# Study on the Influence of Processing Parameters on Piercing Extrusion Process of Large Diameter Cupronickel Alloy Pipes Using 3D FEM Analysis

Authors: Jun Cai; Kuaishe Wang; Bing Zhang; Wen Wang
Journal: Advances in Materials Science and Engineering
 (2017)

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## Abstract

With the rapid development of the shipping and the power industry, the demand for high-performance cupronickel alloy pipes is greatly increasing. The main processing methods of this alloy include semisolid ingot casting and deformation by hot extrusion. Many defects appear during the hot extrusion process for large diameter cupronickel alloy pipes, which results in considerable problems. Therefore, numerical simulation of hot extrusion for cupronickel alloy pipes before the practical production is of vital significance to properly determine the deformation parameters. In order to obtain the influence of processing parameters on the piercing extrusion process of large diameter cupronickel alloy pipe, metal flowing law under different deformation conditions was simulated and analyzed via employing a 3D FEM code. The results showed that piercing speed had no obvious influence on the cupronickel alloy billet. However, the friction had significant influence on the piercing process of cupronickel alloy billet: with the increase of friction coefficient, the temperature and the load increased.


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## Body

## 1. Introduction

Nowadays, the demand for the high-performance cupronickel alloy pipes is greatly increasing due to the rapid development shipping, power, and sea water desalination industry [1]. Cupronickel alloys have an attractive combination of characteristics in terms of their resistance to corrosion and biofouling, which make them an ideal choice for severely corrosive environments, in particular when a great thermal conductivity is needed [2, 3]. Hot extrusion is the main deformation method for large diameter cupronickel alloy pipes [4]. However, various defects such as overload (Figure 1(a)) and die crack (Figure 1(b)) can be often found during the hot extrusion process of large diameter pipes, which results in considerable problems, such as long process times, high energy consumption, low product yield, and high cost [5]. Therefore, numerical simulation for hot extrusion process of large diameter cupronickel alloy pipes before the practical production is significant to properly design the deformation parameters.Figure 1
Defect of large diameter cupronickel alloy pipes during hot extrusion: (a) overload; (b) die crack.
(a)
(b)The producing process of cupronickel alloy pipes includes transportation from furnace→ upsetting of casting ingots → piercing process → hot extrusion. The piercing process is an important processing step that affects temperature distribution and the movement of material and, consequently, the mechanical properties of the pipes. Therefore, the objective of this research is to investigate the influence of processing parameters on piercing extrusion process of large diameter cupronickel alloy pipe. Toward this end, the finite element package DEFORM 3D is used to simulate the heat transfer during the transportation process and the following piercing extrusion process. The influence of processing parameters on piercing extrusion process of large diameter cupronickel alloy pipe was analyzed from the simulation results.


## 2. FEM Simulation Model

The components of the piercing extrusion die included four parts, piercing mandrel, dummy block, container, and blanking plate, as shown in Figure2. The billet was cylindrical solid ingot, with a diameter of 440 mm and a length of 420 mm. Half of the die components and billet are taken as the case to establish 3D FEM model because of their bilateral symmetry structure.Figure 2
Structure components of a piercing extrusion die.The workpiece material is BFe10-1-2 cupronickel alloy, and its material model is given as follows [6]:(1)σ=67.5+88.154ε0.4836exp⁡-0.00315+0.00117εT-1073+0.0768+0.000189T-1073ln⁡ε˙,where σ is the flow stress (MPa), ε is true strain, ε˙ is strain rate in s−1, and T is the deformation temperature (K).The die material is H13 hot work die steel. The initial temperature of piercing mandrel and dummy block is 400°C, and the initial temperatures of container, blanking plate, and billet are 400°C, 200°C, and 950°C, respectively. Meanwhile, the temperature of ambient environment is regarded as 20°C. The piercing speeds are 50, 80, and 100 mm/s, and the friction coefficients are taken to be 0.3, 0.5, and 0.7.


