fig. 20. Break-up of liquid metal films using several alloys. Different film length and break-

From the ligaments multiple droplets are generated which are clearly visible below the gasring-atomizer. The film break-up of the SnCu30 alloy is totally different. The film can be recognized as the dark area with some bright reflection zones at the surface. The film length is much longer compared to pure tin and the break-up mechanism is dominated by a perforation of the film. The holes in the film grow quickly until only ligaments are left which will break into multiple droplets as well. Finally, the last image (right) shows that the metal film of the AlSi12 alloy is again longer. Bright areas on the surface are just reflections. The spray cone is not fully developed which is indicated by the non-conical shape of the cone. A higher pressure pL is necessary to achieve a fully developed hollow cone for this alloy.

The gas flow generated by the gas ring atomizer has been studied carefully for the design of the atomizer. The gas-ring-atomizer can induce strong recirculation zones which can affect the atomization and result in an instable process. Simple pressure measurements on the centreline of the atomizer can help to understand the gas flow in the vicinity of the gas-ringatomizer. Fig. 21 shows the pressure on a tube surface located on the centreline using different gas-ring-atomizer designs. The location and the intensity of the maximum pressure indicate the risk of recirculation zones. The highest risk is given for the ring slit nozzle with a maximum pressure value of 25 kPa just 10 mm below the gas-ring-atomizer. The other atomizers have several discrete holes with different exit angles and same total exit areas of

The flow situation was also studied by using water as fluid instead of molten metal. To get an interior view of the spray cone a laser light sheet was used to illuminate the central plane of the spray cone (Fig. 22). White arrows exhibit the exit and direction of the gas jets. Obviously, the ring slit nozzle attacks the water film from the pressure nozzle directly and droplets come very close to the gas nozzle. In case of molten metal this will lead to an instable process. This result corresponds to the pressure measurements in the figure before. Therefore, discrete holes in the ring gas atomizer are preferred for pressure-gas-atomization.

10 mm

Verfahrensprinzip: Druck-Zerstäubung

Images from high speed video camera Recording frequency; 63 000 frames/s

**5.3 Gas flow in the vicinity of the gas-ring-atomizer** 

18.5 mm². An angle of 0° represents the direction straight downwards.

An exit angle of 0° was chosen for the atomization of molten metal.

Alloy

up mechanism (Achelis et al., 2010).

Fig. 21. Pressure on the surface of a tube placed on the centreline of the gas-ring-atomizer indicates the gas flow field in the vicinity of the atomizer. The effect of different atomizer designs is shown (Lagutkin et al., 2003a/b).

Fig. 22. Influence of different atomizer designs on the spray cone of a pressure-gas-atomizer. The central plane of the spray cone is illuminated by a laser light sheet and water is used as a liquid (Uhlenwinkel et al., 2003).

Bright area = high amount of particles

#### **5.4 Melt flow rate**

The production rate is an important feature for an atomization processes. Typically the mass flow of the pressure gas atomization can be varied between 70 and 200 kg/h using tin and tin-copper alloys. As expected, the melt flow rate can be adjusted by the pressure difference between the pressure vessel and the spray chamber. The gas pressure in the gas-ringatomizer does not influence the melt flow.

Hybrid Gas Atomization for Powder Production 119

Fig. 24. Geometric standard deviation σg versus the mass median diameter d50,3 for different alloys to characterize the particle size distribution of a pressure-gas-atomization (Achelis et

cone angle Θ. The film thickness is calculated from the equation given in (Rizk & Lefebvre,

*MD* 

 

Particle velocities are of interest for the verification of process modeling and for the calculation of cooling and solidification rates. Several measuring techniques are available to measure the particle velocity in the spray cone (e.g. Laser Doppler Anemometry LDA, Phase Doppler Anemometry PDA, Particle Image Velocimetry PIV). Some results of a PDA measurement are presented in fig. 25. Here, the mean velocity on the centreline of the spray cone is plotted versus the gas pressure in the gas-ring-atomizer at a distance of 165 mm. The molten tin was superheated to a temperature of 275 °C and the melt flow reached 180 kg/h. The variation of the gas pressure resulted in a gas mass flow range between 117 and 198 kg/h. Because of the increased gas flow the mean particle size was reduced and both higher gas velocities and smaller particles added up to mean particle velocity between 70 and 135

