Injection Performance of a Gas-Solid Injector Based on the Particle Trajectory Model
Gas-solid injectors are widely used feeding equipment in pneumatic conveying systems. The performance of a gas-solid injector has a significant influence on the type of application it can be employed for. To determine the key factors influencing the injection performance and address clogging problems in a gas-solid injector during a pneumatic conveying process, the particle trajectory model has been utilised as a means to perform simulations. In the particle trajectory model, the gas phase is treated as a continuous medium and the particle phase is treated as a dispersed phase. In this work, numerical and experimental studies were conducted for different nozzle positions in a gas-solid injector. A gas-solid injector test-bed was constructed based on the results of the simulations. The results show that the nozzle position is the key factor that affects the injection performance. The number of extrusive particles first increases and then decreases with the change in the nozzle position from left to right. Additionally, there is an optimum nozzle position that maximises the injection mass and minimises the number of particles remaining in the hopper. Based on the results of this work, the injection performance can be significantly increased and the clogging issues are effectively eliminated.
A gas-solid injector is an important piece of feeding equipment in pneumatic conveyers, which are widely used in the petroleum and chemical industries, material conveying, power stations, and other departments. They possess a simple structure, no moving parts, and concatenate conveniently with other pieces of equipment [1, 2]. Many methods have been used to simulate gas-solid fluidisation. Some examples include the two-fluid smoothed particle hydrodynamics method (TF-SPH) , the multilattice deterministic trajectory model (MLDT) , the multifluid model (MFM), the two-fluid model (TFM) , and the discrete phase model (DPM) . In addition, particle trajectory models (PTMs) are also widely used because they require fewer partial differential equations when addressing the dispersed phase and because they provide exact results when forecasting the particle distribution [7–9]. The particle trajectory model is mainly used to forecast the movement of dilute particle phases in a turbulent flow. The Lagrangian solution model is adopted to address the particle phase. The particle-particle and particle-wall collisions are calculated using a statistical method that is not restricted by the number of particles [10, 11].
Practically, gas-solid injectors may jam depending on the particle diameter and as the volume being conveyed increases. These issues restrict their application and development when dealing with large-sized particles and large-mass flow pneumatic conveying. Many scholars have studied the conveying properties and static pressure distributions in gas-solid injectors and agree that the location of the driving nozzle and the angle of the converging section have an obvious influence on the maximum achievable mass flow rate [12–15]. The goal of this paper is to improve the injection performance of a gas-solid injection (to increase the conveying properties) and determine the key factors that affect the injection performance. The particle trajectories were simulated in a uniform flow field using the PTM and the injection performance at different driving nozzle locations was obtained by analysing the number of injected particles. Finally, a gas-solid injector test-bed was built to investigate the injection performance and verify the simulation models and results.
2. Mathematical Model
The movement of the particles is determined by the interactions between the solid and gas phases, which are determined in two ways. The first is by the exchange of mass, momentum, and energy. The second is through particle-particle and the particle-wall collisions. The particle trajectories are obtained by the PTM, which uses different handling methods for the gas and particle phases. The gas phase is treated as a continuous medium and the variables of the gas phase are obtained by solving the gas control equation. The particle phase is treated as a dispersed phase and the Lagrangian method is used to track the particle trajectories. The mass, momentum, and energy of the gas and particle phases are exchanged during the iterative process .
2.1. Gas Control Equation
The gas phase is treated as a continuous medium in the PTM. Therefore, the gas phase continuity and momentum equations are based on the law of conservation of mass and Newton’s second law [17, 18]. In addition, the interactions between the gas and particles are considered. For larger particle diameters of up to 5 mm, additional interactions are added to the gas control continuity equation:where is the density of gas phase, is the coordinate of direction, is the velocity component of the gas phase in the direction, is the particle phase volume fraction in the gas-solid two-phase mixture, is the number density of the particle phase, and is the single particle mass. The momentum equation is defined aswhere is the dynamic viscosity of the gas phase, is the coordinate of direction, is the velocity component of the gas phase in the direction, is the density of the particle phase in the gas-solid two-phase mixture, is the velocity component of gas phase in the direction, and is the diffuse relaxation time of the particle phase. Equations (1) and (2) are obtained from [17, 18].
The above control equations are all for the gas phase. There are a total of four control equations when we consider the momentum equations and the three directions in the coordinate system. Therefore, the unknown variables for the gas phase are , , , , and . These are addressed by solving the closed form of the turbulence model . The turbulent kinetic energy and turbulent momentum dissipation equations are shown respectively:Equations (3) and (4) are obtained from Yakhot and Orszag’s work .