## 3. Results and Discussion

### 3.1. Heat Transfer Process

Quadrilateral grids are employed to establish the mesh generation of die and billet mesh, and the elements number of billet is 37431, as shown in Figures3 and 4. Lagrangian incremental method is used to solve the deformation simulation. Die displacement is introduced to define the solution step for dynamic analysis, and the step increment is chosen as 3 mm/step (lower than 1/3 of minimum side length of the mesh). The heat transfer process consists of two stages: (1) contact and convective heat transfer during the transportation process of billet from furnace to extruder (shown in Figure 3) and (2) contact heat transfer between billet and dies in container before the beginning of upsetting process (shown in Figure 4).Figure 3
Diagram of transportation of billet from furnace to extruder.Figure 4
Diagram of heat transfer between billet and dies.The heat transfer time of the first stage is about 45 s, and the temperature distribution of billet is given in Figure5(a). It can be seen from the figure that the temperature decrease appears only at the surface of billet, and temperature in the center region keeps the initial temperature of 950°C. The minimum temperature is exhibited in the position of contacting with conveyance (lower than 800°C). The time of the second heat transfer stage is about 15 s, and the distribution of temperature field for billet is illustrated in Figure 5(b). It can be seen from the figure that the maximum temperature is exhibited in the center region of deformation billet and maintains 950°C.Figure 5
Distribution of temperature field of billet: (a) the first stage (b) the second stage.
(a)
(b)


### 3.2. Upsetting Process

Figure6 exhibits the mesh graph of billet before and after upsetting process. The piercing mandrel and dummy block move forward about 20 mm for the purpose of filling the container. As can be seen from Figure 7, there exists obvious clearance between the billet and the upper part of container (red arrows in Figure 6(b)).Figure 6
Mesh graph of billet (a) before and (b) after upsetting process.
(a)
(b)Figure 7
Distribution of temperature field of billet after upsetting.
(a)
(b)The temperature distribution of billet after upsetting process is illustrated in Figure7. It can be found that the maximum temperature is still located in the center region of billet and keeps initial temperature of 950°C. The minimum temperature appears at the contact position with blanking plate (black arrow). Obvious temperature decrease exists in some bottom region of billet (red arrow in Figure 7), while outer side region of billet is still higher than 800°C (blue arrow). Therefore, only a small part of billet has contacted with container.


### 3.3. Piercing Extrusion Process

After upsetting process, the piercing mandrel moves forward to start piercing process, and the total stroke of piercing mandrel is about 360 mm. During the simulation process, remeshing procedure can be automatically carried out by the DEFORM 3D software on the basis of mesh deformation. Figure8 shows the shape variation with different stock of 90 mm, 180 mm, 270 mm, and 360 mm. As can be seen from figures, there exists obvious between billet top and container at the initial stage of piercing process (red arrows in Figures 8(a) and 8(b)). Then, with the increase of deformation, the clearance gradually disappears, as shown in Figures 8(c) and 8(d).Figure 8
Piercing extrusion process at (a) 90 mm, (b) 180 mm, (c) 270 mm, and (d) 360 mm.
(a)
(b)
(c)
(d)