Generally, inert gas atomized metal show spherical shape. Therefore, the mean circularity C = 4π projection area / (perimeter)² of the particles is close to 1.0. But frequent collisions between liquid or semi-liquid droplets and solidified particles in the spray cone can result in

 

66.3 (2)

*LL LLL p*

 and *ML* , and the spray

from the orifice, the film thickness δ, the melt and gas mass flow *MG*

1985 cited in Achelis, 2009) for a pressure atomizer:

In equation (2) DL means the exit diameter of the nozzle.

al., 2010).

**5.6 Particle velocity** 

m/s.

**5.7 Particle shape** 

#### **5.5 Particle size**

Typically, the mass median diameter without gas atomization (only pressure-atomizer) are in the range of 400 to 500 µm. The gas to metal ratio (GMR, here in kg gas / kg melt) is the key parameter to control the mean particle size. Fig. 23 shows that already with low GMR (below 1.0) the mass median diameter can be varied between 40 and 100 µm for pure tin. Even mean particles sizes of approximately 20 µm can be achieved. An increase of the copper content up to 50 weight percent does not make a big difference to the mass median diameter. Only a copper content of 63 weight percent results in larger mean particle sizes. It is assumed the higher surface tension is the main reason for this behavior. All measurements were accomplished by laser diffraction. A superheat of 100 K in the crucible was enough to achieve mostly spherical particles.

Fig. 23. Effect of the GMR on the mass median diameter for different alloys. The superheat TS was almost 100K above the liquidus temperature of the alloy (Achelis et al., 2009).

Normally, the size distribution is characterized by another parameter, for example the geometric standard deviation σg = d84,3/d50,3 = d50,3/d16,3 . Both values are the same if the distribution follows a log-normal size distribution. Here, the standard deviation is defined as σg = d84,3/d50,3. The results in fig. 24 are plotted versus the mass median diameter. Obviously, the geometric standard deviation depends on the mean particle size and a low mean particle size results in a higher geometric standard deviation. This holds for pure tin and this tin-copper alloys as well. A standard deviation below 2.0 achieved by a gas atomization technique is considered extremely good.

Of course, there are other parameters effecting the particle size distribution, specially the design of the atomizers. But the examples shown are representative. The mass median diameter can be calculated by the following semi-empirical equation (Achelis, 2009):

$$d\_{g\_{0,3}} = 1.45 \, m \left[ 0.07 \left( \frac{\sigma\_L}{\rho\_G \, u\_G^2} \right)^{0.6} \left( \frac{\rho\_L}{\rho\_G} \right)^{0.1} \delta^{0.4} \left( 1 + \frac{\dot{M}\_L}{\dot{M}\_G} \right) + 0.01 \left( \frac{\eta\_L^2}{\sigma\_L \rho\_L} \right)^{0.5} \left( 1 + \frac{\dot{M}\_L}{\dot{M}\_G} \right) \right] \left( \frac{360}{\Theta} \right)^{0.37} \tag{1}$$

Here, the mass median diameter d50,3 (in m) depends on the surface tension σL, density ρ<sup>L</sup> and viscosity ηL of the melt, the gas density ρG, the gas velocity uG at a distance of 25 mm

Typically, the mass median diameter without gas atomization (only pressure-atomizer) are in the range of 400 to 500 µm. The gas to metal ratio (GMR, here in kg gas / kg melt) is the key parameter to control the mean particle size. Fig. 23 shows that already with low GMR (below 1.0) the mass median diameter can be varied between 40 and 100 µm for pure tin. Even mean particles sizes of approximately 20 µm can be achieved. An increase of the copper content up to 50 weight percent does not make a big difference to the mass median diameter. Only a copper content of 63 weight percent results in larger mean particle sizes. It is assumed the higher surface tension is the main reason for this behavior. All measurements were accomplished by laser diffraction. A superheat of 100 K in the crucible

**Gas to metal ratio (GMR)** Fig. 23. Effect of the GMR on the mass median diameter for different alloys. The superheat TS was almost 100K above the liquidus temperature of the alloy (Achelis et al., 2009).