2.2. Trajectory Equation of Particle Phase
The force analysis on the particle phase was performed using Newton’s second law in the PTM and the particle trajectory equations were acquired by integrating twice.
2.2.1. Motion Equation
The particle motion equation (Figure 1) is shown in the following equation, which is obtained from Newton’s second law:where is the particle velocity, is the average particle mass, is the fluid drag force on the particle, is the force of gravity on the particle, and represents the other forces on the particle.
The other particle forces include the Saffman force, the Brown force, and the Magnus force. In this study, the particle diameter is 5 mm, meaning that the Brown force and the Magnus force have little effect on the particle movement, as described in [21–24]. Therefore, these forces are ignored when considering the particle state of motion.
The fluid drag force is defined as where is the particle density, is the particle diameter, is the fluid drag coefficient, which is defined as when the particle diameter is 5 mm, is the gas velocity, and is the particle velocity.
The Saffman force is defined aswhere is the Saffman force constant, which is defined as and is the deformation tenser.
2.2.2. Particle Trajectory
When the particles are in a uniform flow field and do not collide with the walls or other particles, as described in (5), the particle trajectory equations may be defined as follows: -direction: -direction: -direction: assuming that the initial particle velocities in the - and -directions are zero. By substituting (6) and (7) into (8)~(10), the particle phase trajectory equations in the -, -, and -directions may be obtained by integrating twice: -direction: -direction: -direction: where , , and are the initial particle coordinates in the -, -, and -directions, is the computational coefficient of fluid drag, is the computational coefficient of the Saffman force, is the coefficient of the simplified equation, , , and are the gas velocities in the -, -, and -directions, is the difference in the initial gas and particle velocities, and and are the coefficients generated when simplifying the integral computation. These coefficients are shown in
The particle velocity recovery factor for the collisions with the wall is determined from Alister’s experiment . There is a close relationship between the recovery factor and the particle impact angle, which is defined as where is the normal recovery factor, is the tangential recovery factor, and is the particle impact angle.
The flow field of the gas phase in the gas-solid injector is calculated using a colocated grid with the SIMPLE method. The particle coordinate positions are solved using the equations of motion. Additionally, the solid volume percentage of the colocated grids is also calculated. Then, the calculated value is returned for the calculation of the flow field. In this method, the coupled solution for the determination of the continuous fluid and particle phases may be alternated.
3.1. Simulation Model and Initial Parameters
The gas-solid injector consists of a driving nozzle, feed opening, mixing chamber, contraction section, and delivery pipe (Figure 2). The inner diameter of the driving nozzle is 20 mm, the diameter of the delivery pipe is 14 mm, and the inclination angle is 8°. The nozzle locations addressed by the four models are , , , and , respectively. The initial parameters for the simulation model are shown in Table 1. The feeding time was set to be 0.2 s and 0.4 s, respectively, to prevent the material from becoming plugged in the gas-solid injector.
3.2. Simulation Results
One group of steady-state simulations and two groups of transient simulations were conducted for different feeding times and particle trajectories in the gas-solid injector to analyse the injection mass.
The coordinates at each time step are solved using the PTM. The particle trajectories are shown in Figure 3 after the particle coordinates are projected into the gas-solid injection model. The nozzle locations at , , , and are shown in Figure 3-, , , and , respectively.
The injection block not only increases the use cost but also reduces the reliability of the pneumatic conveying system. Reducing the number of particles in the injector may alleviate material blockage issues and achieve a balance between the feeding mass and the extrusive mass. A statistical analysis of the extrusive number and the residual number of particles is conducted separately for each of the four models. The statistical results are shown in Figures 4–7.
The number of extrusive particles and particles remaining in the hopper for a 0.2 s feeding time is shown in Figures 4 and 5, respectively, where the horizontal axis represents the simulation time and the vertical axis represents the number of particles remaining in the hopper.
The number of extrusive particles and the number of particles remaining in the hopper for a 0.4 s feeding time are shown in Figures 6 and 7, respectively, where the horizontal axis represents the simulation time and the vertical axis represents the remaining number of particles in the hopper.
4.1. Experimental Equipment
The gas-solid injector test-bed consists of a gas inlet, a bolt, flange, support frame, injector, and hopper (Figure 8). One side of the gas inlet connects the gas-holder and the other side inserts into the injector through the flange and is fixed by the bolt, which can move up and down in the axial direction.