#### 3.3.1. Effect of Speed on the Piercing Result

Figure9 illustrates the temperature distribution of billet at various piercing speeds with the friction coefficient of 0.3. The minimum temperature is exhibited at the contact position with blanking plate (red arrow in Figure 9(a)) and is lower than 500°C. Meanwhile, the maximum temperature is higher than 950°C, which can be attributed to the inner heat generated by the plastic deformation. Moreover, the maximum temperature is located in middle of the extruded billet, which is higher than that on the surface, as shown in Figure 9. Similar distribution was also reported by Guo et al. [7] in needle piercing extrusion of AISI304 stainless steel pipe.Figure 9
Temperature distribution of billet deformed at the piercing speed of (a) 50 mm/s, (b) 80 mm/s, and (c) 100 mm/s.
(a)
(b)
(c)It should be noted that the temperature field of billets at various piercing speeds shows similar distribution. This may be accounted for the fact that the piercing speed is high (even at 50 mm/s), resulting in the similar distribution of temperature field.The strain field distribution of billet at various piercing speeds is given in Figure10. It can be seen from the figure that there is no significant difference among the billets. High-strain region is located at the position of contacting with piercing mandrel.Figure 10
Strain field distribution of billet deformed at the piercing speed of (a) 50 mm/s, (b) 80 mm/s, and (c) 100 mm/s.
(a)
(b)
(c)The stress field distribution of billet at various piercing speeds is shown in Figure11. As can be seen from the figure, the stress field exhibits similar distribution at different piercing speeds. The maximum stress is located at the position of contacting with blanking plate (about 200 MPa).Figure 11
Stress field distribution of billet deformed at the piercing speed of (a) 50 mm/s, (b) 80 mm/s, and (c) 100 mm/s.
(a)
(b)
(c)The load-stroke curves at three piercing speeds are plotted in Figure12. As shown in Figure 12, a steep increase in the piercing load takes place at the final stage. Meanwhile, the piercing load at the speed of 50 mm/s is a little lower than that of the other two speeds. The load curves at the speed of 80 mm/s and 100 mm/s show little difference, and the loads at all piercing speeds are lower than the maximum capability of device (12 MN).Figure 12
Effect of deformation speed on the load-stroke curves.


#### 3.3.2. Effect of Friction on the Piercing Result

Figure13 shows the temperature distribution of billet at the friction coefficient of 0.5 and 0.7 (piercing speed of 100 mm/s). Compared with Figure 9(c), it can be seen from Figure 13 that the maximum temperature increases with the increase of the friction coefficient. Meanwhile, it can be seen from Figure 13(a) that there exists obvious bulge at the lower part of billet (red arrow), while the bulge is not obvious at the friction coefficient of 0.3 (shown in Figure 9). When the friction coefficient reaches 0.7, the bulge appears at both lower (red arrow) and upper (blue arrow) parts, as shown in Figure 13(b).Figure 13
Effect of friction on the temperature distribution of billet at the piercing speed of 100 mm/s with friction coefficient of (a) 0.5 and (b) 0.7.
(a)
(b)The strain field distribution of billet at various friction conditions is given in Figure14. It can be seen that there exists unclear difference among the billets (shown in Figures 10(c) and 14), which indicates that the friction has no significant influence on the strain.Figure 14
Strain field distribution of billet deformed at the friction coefficient of (a) 0.5 and (b) 0.7.
(a)
(b)The stress field distribution of billet at various friction conditions is given in Figure15. It can be seen that the maximum stress is still located at the position of contacting with blanking plate. However, the stress at the flank of billet increases quickly with the increase of friction. Therefore, friction has obvious influence on the stress field.Figure 15
Stress field distribution of billet deformed at the friction coefficient of (a) 0.5 and (b) 0.7.
(a)
(b)The load-stroke curves at the piercing speeds of 100 mm/s with the friction coefficient of 0.3, 0.5, and 0.7 are given in Figure16. It is clear that friction has significant influence on the loads. With the increase of friction, the load increases sharply. The maximum load of friction coefficient of 0.7 is much higher than 12 MN, which indicates that the cupronickel alloy pipes could not be produced under this deformation condition. Meanwhile, the real product of large diameter cupronickel alloy pipes is given in Figure 17.Figure 16
Effect of friction on the load-stroke curves.Figure 17
Simulation result of billet deformed with the elements number of 30787: (a) strain; (b) stress.
(a)
(b)In order to investigate the effect of mesh convergence on the simulation results, different elements numbers (i.e., various mesh size) are introduced to repeat the simulation process. Figure17 is the stain field and stress field distribution of billet deformed at the piercing speed of 50 mm/s with the elements number of 30787 (smaller mesh size), and Figure 18 gives the simulation result with the elements number of 40177 (larger mesh size). It can be seen from Figures 17(a) and 18(a) that the strain field distribution is very similar to that of Figure 10(a). Meanwhile, mesh size has no obvious influence on the stress field distribution of billet, as shown in Figures 11(a), 17(b), and 18(b). Table 1 shows the effect of the elements number on the maximum load. It can be found from the table that the elements number has also small influence on the maximum load. Meanwhile, the real product of large diameter cupronickel alloy pipes is given in Figure 19.Table 1
Effect of the elements number on the maximum load.
Elements number
30787
37431
40177
Max load/MN
8.28
8.20
8.13Figure 18
Simulation result of billet deformed with the elements number of 40177: (a) strain; (b) stress.
(a)
(b)Figure 19
Real product of large diameter cupronickel alloy pipes.