Normally, the size distribution is characterized by another parameter, for example the geometric standard deviation σg = d84,3/d50,3 = d50,3/d16,3 . Both values are the same if the distribution follows a log-normal size distribution. Here, the standard deviation is defined as σg = d84,3/d50,3. The results in fig. 24 are plotted versus the mass median diameter. Obviously, the geometric standard deviation depends on the mean particle size and a low mean particle size results in a higher geometric standard deviation. This holds for pure tin and this tin-copper alloys as well. A standard deviation below 2.0 achieved by a gas

Of course, there are other parameters effecting the particle size distribution, specially the design of the atomizers. But the examples shown are representative. The mass median

<sup>360</sup> 1.45 0.07 <sup>1</sup> 0.01 <sup>1</sup>

 

*G L*

*M M*

  0.37 0.5 <sup>2</sup>

*M M*

*G L*

 

 

(1)

 

 

*L L L*

 

 

diameter can be calculated by the following semi-empirical equation (Achelis, 2009):

0.6 0.1

*G L*

*<sup>u</sup> <sup>d</sup> <sup>m</sup>*

 

0.4

 

Here, the mass median diameter d50,3 (in m) depends on the surface tension σL, density ρ<sup>L</sup> and viscosity ηL of the melt, the gas density ρG, the gas velocity uG at a distance of 25 mm

**5.5 Particle size** 

was enough to achieve mostly spherical particles.

**Mass** 

atomization technique is considered extremely good.

50,3 2

   

*G G L*

**median diameter**

 **d50,3 [µm]**

**Druck-Gas-Zerstäuber**

Fig. 24. Geometric standard deviation σg versus the mass median diameter d50,3 for different alloys to characterize the particle size distribution of a pressure-gas-atomization (Achelis et al., 2010).

from the orifice, the film thickness δ, the melt and gas mass flow *MG* and *ML* , and the spray cone angle Θ. The film thickness is calculated from the equation given in (Rizk & Lefebvre, 1985 cited in Achelis, 2009) for a pressure atomizer:

$$\delta = 3.66 \left( \frac{D\_L \, \dot{M}\_L \, \eta\_L}{\rho\_L \, \Delta p\_L} \right) \tag{2}$$

In equation (2) DL means the exit diameter of the nozzle.

#### **5.6 Particle velocity**

Particle velocities are of interest for the verification of process modeling and for the calculation of cooling and solidification rates. Several measuring techniques are available to measure the particle velocity in the spray cone (e.g. Laser Doppler Anemometry LDA, Phase Doppler Anemometry PDA, Particle Image Velocimetry PIV). Some results of a PDA measurement are presented in fig. 25. Here, the mean velocity on the centreline of the spray cone is plotted versus the gas pressure in the gas-ring-atomizer at a distance of 165 mm. The molten tin was superheated to a temperature of 275 °C and the melt flow reached 180 kg/h. The variation of the gas pressure resulted in a gas mass flow range between 117 and 198 kg/h. Because of the increased gas flow the mean particle size was reduced and both higher gas velocities and smaller particles added up to mean particle velocity between 70 and 135 m/s.

#### **5.7 Particle shape**

Generally, inert gas atomized metal show spherical shape. Therefore, the mean circularity C = 4π projection area / (perimeter)² of the particles is close to 1.0. But frequent collisions between liquid or semi-liquid droplets and solidified particles in the spray cone can result in

Hybrid Gas Atomization for Powder Production 121

1.0 and the SEM picture on the right side confirms this result clearly. Without gas recirculation the circularity drops considerably and SEM figure shows the reason of this

