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Numerical simulation of nickel-based alloys’ welding transient stress using various cooling techniques

  • Meng He , Jianing Qi , Zhentai Zheng EMAIL logo , Fen Shi and Yunfeng Lei
Published/Copyright: December 5, 2020
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High Temperature Materials and Processes
From the journal High Temperature Materials and Processes Volume 39 Issue 1

Abstract

Nickel-based alloys play an important role in the field of high-temperature alloys, which are widely used in nuclear reactors, aerospace and components of turbomachinery. However, the high susceptibility of welding hot crack is a main shortcoming to nickel-based alloys. One of the methods that reduce hot cracking susceptibility is by adjusting element constitution of weld metal and another method is by reducing transient stress. This article used finite element method to study the effect of cooling source on transient stress of the nickel-based alloy weld joint. The selection of appropriate cooling technique can decrease the peak of the transient von Mises stress and make the tensile stress turn into compressive stress, which is beneficial to reduce hot cracking susceptibility. The peak of the transient von Mises stress decreases as the cooling intensity increases from 0 to 15,000 W/m2 K, but increases if the cooling intensity is ineffective. When the distance between cooling source and heat source reaches 35 mm, the weld can get larger region of compressive stress. The peak of the transient von Mises stress decreases with increasing radius of cooling source and reaches minimum value at 12 mm. Combined cooling is more effective in reducing the peak of this stress than the conventional single trailing cooling source.

Keywords: nickel-based alloys; hot cracking susceptibility; rapid cooling; finite element method; transient stress

1 Introduction

Nickel-based alloys are the most widely used superalloys for the applications requiring heat and corrosion resistance such as nuclear reactors, aerospace and components of turbomachinery. However, it has higher hot cracking susceptibility than carbon steel and stainless steel during welding. It is generally known that one of the cracking mechanisms in fusion zone (FZ) and heat affected zone (HAZ) is the low melting point eutectic formed by the segregation of alloying elements, and another important mechanism is the mechanical tensile stresses generated in the welding process. Because of the drastic change of temperature and stress in the welding process, the liquation film and low ductility metal in FZ and HAZ are stretched beyond their plastic strain range by tensile stresses, leading to the formation of hot cracks. Hence, there are two ways to reduce hot cracking susceptibility: adjusting weld metal compositions and reducing the tensile stresses of welding joint. Furthermore, the welding hot cracks of nickel-based alloy are caused during the cooling process of weld, and the residual stress appears on weld after the cooling process. Therefore, the peak value and distribution of the residual stress have no effect on hot cracks. This means that transient stress in the welding process is very essential to reduce hot cracking susceptibility but not the residual stress.

Ren et al. [1] found that the continuous (Cr, Mo)-rich phase decreased as the heat input and preheating temperature increased in the fiber laser welding of Inconel 617. Vishwakarma and Chaturvedi [2] revealed that the HAZ grain boundary liquation of Allvac 718 Plus was caused by the segregation of the minor alloying elements of Saida et al. [3] have reported that ductility dip cracking in multilayer weld metal of alloy 690 can be attributed to grain boundary segregation of P and S. Mo et al. [4] found that boron segregated at grain boundaries in NiCrFe-7 weld metal, and the boron promoted the formation of continuous M23(C, B)6 carbide chains and M2B borides along grain boundaries, which causes more ductility-dip-cracking (DDC) in the weld metal. Osoba et al. [5] studied microstructures of Haynes 282 nickel-based alloys with laser welding and found that carbon has inhibitory effect on the formation of eutectic γ–γ′, which results in solidification cracking. Ramirez and Lippold [6] found that C, Nb and Ti can form bending grain boundaries when enough medium size (Nb,Ti)C eutectic phase is generated. Such boundaries were less prone to sliding and were beneficial to resist DDC cracking. Chamanfar et al. [7] found that the segregation and γ′ dissolution in FZ and HAZ are the mechanisms for cracking.