## 3.1. Heat Transfer Process

Quadrilateral grids are employed to establish the mesh generation of die and billet mesh, and the elements number of billet is 37431, as shown in Figures3 and 4. Lagrangian incremental method is used to solve the deformation simulation. Die displacement is introduced to define the solution step for dynamic analysis, and the step increment is chosen as 3 mm/step (lower than 1/3 of minimum side length of the mesh). The heat transfer process consists of two stages: (1) contact and convective heat transfer during the transportation process of billet from furnace to extruder (shown in Figure 3) and (2) contact heat transfer between billet and dies in container before the beginning of upsetting process (shown in Figure 4).Figure 3
Diagram of transportation of billet from furnace to extruder.Figure 4
Diagram of heat transfer between billet and dies.The heat transfer time of the first stage is about 45 s, and the temperature distribution of billet is given in Figure5(a). It can be seen from the figure that the temperature decrease appears only at the surface of billet, and temperature in the center region keeps the initial temperature of 950°C. The minimum temperature is exhibited in the position of contacting with conveyance (lower than 800°C). The time of the second heat transfer stage is about 15 s, and the distribution of temperature field for billet is illustrated in Figure 5(b). It can be seen from the figure that the maximum temperature is exhibited in the center region of deformation billet and maintains 950°C.Figure 5
Distribution of temperature field of billet: (a) the first stage (b) the second stage.
(a)
(b)


## 3.2. Upsetting Process

Figure6 exhibits the mesh graph of billet before and after upsetting process. The piercing mandrel and dummy block move forward about 20 mm for the purpose of filling the container. As can be seen from Figure 7, there exists obvious clearance between the billet and the upper part of container (red arrows in Figure 6(b)).Figure 6
Mesh graph of billet (a) before and (b) after upsetting process.
(a)
(b)Figure 7
Distribution of temperature field of billet after upsetting.
(a)
(b)The temperature distribution of billet after upsetting process is illustrated in Figure7. It can be found that the maximum temperature is still located in the center region of billet and keeps initial temperature of 950°C. The minimum temperature appears at the contact position with blanking plate (black arrow). Obvious temperature decrease exists in some bottom region of billet (red arrow in Figure 7), while outer side region of billet is still higher than 800°C (blue arrow). Therefore, only a small part of billet has contacted with container.


## 3.3. Piercing Extrusion Process

After upsetting process, the piercing mandrel moves forward to start piercing process, and the total stroke of piercing mandrel is about 360 mm. During the simulation process, remeshing procedure can be automatically carried out by the DEFORM 3D software on the basis of mesh deformation. Figure8 shows the shape variation with different stock of 90 mm, 180 mm, 270 mm, and 360 mm. As can be seen from figures, there exists obvious between billet top and container at the initial stage of piercing process (red arrows in Figures 8(a) and 8(b)). Then, with the increase of deformation, the clearance gradually disappears, as shown in Figures 8(c) and 8(d).Figure 8
Piercing extrusion process at (a) 90 mm, (b) 180 mm, (c) 270 mm, and (d) 360 mm.
(a)
(b)
(c)
(d)