Gas atomization is the most versatile method to produce powders by atomization of a liquid melt. In this context, free-fall atomizers are external mixing gas atomizers based on a combination of a primary and a secondary gas nozzle. The primary gas stabilizes the atomization process and the secondary gas is used for atomization of the liquid. If only the secondary gas is used, a gas recirculation flow underneath the secondary nozzle occurs. This recirculation flow may cause the transport of atomized ligaments or droplets in the direction of the atomizer body. Liquid impinging on the atomizer body may clog the gas orifices and badly influence the atomizer performance. Thus in common free-fall atomizer design, the primary gas is used to suppress the recirculation flow and to stabilize the atomization

To improve the operating conditions and to overcome limitations of the free-fall atomizer, a Coanda-flow ring device was developed and installed inside the secondary gas flow. By using the Coanda-flow device, the secondary gas flow is deflected in the downward direction, the entrainment mass flow is increased, and, therefore, a primary gas nozzle is not necessary for suppression of gas recirculation. The concept was derived and verified by means of numerical gas flow simulations and model experiments. The application of the flow-adapted design option for free-fall atomizers was demonstrated by the atomization of a viscous melt. The results indicated a stable operation of the free-fall atomizer even at higher

The concept of a prefilming hybrid atomizer has been introduced. The atomizer is designed for atomizing highly viscous liquids and melts. Physical gas flow effects are utilized to increase the atomizer efficiency. The hybrid atomizer design is based on numerical flow simulations of the gas phase. Experiments where water a viscous model liquid (glycerol) a have been atomized with air show a higher disintegration efficiency than a conventional external mixing atomizer for the viscous liquid atomization process. Model experiments atomizing fluids of low viscosity like water show an insufficient atomization efficiency of the hybrid atomizer design. Thus the hybrid atomizer concept is a novel device for highly viscous liquids and melts. The experimental results for atomization of a mineral melt by heated gases underline the success of the hybrid atomization process with some limitations. For the present conditions, a minimum mass-median particle size of 210 µm has been achieved. The coarse product obtained by melt atomization is due to limitations of the available maximum

The complexity of the pressure-gas-atomization is a drawback for frequent applications in industry. To overcome the problem the system can be simplified in the future if it is used with low melting point alloys. Today, pumps for molten metal like tin alloys are available and the complexity of the system can be reduced considerably because a pressure vessel is

Another future objective is the use of the pressure-gas-atomizer for coating applications. It has already been proofed that this atomization system is dedicated to generate thick

atomization gas temperature and may be overcome in future developments.

not necessary anymore and thus the process principally can operate continuously.

behavior in agglomerates and multiple satellites.

**6. Conclusions and future Investigations** 

secondary gas pressures, as well as a finer particle yield.

process.

Fig. 25. Correlation between pressure in the gas nozzle and mean particle velocity on the centreline for pure tin measured by Phase-Doppler-Anemometry (Lagutkine et al., 2004a)

agglomerations and/or multiple small particles (satellites) attached to a bigger one. This will reduce the flowability of the powder which is an important quality feature. Often, satellites occur because of the gas flow in the spray chamber. Close to the wall of the spray chamber the gas velocity direction is contrary to the main flow direction and small particles are transported to the spray cone again and collide with the droplets. This recirculation zone inside the spray chamber can be avoided by a recirculation of the clean gas (after the particle collector (cyclone and/or filter) and the fan). The clean gas is added at the top of the spray chamber and - as a side effect – leads to a better visibility of the atomization process.

There appears to be a significant influence of the gas recirculation on the circularity of the powder (figure 26). With gas recirculation the mean circularity of the powder is very close to

Fig. 26. Mean circularity versus mass median diameter with/without gas recirculation measured by image analysis (G3 Morphology, Malvern), (Achelis et al., 2010)

**Pressure in the gas nozzle [MPa]**

Fig. 25. Correlation between pressure in the gas nozzle and mean particle velocity on the centreline for pure tin measured by Phase-Doppler-Anemometry (Lagutkine et al., 2004a)

chamber and - as a side effect – leads to a better visibility of the atomization process.

agglomerations and/or multiple small particles (satellites) attached to a bigger one. This will reduce the flowability of the powder which is an important quality feature. Often, satellites occur because of the gas flow in the spray chamber. Close to the wall of the spray chamber the gas velocity direction is contrary to the main flow direction and small particles are transported to the spray cone again and collide with the droplets. This recirculation zone inside the spray chamber can be avoided by a recirculation of the clean gas (after the particle collector (cyclone and/or filter) and the fan). The clean gas is added at the top of the spray