4.2. Test Objective and Method
A mixture of sediment and stone was used with the gas-solid injector test-bed to explore the influence of the nozzle position on the injection performance and verify the simulation results. The material supply pipe had an inner diameter of 80 mm and is divided into eight equal parts along the axial direction of mixture chamber. These parts are denoted by A to I from left to right. The nozzle was placed in a position and the mixture was continually dropped into the hopper. The injected material was gathered every five minutes after a relatively stable injection mass is achieved. The results from the tests are shown in Table 2.
4.3. Experiment Results
The jet gas flow caused a significant number of impacts and there was a great deal of noise when the nozzle was located at point A. The material erupted in reverse from the hopper, leading to the failure of the test. Only a handful of the material was injected into the mixture chamber because the material could not be mixed with the high-speed gas when the nozzle was located at point I. The average injection mass was adjusted by eliminating the data at nozzle locations A and I. The fitted curve is shown in Figure 9 and the relationship between the average injection mass and the nozzle location is expressed in which achieved an -squared value of .
The particle trajectories in the mixing chamber of the gas-solid injectors, which are shown in Figure 3-, are sparser compared to the other three models when using the PTM, which indicates less particle deposition and particle-wall collisions. In contrast, the particle trajectories shown in Figures 3- and 3- are denser, indicating more particle deposition and energy consumption, an unstable flow field, and a greater degree of wear in mixing chamber. The particle trajectories in the delivery pipe, shown in Figure 3-, exhibit a greater degree of linearity compared to the other three models when using the PTM, which indicates less collisions between the particles and wall. The other three models exhibit clear particle-particle or particle-wall collisions. In general, a greater number of collisions lead to a greater degree of wear and higher energy consumption in the pipes. As a result, the material conveying process becomes more difficult.
The particles are injected over 0.15 s and the number of extrusive particles increases from 0.18 s to 0.22 s. From 0.25 s to 0.34 s, the particle count increases steadily before beginning a downward trend after 0.35 s and sharply declines during the 0.38 s~0.50 s period (Figure 4). The number of extrusive particles is largest when the nozzle is at . Additionally, a small increase occurs from 0.50 s to 0.75 s when the nozzle is at and . This illustrates that, during this time, the sedimentary particles at the bottom of injector reenter the flow field and are ejected out of the mixing chamber.
The number of remaining particles is less using the PTM than that for the other three injector models when the nozzle location is at after 0.22 s (Figure 5). Remarkably, the number of particles for all four models peaks at 0.30 s (after the feeding stops). The curves are similar for nozzle locations at and after 0.30 s. The curves are also similar when the nozzle location is at and . However, the number of particles remaining in the hopper in the latter is less than the former after 0.70 s to the end of the injection period because the flow field experienced acute fluctuations when the sedimentary particles quickly reentered the flow field.
As the feeding time increases, the number of extrusive particles reaches a maximum when the nozzle location is at (Figure 6). The number of extrusive particles increases steadily from 0.25 s to 0.50 s but increases slowly when the nozzle position is at , indicating that the feeding and injecting masses are balanced. The number of extrusive particles tends to decline after 0.55 s and then declines sharply from 0.58 s to 0.62 s. This is the same trend observed in Figure 3 for a nozzle position of . The number of extrusive particles increases slightly after 0.70 s. However, this does not appear when the nozzle position is . The number of remaining particles in the four models is clearly different from each other; the number of remaining particles in the PTM is less than that for the other three models for a nozzle position of (Figure 7). After 0.5 s, the material feed stops and the number of extrusive particles linearly decreases in all of the models.
The simulation results show that the number of extrusive particles is maximised when the nozzle is positioned at , indicating that the injection performance is very good and the number of remaining particles is then minimised. However, the particle-wall collisions are a significant issue in the delivery pipe. The linearity of particle trajectories is better and fewer particle-wall collisions are observed compared to that for the other three models for a nozzle location of . However, the particle trajectories are complex and the number of remaining particles is maximised. Consequently, a nozzle location of is chosen for the gas-solid injector test-bed to verify the simulation results regarding the injection performance.
The experimental results show that nozzle location is the key factor that influences the injection performance, especially the injection mass. The injection mass increases first and then decreases as the nozzle position moves from left to right (or from A to I), indicating that there is an optimum nozzle position and thus verifying the simulation.