### 3.3.1. Effect of Speed on the Piercing Result

Figure9 illustrates the temperature distribution of billet at various piercing speeds with the friction coefficient of 0.3. The minimum temperature is exhibited at the contact position with blanking plate (red arrow in Figure 9(a)) and is lower than 500°C. Meanwhile, the maximum temperature is higher than 950°C, which can be attributed to the inner heat generated by the plastic deformation. Moreover, the maximum temperature is located in middle of the extruded billet, which is higher than that on the surface, as shown in Figure 9. Similar distribution was also reported by Guo et al. [7] in needle piercing extrusion of AISI304 stainless steel pipe.Figure 9
Temperature distribution of billet deformed at the piercing speed of (a) 50 mm/s, (b) 80 mm/s, and (c) 100 mm/s.
(a)
(b)
(c)It should be noted that the temperature field of billets at various piercing speeds shows similar distribution. This may be accounted for the fact that the piercing speed is high (even at 50 mm/s), resulting in the similar distribution of temperature field.The strain field distribution of billet at various piercing speeds is given in Figure10. It can be seen from the figure that there is no significant difference among the billets. High-strain region is located at the position of contacting with piercing mandrel.Figure 10
Strain field distribution of billet deformed at the piercing speed of (a) 50 mm/s, (b) 80 mm/s, and (c) 100 mm/s.
(a)
(b)
(c)The stress field distribution of billet at various piercing speeds is shown in Figure11. As can be seen from the figure, the stress field exhibits similar distribution at different piercing speeds. The maximum stress is located at the position of contacting with blanking plate (about 200 MPa).Figure 11
Stress field distribution of billet deformed at the piercing speed of (a) 50 mm/s, (b) 80 mm/s, and (c) 100 mm/s.
(a)
(b)
(c)The load-stroke curves at three piercing speeds are plotted in Figure12. As shown in Figure 12, a steep increase in the piercing load takes place at the final stage. Meanwhile, the piercing load at the speed of 50 mm/s is a little lower than that of the other two speeds. The load curves at the speed of 80 mm/s and 100 mm/s show little difference, and the loads at all piercing speeds are lower than the maximum capability of device (12 MN).Figure 12
Effect of deformation speed on the load-stroke curves.