There appears to be a significant influence of the gas recirculation on the circularity of the powder (figure 26). With gas recirculation the mean circularity of the powder is very close to

**Mass median diameter d50,3 [µm]**

Fig. 26. Mean circularity versus mass median diameter with/without gas recirculation

measured by image analysis (G3 Morphology, Malvern), (Achelis et al., 2010)

**with gas recirculation without gas recirculation**

**Druck-Gas-Zerstäuber**

**Mean particle velocity [m/s]**

**Mean circularity [-]** 1.0 and the SEM picture on the right side confirms this result clearly. Without gas recirculation the circularity drops considerably and SEM figure shows the reason of this behavior in agglomerates and multiple satellites.

#### **6. Conclusions and future Investigations**

Gas atomization is the most versatile method to produce powders by atomization of a liquid melt. In this context, free-fall atomizers are external mixing gas atomizers based on a combination of a primary and a secondary gas nozzle. The primary gas stabilizes the atomization process and the secondary gas is used for atomization of the liquid. If only the secondary gas is used, a gas recirculation flow underneath the secondary nozzle occurs. This recirculation flow may cause the transport of atomized ligaments or droplets in the direction of the atomizer body. Liquid impinging on the atomizer body may clog the gas orifices and badly influence the atomizer performance. Thus in common free-fall atomizer design, the primary gas is used to suppress the recirculation flow and to stabilize the atomization process.

To improve the operating conditions and to overcome limitations of the free-fall atomizer, a Coanda-flow ring device was developed and installed inside the secondary gas flow. By using the Coanda-flow device, the secondary gas flow is deflected in the downward direction, the entrainment mass flow is increased, and, therefore, a primary gas nozzle is not necessary for suppression of gas recirculation. The concept was derived and verified by means of numerical gas flow simulations and model experiments. The application of the flow-adapted design option for free-fall atomizers was demonstrated by the atomization of a viscous melt. The results indicated a stable operation of the free-fall atomizer even at higher secondary gas pressures, as well as a finer particle yield.

The concept of a prefilming hybrid atomizer has been introduced. The atomizer is designed for atomizing highly viscous liquids and melts. Physical gas flow effects are utilized to increase the atomizer efficiency. The hybrid atomizer design is based on numerical flow simulations of the gas phase. Experiments where water a viscous model liquid (glycerol) a have been atomized with air show a higher disintegration efficiency than a conventional external mixing atomizer for the viscous liquid atomization process. Model experiments atomizing fluids of low viscosity like water show an insufficient atomization efficiency of the hybrid atomizer design. Thus the hybrid atomizer concept is a novel device for highly viscous liquids and melts. The experimental results for atomization of a mineral melt by heated gases underline the success of the hybrid atomization process with some limitations. For the present conditions, a minimum mass-median particle size of 210 µm has been achieved. The coarse product obtained by melt atomization is due to limitations of the available maximum atomization gas temperature and may be overcome in future developments.

The complexity of the pressure-gas-atomization is a drawback for frequent applications in industry. To overcome the problem the system can be simplified in the future if it is used with low melting point alloys. Today, pumps for molten metal like tin alloys are available and the complexity of the system can be reduced considerably because a pressure vessel is not necessary anymore and thus the process principally can operate continuously.

Another future objective is the use of the pressure-gas-atomizer for coating applications. It has already been proofed that this atomization system is dedicated to generate thick

Hybrid Gas Atomization for Powder Production 123

Czisch, C.; Lohner, H.; Fritsching, U., Bauckhage, K. & Edlinger, A. (2003). in: K. Bauckhage,

Czisch, C.; Lohner, H. & Fritsching, U. (2004). Einfluss der Gasdüsenanordnung auf den

Czisch, C. & Fritsching, U. (2008a). Flow-adapted design for Free-fall atomizers, *Atomization* 

Czisch, C. & Fritsching, U. (2008b). Atomizer design for viscous-melt atomization, Mat. Sci.