When the nozzle was in position A, the jet gas flow caused serious impacts, leading to significant noise and resulted in little mass being ejected. The material erupted in reverse from the hopper and blocked the mixing chamber during continuous feeding.
When the nozzle was in position D, the injection mass was maximised and the average maximum injection mass was 3.497 m3/h with a peak injection mass of 3.66 m3/h. These injection masses were determined to have met the requirements for the engineering application.
When the nozzle was in position I, the injection air did not mix with the material. Only a small amount of material was ejected out the mixing chamber and most of the material did not leave the hopper.
Due to the limitations of the experimental conditions, this paper only addresses the injection performance from the view of the nozzle position. There are other parameters that influence the injection properties of a gas-solid injector that are not examined here, such as the geometric construction of the mixing chamber, the wall conditions, and the material properties. Future studies are expected to examine these aspects.
Based on the theoretical analysis, the conclusions obtained from the simulation and experimental studies regarding key factors that affect the injector performance are as follows:(1)The nozzle location is the key factor affecting the gas-solid injector performance. There is an optimal nozzle location at which the number of extrusive particles is maximised and the number of particles remaining in the hopper is minimised.(2)The simulation results indicate that injection performance peaks when the nozzle is positioned at 30 mm. However, the particle-wall and particle-particle collisions are more intense in the delivery pipe at this nozzle position. The particle trajectories are more linear and the particle-wall collisions decrease for a nozzle position of 90 mm. The particle trajectories at this nozzle position are more complicated, and the greatest amount of remaining particles in the hopper is observed for this nozzle position.(3)The results of the experimental study indicate that the nozzle location has a clear influence on the injection performance. The injection performance improves remarkably in the optimum nozzle position of the gas-solid injector when the structural parameters do not change.
Conflict of Interests
The authors declare that there is no conflict of interests regarding the publication of this paper.
This project is supported by National High-Tech Research and Development Program of China (863 Program) (no. 2012AA062102), the Graduate Student Innovation Training Project in Jiangsu Province (nos. KYLX_1379 and CXLX13_936), and the Priority Academic Program Development of Jiangsu Higher Education Institutions.
W.-Y. Yu, R. Tian, and S.-Y. Yan, “Numerical simulation on the flow structure and performance of the ejector,” Journal of Engineering Thermophysics, vol. 33, no. 11, pp. 1881–1883, 2012.View at: Google Scholar
Z. G. Feng, E. E. Michaelides, and S. L. Mao, “Simulation of particle-wall collisions in a viscous fluid using a resolved discrete particle method,” in Proceedings of the Asme Fluids Engineering Division Summer Conference, vol. 1, pp. 57–62, 2010.View at: Google Scholar
Y.-Q. Xiong and M.-Y. Zhang, “Experimental study on static pressure distribution properties of gas-solid injector under pressure,” Journal of Combustion Science and Technology, vol. 10, no. 2, pp. 130–134, 2004.View at: Google Scholar
Y.-Q. Xiong, M.-Y. Zhang, Z.-L. Yuan, and D.-M. Xue, “Three-dimensional numerical simulation on gas-solid two-phase flows in gas-solid injector,” Proceedings of the Chinese Society of Electrical Engineering, vol. 25, no. 20, pp. 77–82, 2005.View at: Google Scholar
Y. Q. Xiong, Z. L. Yuan, and M. Y. Zhang, “Three-dimensional numerical simulation on conveying properties of gas-solid injector under pressurization,” Journal of Chemical Industry and Engineering, vol. 10, no. 55, pp. 1638–1643, 2004.View at: Google Scholar
Z. C. Zheng, X. Y. Zou, X. F. Yang, and H. Cheng, “Simulation of effects of the Saffman force and the Magnus force on sand saltation in turbulent flow,” in Proceedings of the ASME International Mechanical Engineering Congress and Exposition (IMECE '11), vol. 6, pp. 501–506, Denver, Colo, USA, November 2011.View at: Google Scholar
Z. Zhu and J. Lin, “Pressure gradient force, saffman lift, and magnus lift on the fiber-like particle in fluid,” Journal of Dong Hua University, vol. 17, no. 2, pp. 23–27, 2000.View at: Google Scholar
Q. Li, V. Rudolph, F. Y. Wang, and M. Horio, “A study of particle packing compression under fluid drag force by DEM simulations,” Developments in Chemical Engineering and Mineral Processing, vol. 13, no. 5-6, pp. 693–708, 2005.View at: Google Scholar