### 3.3.2. Effect of Friction on the Piercing Result

Figure13 shows the temperature distribution of billet at the friction coefficient of 0.5 and 0.7 (piercing speed of 100 mm/s). Compared with Figure 9(c), it can be seen from Figure 13 that the maximum temperature increases with the increase of the friction coefficient. Meanwhile, it can be seen from Figure 13(a) that there exists obvious bulge at the lower part of billet (red arrow), while the bulge is not obvious at the friction coefficient of 0.3 (shown in Figure 9). When the friction coefficient reaches 0.7, the bulge appears at both lower (red arrow) and upper (blue arrow) parts, as shown in Figure 13(b).Figure 13
Effect of friction on the temperature distribution of billet at the piercing speed of 100 mm/s with friction coefficient of (a) 0.5 and (b) 0.7.
(a)
(b)The strain field distribution of billet at various friction conditions is given in Figure14. It can be seen that there exists unclear difference among the billets (shown in Figures 10(c) and 14), which indicates that the friction has no significant influence on the strain.Figure 14
Strain field distribution of billet deformed at the friction coefficient of (a) 0.5 and (b) 0.7.
(a)
(b)The stress field distribution of billet at various friction conditions is given in Figure15. It can be seen that the maximum stress is still located at the position of contacting with blanking plate. However, the stress at the flank of billet increases quickly with the increase of friction. Therefore, friction has obvious influence on the stress field.Figure 15
Stress field distribution of billet deformed at the friction coefficient of (a) 0.5 and (b) 0.7.
(a)
(b)The load-stroke curves at the piercing speeds of 100 mm/s with the friction coefficient of 0.3, 0.5, and 0.7 are given in Figure16. It is clear that friction has significant influence on the loads. With the increase of friction, the load increases sharply. The maximum load of friction coefficient of 0.7 is much higher than 12 MN, which indicates that the cupronickel alloy pipes could not be produced under this deformation condition. Meanwhile, the real product of large diameter cupronickel alloy pipes is given in Figure 17.Figure 16
Effect of friction on the load-stroke curves.Figure 17
Simulation result of billet deformed with the elements number of 30787: (a) strain; (b) stress.
(a)
(b)In order to investigate the effect of mesh convergence on the simulation results, different elements numbers (i.e., various mesh size) are introduced to repeat the simulation process. Figure17 is the stain field and stress field distribution of billet deformed at the piercing speed of 50 mm/s with the elements number of 30787 (smaller mesh size), and Figure 18 gives the simulation result with the elements number of 40177 (larger mesh size). It can be seen from Figures 17(a) and 18(a) that the strain field distribution is very similar to that of Figure 10(a). Meanwhile, mesh size has no obvious influence on the stress field distribution of billet, as shown in Figures 11(a), 17(b), and 18(b). Table 1 shows the effect of the elements number on the maximum load. It can be found from the table that the elements number has also small influence on the maximum load. Meanwhile, the real product of large diameter cupronickel alloy pipes is given in Figure 19.Table 1
Effect of the elements number on the maximum load.
Elements number
30787
37431
40177
Max load/MN
8.28
8.20
8.13Figure 18
Simulation result of billet deformed with the elements number of 40177: (a) strain; (b) stress.
(a)
(b)Figure 19
Real product of large diameter cupronickel alloy pipes.


## 3.3.1. Effect of Speed on the Piercing Result

Figure9 illustrates the temperature distribution of billet at various piercing speeds with the friction coefficient of 0.3. The minimum temperature is exhibited at the contact position with blanking plate (red arrow in Figure 9(a)) and is lower than 500°C. Meanwhile, the maximum temperature is higher than 950°C, which can be attributed to the inner heat generated by the plastic deformation. Moreover, the maximum temperature is located in middle of the extruded billet, which is higher than that on the surface, as shown in Figure 9. Similar distribution was also reported by Guo et al. [7] in needle piercing extrusion of AISI304 stainless steel pipe.Figure 9
Temperature distribution of billet deformed at the piercing speed of (a) 50 mm/s, (b) 80 mm/s, and (c) 100 mm/s.
(a)
(b)
(c)It should be noted that the temperature field of billets at various piercing speeds shows similar distribution. This may be accounted for the fact that the piercing speed is high (even at 50 mm/s), resulting in the similar distribution of temperature field.The strain field distribution of billet at various piercing speeds is given in Figure10. It can be seen from the figure that there is no significant difference among the billets. High-strain region is located at the position of contacting with piercing mandrel.Figure 10
Strain field distribution of billet deformed at the piercing speed of (a) 50 mm/s, (b) 80 mm/s, and (c) 100 mm/s.
(a)
(b)
(c)The stress field distribution of billet at various piercing speeds is shown in Figure11. As can be seen from the figure, the stress field exhibits similar distribution at different piercing speeds. The maximum stress is located at the position of contacting with blanking plate (about 200 MPa).Figure 11
Stress field distribution of billet deformed at the piercing speed of (a) 50 mm/s, (b) 80 mm/s, and (c) 100 mm/s.
(a)
(b)
(c)The load-stroke curves at three piercing speeds are plotted in Figure12. As shown in Figure 12, a steep increase in the piercing load takes place at the final stage. Meanwhile, the piercing load at the speed of 50 mm/s is a little lower than that of the other two speeds. The load curves at the speed of 80 mm/s and 100 mm/s show little difference, and the loads at all piercing speeds are lower than the maximum capability of device (12 MN).Figure 12
Effect of deformation speed on the load-stroke curves.