Dunkley, J.J. & Sheikhaliev, S. (1995): Single Fluid Atomization of Liquid Metals, *Proceedings* 

Dunkley J.J. (2001). in: 2001 International Conference on Powder Metallurgy and Particulate

Fritsching, U. (2004). *Spray Simulation: Modeling and Numerical Simulation of Sprayforming* 

Fritsching, U. & Bauckhage, K. (2006a). *Sprayforming of Metals*, in: Ullmann´s Encyclopedia

Fritsching, U. (2006b). Spray Systems, in: Multiphase Flow Handbook, Ed.: C.T. Crowe, CRC-Press, Boca Raton, Fl, USA, 2006, Chapter 8, pp. 8.1 - 8.100; ISBN: 0849312809

Heck, U. (1998). *Zur Zerstäubung in Freifalldüsen*, VDI Verlag GmbH Düsseldorf, Germany Heck, U.; Fritsching, U. & Bauckhage, K. (2000). Gas-Flow Effects on Twin-Fluid Atomization of Liquid Metals, *Atomization and Sprays,* Vol. 10, No. 1, pp. 25 – 46 Lagutkin, S.; Achelis, L.; Sheikaliev, S.; Uhlenwinkel, V. & Srivastava V. (2003a):

*Spray Deposition and Melt Atomization 2003*, Bremen (Germany), June, 2003, Lagutkin, S. (2003b): *Development of Technology and Equipment for Metal Powder Production by* 

Lagutkin, S.; Uhlenwinkel, V.; Achelis, L.; Pulbere, S. &. Sheikhaliev S. (2004a): Centrifugal-

Fraser, R.P.; Dombrowski, N. & Routley, J.H. (1962). *Chem. Eng. Sci.,* Vol. 18, pp. 339-353 Fritsching, U. & Bauckhage, K. (1992). Investigations on the atomization of molten metals:

*and Melt Atomization Conf. SDMA 2003*, Bremen, 22.-25.6.2003

zerstäubung, *Chem.-Ing.-Tech.*, Vol. 76, No. 6, pp. 754-757

Dombrowski, N. & Johns, W.R. (1963). *Chem. Eng. Sci.*, Vol. 3, pp. 203-214

*Metals*, Cambridge University Press, Cambridge, UK

*and Sprays*, Vol. 18 No. 6, pp. 511-522

Engng. A Vol. 477 No. 1-2, pp. 21-25

(USA), May 1995, Vol. 1, pp. 79-87

*Dynamics,* Vol. 5, No. 1, pp. 81-98

Academy of Sciences. 2003, in Russian

Lefebvre, A.H. (1980). *Prog. Energy Combust. Sci.*, Vol. 6, pp. 233-261 Lefebvre, A.H. (1989). *Atomization and Sprays*, Hemisphere Publ. Corp., US

Princeton, USA

Weinheim, Germany

U. Fritsching, J. Ziesenis, A. Uhlenwinkel, A. Leatham (Eds), *Proc. Spray Deposition* 

Desintegationsvorgang und das Zerstäubungsergebnis bei der Zweistoff-

*of the International Conference on Powder Metallurgy & Particulate Materials*, Seattle

Materials PM2TEC 01, 2-29-2-35, 2001, Metal Powder Industries Federation,

The coaxial jet and the gas flow in the nozzle near field, *PHOENICS J. Comp. Fluid* 

of Industrial Chemistry, 7th Edition, 2006 Electronic Release, Wiley VCH,

Atomisation Process for Metal Powder. *Proceedings of the International Conference on* 

*Centrifugal-Gas Atomization of Melt*. Ph.D. thesis. Ekaterinburg, Ural Department of

Gas Atomization: Preliminary Investigation of the Method, *Proc. International Conference on Powder Metallurgy 2004*, Wien, Austria, Oct. 2004, Vol. 1, S.71-76 Lagutkin, S.; Achelis, L.; Sheikhaliev, S.; Uhlenwinkel, V. & Srivastava V. (2004b): Atomization process for metal powder. *MSE-A* 383 (1), (2004), pp. 1-6 Lavernia, E.J. & Wu, Y. (1996). *Spray Atomization and Deposition*, J. Wiley & Sons, Chichester

coatings on a tube. As an example a steel tube with a diameter of the 80 mm was coated with a 10 mm thick tin layer. The density of the coating was much better the than 99% of the full density (Uhlenwinkel et al., 2008).