It is obvious that most of those researchers paid more attention to the effect of alloying element on the hot cracking sensitivity of nickel-based weld alloy. However, adjusting alloying element can only reduce the hot cracking susceptibility of weld and cannot reduce the hot cracking susceptibility of HAZ. Therefore, it is necessary to take appropriate measures to reduce the hot cracking susceptibility of weld and HAZ by reducing transient stress at the same time. Cooling technique is regarded as an effective method to achieve this goal.

Manikandan et al. [8] found that the enhanced cooling rate with liquid nitrogen reduced the interdendritic phases, and the dendrite arm spacing was reduced from the range of 15–54 to 3–17 µm during the gas tungsten arc welding (GTAW) process. Jiang et al. [9] found that the heat sink technology can decrease the residual stress greatly, and with the average heat transfer coefficient increase, the transverse stress is decreased greatly. Transverse tensile stresses have been changed to compressive in some zones. Yegaie et al. [10] found that the heat sink can limit the high-temperature region to the vicinity of heat source and decrease the maximum temperature of the sample, which result in lower residual stresses and even compressive stresses near the weld zone. Li et al. [11,12] further studied the effect of distance between cooling source and heat source on residual stress by controlled low stress non-deformation technique and found that there exists an appropriate distance in which the residual stress and plastic strain were both well controlled. Kala et al. [13], Zhang et al. [14] and Bajpei et al. [15] also studied the effect of cooling source on residual stress and deformation using different materials with various coolants.

In the previous research studies, most of the researchers paid attention to the effect of cooling technique on the residual stress and ignored the effect of cooling technique on transient stress. However, transient stress plays an important role in reducing the hot cracking sensitivity of nickel-based weld but not residual stress. Therefore, in this study, the effect of cooling technique in reducing the transient stress and playing down the hot crack sensitivity of nickel-based weld is discussed.

2 Finite element model

A three-dimensional finite element model was developed by ANSYS to simulate the transient stress in the process of welding with rapid cooling. First, thermal analysis was performed to calculate the temperature histories. Then the temperature results were applied to the mechanical model to simulate the transient stress by the indirect coupling method.

2.1 Finite element mesh

Nicrofer 6023H (i.e., UNS N06601) sheets were butt welded together with the dimension of 100 mm × 60 mm × 4 mm. The weldments were symmetrical from weld center line; so only half of the sheets were selected as a simulation model to reduce the calculation cost. In total, 17,697 nodes and 11,891 elements were meshed. Solid70 and solid90 were selected as element types and used for temperature field analysis in different areas. Because the weld metal changed drastically in the actual welding process, a finer mesh with length 1 mm was used in the finite element model in weld zone, and the element size increased gradually from weld center line to the edge of sheet. The finite element mesh is shown in Figure 1.

Figure 1 Finite element mesh.
Figure 1

Finite element mesh.

2.2 Material properties

The solidus temperature of Nicrofer 6023H is 1,320°C and the liquidus temperature is 1,370°C. The temperature-dependent physical properties and mechanical properties referenced to the specifications of Nicrofer 6023H published by ThyssenKrupp VDM. Because the specifications published by ThyssenKrupp VDM can only provide thermal and physical properties, mechanical parameters in the temperature range are lower than melting point and the parameters in high temperature are difficult to obtain, an extrapolation method was used to define a reference value when the temperature was higher than the melting point. Furthermore, the finite element model in this article only took the latent heat of fusion and solidification into consideration.

2.3 Heat source and heat dispersion model

In thermal analysis, a moving heat source based on the double ellipsoidal heat source model proposed by Goldak et al. [16] and Goldak and Akhlaghi [17] was applied to simulate the heat provided by welding torch in the GTAW process. The volumetric power density distribution of the front half is as follows:

(1)q(x,y,z)=63ffq0abcfππexp−3x2cf2−3y2a2−3z2b2.