## 3.3.2. Effect of Friction on the Piercing Result

Figure13 shows the temperature distribution of billet at the friction coefficient of 0.5 and 0.7 (piercing speed of 100 mm/s). Compared with Figure 9(c), it can be seen from Figure 13 that the maximum temperature increases with the increase of the friction coefficient. Meanwhile, it can be seen from Figure 13(a) that there exists obvious bulge at the lower part of billet (red arrow), while the bulge is not obvious at the friction coefficient of 0.3 (shown in Figure 9). When the friction coefficient reaches 0.7, the bulge appears at both lower (red arrow) and upper (blue arrow) parts, as shown in Figure 13(b).Figure 13
Effect of friction on the temperature distribution of billet at the piercing speed of 100 mm/s with friction coefficient of (a) 0.5 and (b) 0.7.
(a)
(b)The strain field distribution of billet at various friction conditions is given in Figure14. It can be seen that there exists unclear difference among the billets (shown in Figures 10(c) and 14), which indicates that the friction has no significant influence on the strain.Figure 14
Strain field distribution of billet deformed at the friction coefficient of (a) 0.5 and (b) 0.7.
(a)
(b)The stress field distribution of billet at various friction conditions is given in Figure15. It can be seen that the maximum stress is still located at the position of contacting with blanking plate. However, the stress at the flank of billet increases quickly with the increase of friction. Therefore, friction has obvious influence on the stress field.Figure 15
Stress field distribution of billet deformed at the friction coefficient of (a) 0.5 and (b) 0.7.
(a)
(b)The load-stroke curves at the piercing speeds of 100 mm/s with the friction coefficient of 0.3, 0.5, and 0.7 are given in Figure16. It is clear that friction has significant influence on the loads. With the increase of friction, the load increases sharply. The maximum load of friction coefficient of 0.7 is much higher than 12 MN, which indicates that the cupronickel alloy pipes could not be produced under this deformation condition. Meanwhile, the real product of large diameter cupronickel alloy pipes is given in Figure 17.Figure 16
Effect of friction on the load-stroke curves.Figure 17
Simulation result of billet deformed with the elements number of 30787: (a) strain; (b) stress.
(a)
(b)In order to investigate the effect of mesh convergence on the simulation results, different elements numbers (i.e., various mesh size) are introduced to repeat the simulation process. Figure17 is the stain field and stress field distribution of billet deformed at the piercing speed of 50 mm/s with the elements number of 30787 (smaller mesh size), and Figure 18 gives the simulation result with the elements number of 40177 (larger mesh size). It can be seen from Figures 17(a) and 18(a) that the strain field distribution is very similar to that of Figure 10(a). Meanwhile, mesh size has no obvious influence on the stress field distribution of billet, as shown in Figures 11(a), 17(b), and 18(b). Table 1 shows the effect of the elements number on the maximum load. It can be found from the table that the elements number has also small influence on the maximum load. Meanwhile, the real product of large diameter cupronickel alloy pipes is given in Figure 19.Table 1
Effect of the elements number on the maximum load.
Elements number
30787
37431
40177
Max load/MN
8.28
8.20
8.13Figure 18
Simulation result of billet deformed with the elements number of 40177: (a) strain; (b) stress.
(a)
(b)Figure 19
Real product of large diameter cupronickel alloy pipes.


## 4. Conclusions

The piercing extrusion process of large diameter cupronickel alloy pipe at different piercing speeds and friction coefficient was simulated by using a 3D FEM code. The following conclusions are obtained:(1)
Temperature in the center region of billet keeps the initial temperature after transportation and upsetting process.(2)
Piercing speed has no obvious influence on the temperature field, strain field, stress field, and the load-stroke curves.(3)
Friction has significant influence on the billet. With the increase of friction coefficient, the maximum temperature of billet increases, and the load increases sharply.



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*Source: 8329048-2017-03-02.xml*