#### **7. Acknowledgments**

The results that have been presented here are mainly based on the project work of several PhD students at the Particles and Process Engineering department of the University of Bremen. Namely the contributions of Dr.-Ing. L. Achelis, Dr.-Ing. S. Markus, Dr.-Ing. H. Lohner, Dr.-Ing. U. Heck, Dr. S. Pulbere and Dr.-Ing. C. Czisch are acknowledged. The cooperation in these fields with international colleagues, namely Dr. S. Lagutkin, Prof. S. Sheikhaliev and Dr. V. Srivastava is greatfully acknowledged.

The financial support of the projects has been mainly given by the German Research Foundation (DFG), whose support during the past decade in several areas and through projects is greatfully acknowledged.

#### **8. References**


coatings on a tube. As an example a steel tube with a diameter of the 80 mm was coated with a 10 mm thick tin layer. The density of the coating was much better the than 99% of the

The results that have been presented here are mainly based on the project work of several PhD students at the Particles and Process Engineering department of the University of Bremen. Namely the contributions of Dr.-Ing. L. Achelis, Dr.-Ing. S. Markus, Dr.-Ing. H. Lohner, Dr.-Ing. U. Heck, Dr. S. Pulbere and Dr.-Ing. C. Czisch are acknowledged. The cooperation in these fields with international colleagues, namely Dr. S. Lagutkin, Prof. S.

The financial support of the projects has been mainly given by the German Research Foundation (DFG), whose support during the past decade in several areas and through

Achelis, L.; Uhlenwinkel, V.; Lagutkin S. & Sheikhaliev, S. (2006): Atomization Using a

Achelis, L. & Uhlenwinkel, V. (2008): Characterisation of metal powders generated by a

Achelis L. (2009): *Kombinierte Drall-Druck-Gaszerstäubung von Metallschmelzen*. Shaker Verlag,

Achelis, L.; Sulatycki, K.; Uhlenwinkel, V. & Mädler, L. (2010): Spray angle and particle size

Metal Powder Industries Federation, Princeton, N.J., Vol. 20, pp. 205–223

Bauckhage, K. & Fritsching U. (2000). in: K.P. Cooper, I.E. Anderson, S.D. Ridder, F.S.

Bergmann, D.; Fritsching, U. & Bauckhage, K. (2001) Simulation of molten metal droplet

Bradley, D. (1973). On the atomization of liquids by high-velocity gases, Part 1, *J. Phys. D: Appl. Phys.*, Vol. 6, 1724–1736, Part 2, *J. Phys. D: Appl. Phys.*, Vol. 6, pp. 2267–2272 Campanile, F. & Azzopardi, B.J. (2003). in: Cavaliere, A. (Ed) CD-ROM *Proc. International* 

Bayvel, L. & Orzechowski, Z. (1993). *Liquid Atomization*, Taylor & Francis ,Washington Bauckhage, K. (1992). Das Zerstäuben metallischer Schmelzen, *Chem.-Ing.-Tech.*, Vol. 64 No.

Pressure-Gas-Atomizer. *Proceedings of the International Conference on Powder* 

in the pressure gas atomization of tin and tin-copper alloys, *Proceeding of the International Conference on Powder Metallurgy 2010*, Florence (Italy), October 2010 Anderson, I.E. & Figliola, R.S. (1998). Observations of gas atomization process Dynamics, in

*Modern Developments in Powder Metallurgy*, Gummeson, P.U. &Gustafson, D.A. Eds.,

Biancaniello (Eds.) *Liquid Metal Atomization: Fundamentals and Practice*, TMS,

*Conference on Liquid Atomization and Spray Systems ICLASS 2003*, Sorrento, Italy, 13-

full density (Uhlenwinkel et al., 2008).

projects is greatfully acknowledged.