The volumetric power density distribution of the rear half is as follows:

(2)q(x,y,z)=63fbq0abcbππexp−3x2cb2−3y2a2−3z2b2,

where a, b, cf and cb are the shape parameters that determine the size of weld pool, q0 is the effective heat input and ff and fb are the fractions of the heat deposited in the front and rear half where ff + fb = 2. Here it is assumed that ff is 0.6 and fb is 1.4. The number “3” is the actual heat flux distribution parameter, which characterizes the concentration level of heat flux distribution. The distribution of double ellipsoidal heat source model is shown in Figure 2.

Figure 2 Double ellipsoidal heat source model.
Figure 2

Double ellipsoidal heat source model.

Figure 3 shows the schematic diagram of GTAW with cooling source as an example of the rapid cooling technique in this article. Liquid nitrogen was selected as the coolant because (a) of high cooling efficiency and (b) nitrogen does not harm the nickel-based alloy weld. The liquid nitrogen was squeezed out from a container by a pneumatic device into a copper pipe, which is named cooling pipe. In position 1, the cooling pipe is located 10 mm above the surface of weldment parallel to the weld direction trailed with a welding torch. In position 2, the cooling pipe is below the surface of weldment parallel to the weld direction and 10 mm distant from the surface.

Figure 3 Schematic diagram of GTAW with trailing cooling source.
Figure 3

Schematic diagram of GTAW with trailing cooling source.

To simulate the rapid cooling effect in the finite element analysis, the average heat transfer coefficient was calculated by the following expression introduced by Martin [18]:

(3)h¯=kNu¯D,

where k is the thermal conductivity of liquid nitrogen, Nu¯ is the average Nusselt number and D is the equivalent cooling Pipe diameter. h¯ is applied as the condition of radiation over the nodes in which the cooling is applied.

2.4 Other heat boundary conditions and mechanical constraints

In thermal analysis, the ambient temperature was defined as 20°C, and the convection and radiation heat transfer coefficient, h, was applied to all surfaces except for square groove face, as well as over the surfaces exposed to heat and cooling sources. The convection and radiation heat transfer coefficient was given by the following equivalent expressions in total form introduced by Deng and Murakawa [19]:

(4)h=0.0668T0<T≤500°C,
(5)h=0.231T−82.1T>500°C.

It is important to select an appropriate set of displacement constraints. When the stress field was simulated, the rigid displacement of weldment must be limited to release the thermal strains which will slow down the convergence considerably. The welding situation changed with time irregularly, and so a nonlinear analysis was needed. In addition, the upper limit of the number of equilibrium iterations was increased, and a linear search was activated together with the Newton–Raphson method to ensure the convergence of whole stress field simulation process. For the purpose of avoiding stress concentration and making sure that there is no rigid displacement, the following constraints were used: area 3 is imposed on symmetry constraint, line 2 is constrained in the Z-direction and keypoint 1 is constrained in the X-direction as shown in Figure 4.

Figure 4 Constraints of mechanical model in simulation of welding transient stress.
Figure 4

Constraints of mechanical model in simulation of welding transient stress.

3 Model validation experiment

It is too difficult to measure the transient stress by instruments. Moreover, the transient stress is caused by temperature’s uneven distribution. In other words, the distribution of temperature determines the transient stress. Therefore, the simulated and experimental temperature histories were compared to validate the thermal model in this article. The corresponding experiment was carried out by a welding machine of Panasonic YC300WX N type and an automatic welding device. Two sheets of Nicrofer 6023H were placed on the welding platform with dimensions of 100 mm × 60 mm × 4 mm. The parameters of the welding process are summarized in Table 1.

Table 1

Parameters of Nicrofer 6023H GTAW process

ParametersValue
Arc voltage (V)12
Welding current (A)140
Welding speed (mm/s)2
Thermal efficiency0.7

Three K-type thermocouples were used as the temperature measurements and placed as shown in Figure 5. The temperature histories were recorded by a data acquisition instrument of TOPTEST TP99080324. As can be seen from Figure 6, the experimental temperature histories of point A (x = 30 mm, y = 10 mm and z = 2 mm), point B (x = 50 mm, y = 13 mm and z = 2 mm) and point C (x = 70 mm, y = 16 mm and z = 2 mm) agreed with the simulation results.