4, pp. 322–332

Warrendale, USA, pp. 23 – 36

17.07.2003, ILASS-Europe

**8. References** 

Sheikhaliev and Dr. V. Srivastava is greatfully acknowledged.

*Metallurgy 2006*, Busan (South Koria), Sept. 2006

Aachen 2009, ISBN 978-3-8322-8012-3

pressure-gas-atomizer. *MSE A* 477 (2008), pp.15-20

Ashgriz, N. (2011). *Handbook of Atomization and Sprays*, Springer, New York

sprays, *Comp. Fluid Dynamics-Journal,* Vol. 9, pp. 203 – 211

**7. Acknowledgments** 


Liu, H. (2000) *Science and Engineering of Droplets: Fundamentals and Applications,* William

Lohner, H. (2002). *Zerstäuben von Mineralschmelzen mit Heißgas,* PhD. thesis, University

Lohner, H.; Czisch, C. & Fritsching, U. (2003). Impact of Gas Nozzle Arrangement on the

Lohner, H.; Czisch, C.; Schreckenberg, P.; Fritsching, U. & Bauckhage, K. (2005). Atomization of viscous melts, *Atomization and Sprays*, Vol. 15, No. 2, pp. 169-180 Markus, S.; Fritsching, U. & Bauckhage, K. (2002). Jet Break Up of Liquid Metals in Twin

Pickering, S.J.; Hay, N.; Roylance, T.F. & Thomas, G.H. (1985). *Ironmaking and Steelmaking*,

Rizk, N.K. & Lefebvre A.H. (1985) : Internal Flow Characteristics of Simplex Swirl Atomizer. *Journal of propulsion and power*, Vol. 1 (1985) No. 3, New York, pp. 193-199 Strauss, J.T. (1999). Hotter gas increases atomization efficiency, *Metal Powder Report,* Vol. 11,

Uhlenwinkel, V. & Sheikhaliev S., et al. (2002): *Verfahren und Vorrichtung zum Herstellen von* 

Uhlenwinkel, V.; Achelis, L.; Sheichaliev, S. & Lagutkin, S. (2003): A new Technique for Molten Metal Atomization. *Proc. ICLASS 2003*, Sorento, Italy, June, 2003 Uhlenwinkel, V.; Achelis, L. & Mädler, L. (2008): New atomization process to achieve high

production rates during thermal spraying of thick coatings, Proceedings of the *International Thermal Spray Conference 2008*, Maastricht (Netherlands), June 2008 Wille, R. Fernholz, H. (1965). Report on the First European Mechanics Colloquium on the

*Metallpulver und keramischem Pulver*, Pat.Nr. 10237213, 14.Aug. 2002

Yule, A.J. & Dunkley J.J. (1994). *Atomization of Melts*, Clarendon Press Oxford, UK

Coanda Effect, *J. Fluid Mech.*, Vol. 23, pp. 801-819

Fluid Atomization, *Materials Sci. & Engng. A*, No. 326, pp. 122 – 133

*Atomization and Spray Systems*, Sorrento, Sep. 2003 (Italien)

Flow Field of a Twin Fluid Atomizer with External Mixing, *Int. Conf. on Liquid* 

Andrew Publ., Norwich, USA

Bremen

Vol. 12 No. 1

pp. 24-28

## *Edited by Katsuyoshi Kondoh*

From high-performance, economical and environmental points of view, Powder metallurgy process shows remarkable advantages in production of parts and components due to their special compositions by elemental mixing and 3-dimensional near net shape forming methods. Powder metallurgy process can be applied to not only metal materials but also ceramics and organic materials, which both are employed as structural and electrical products. Author contributions to Powder metallurgy present excellent and significantly important research topics to evaluate various properties and performance of P/M materials for applying these materials as actual components. In particular, the life estimation of P/M ferrous materials by sliding contact fatigue test and tribological performance evaluation of P/M semi-metallic materials are focused and introduced in this book.

Powder Metallurgy

Powder Metallurgy

*Edited by Katsuyoshi Kondoh*

Photo by Spantomoda / iStock