Figure 5 Schematic diagram of temperature measurement in the GTAW process.
Figure 5

Schematic diagram of temperature measurement in the GTAW process.

Figure 6 Comparison of experimental and simulated temperature histories in GTAW process: (a) point A; (b) point B and (c) point C.
Figure 6

Comparison of experimental and simulated temperature histories in GTAW process: (a) point A; (b) point B and (c) point C.

4 Results and discussion

In the welding of nickel-based alloys, alloy elements segregate in particular at grain boundaries and form low melting point phases such as eutectic γ–γ′, Laves phase and MC carbides along solidified grain boundaries. The presence of intergranular liquid films results in micro-fissure because the liquid films cannot withstand the thermal and mechanical tensile stresses in the GTAW process. Consequently, solidification cracking and liquation cracking occur by the solid–liquid interface separation in brittle temperature range (BTR), which is lower than the melting point of nickel-based alloys. It is one of the critical factors of high hot cracking susceptibility. Besides, there is a ductility dip temperature range (DTR) between solidus temperature (Ts) and 0.5Ts. The weld is in low ductility in this temperature range and easy to crack under tensile stresses, inducing the formation of DDC. The BTR and DTR are shown in Figure 7.

Figure 7 Schematic diagram of ductility as a function of temperature.
Figure 7

Schematic diagram of ductility as a function of temperature.

With the aim of investigating the effect of rapid cooling on hot cracking susceptibility in the nickel-based alloy weld, the transient von Mises stress in the temperature range of 1,350–550°C was discussed.

4.1 Effect of cooling intensity on transient stress

To analyze the effect of cooling intensity on GTAW temperature field, the temperature histories of the points x = 50 mm, y = 0 mm and z = 4 mm under different cooling intensities were investigated, and the results are shown in Figure 8. It is clearly shown that the node under cooling source undergoes two heating cycles. The heating cycle between 20 and 50 s was caused by the weld heating itself, and the other between 50 and 150 s was caused by the surrounding zones. The cooling source cannot decrease the maximum temperature, but can increase the cooling rate. The cooling rate was increased gradually with the cooling intensity, reaching a maximum at 15,000 W/m2 K, and then it was kept stable even if the cooling intensity increases to 20,000 W/m2 K.

Figure 8 Effect of cooling intensity on temperature histories.
Figure 8

Effect of cooling intensity on temperature histories.

The nickel-based alloys could be sensitized in 1,350–550°C, which will lead to the hot crack susceptibility of nickel-based alloys weld. It is very important to decrease the dwell time in 1,350–550°C. In the case of cooling with a cooling source, it took similar time to cool from 1,350 to 1,200°C compared to that without a cooling source, but it took less time to cool from 1,200 to 550°C when the cooling source was used. This means the dwell time around the BTR and the DTR decreases a lot. It is obviously shown that the cooling source is helpful in decreasing the risk of sensitization of the nickel-based alloy weld, leading to a decrease in the hot cracking susceptibility.

Figure 9 shows the temperature distributions and isotherms of conventional welding and welding with trailing cooling source when t = 30 s. It can be found that the high-temperature region was limited to the vicinity of heat source and a low-temperature zone formed in the weld. This indicates that lower hot stresses has form in the period of GTAW with trailing cooling source.

Figure 9 3D simulated temperature fields and isotherms of conventional GTAW and GTAW with trailing cooling source. (a) Temperature field of conventional welding; (b) temperature field of welding with trailing cooling source; (c) isotherms of conventional welding and (d) isotherms of welding with trailing cooling source.
Figure 9

3D simulated temperature fields and isotherms of conventional GTAW and GTAW with trailing cooling source. (a) Temperature field of conventional welding; (b) temperature field of welding with trailing cooling source; (c) isotherms of conventional welding and (d) isotherms of welding with trailing cooling source.

The simulated transient von Mises stress for different cooling intensities is shown in Figure 10. The transient von Mises stress had a little difference between the various cooling intensities and without cooling source in the temperature range of 1,350–1,200°C. That is because they had the same cooling rate that can be seen in Figure 8. However, in the temperature range of 1,200–550°C, the model with cooling source had lower transient von Mises stress than that without cooling source. Furthermore, a little difference was found between the various cooling intensities in the temperature range of 1,200–1,000°C because of the same cooling rate that can be seen in Figure 8. However, the transient von Mises stress decreased obviously from 1,000 to 550°C as the cooling intensity increases from 4,000 to 15,000 W/m2 K, and then it remained stable even if the cooling intensity reaches 20,000 W/m2 K. This is mainly because of the shrinkage of the metal in the quench zone, which causes the pressure on the front metal. The compressive stress produced by this extrusion can largely offset the tensile stress which was benefit to reduce the hot cracking susceptibility.

Figure 10 Effect of cooling intensity on the transient von Mises stress.
Figure 10

Effect of cooling intensity on the transient von Mises stress.

Figure 11 shows the transverse stress distributions along weld center line of different cooling intensities at t = 30 s. At this moment (t = 30 s), the heat source is moved to the place where x = 60 mm, and the cooling source is moved to the place where x = 45 mm. The transverse stresses of weld metal between cooling source and heat source were mainly investigated. The weld metal near the cooling source acted shrinks more rapidly as the cooling intensity increases. Hence, the transverse stresses became higher and even increased to approximately 600 MPa when the cooling intensity is 20,000 W/m2 K. Setting cooling intensity to 15,000 and 20,000 W/m2 K was only for the purpose of finding out the change rule of transient stress and compression to the metal between cooling source and heat source under limited conditions, which is difficult to achieve in the actual experiments. In the case without the cooling source, the transverse stress of weld metal from x = 45 mm to x = 60 mm was tensile and increased gradually. However, in the case with the cooling source, the cooling source changed the transverse stress from tensile to compressive. This is mainly because the weld metal near cooling source grinds against front meal. Moreover, it is obvious that the transverse compressive stress produced by this extrusion is helpful to play down the hot crack susceptibility. Furthermore, with the increase in cooling intensity, the compressive stress between x = 45 mm and x = 50 mm increased and there is no change in the compressive stress from x = 50 mm to x = 60 mm. That is because the cooling rate is increased with the increase in cooling intensity, and the compressive stress induced by the rapid cooling becomes stronger. This is consistent with the change of the transient von Mises stress in different temperature ranges in Figure 10. It can be concluded that the cooling source can change the transverse stress from tensile stress to compressive stress and improve the resistance to hot cracking. There is an appropriate value of cooling intensity, which is 15,000 W/m2 K in this article.

Figure 11 Transverse stress distributions along weld center line of different cooling intensities when t = 30 s.
Figure 11

Transverse stress distributions along weld center line of different cooling intensities when t = 30 s.

4.2 Effect of distance between cooling source and heat source on transient stress

During GTAW with trailing cooling source, the compression induced by rapid cooling may change with the distance between cooling source and heat source, Dis. Figure 12 shows the effect of Dis on the transient von Mises stress at the point x = 50 mm, y = 0 mm and z = 4 mm.

Figure 12 Effect of distance between cooling source and heat source on the transient von Mises stress.
Figure 12

Effect of distance between cooling source and heat source on the transient von Mises stress.

The model without cooling source can be seen as Dis toward infinity. It is shown that the difference in the Dis does not change the transient von Mises stress in the temperature range of 1,350–1,200°C. That is because that the weld metal has the same cooling rate in the temperature range of 1,350–1,200°C even if the Dis is different. In the temperature range of 1,200–550°C, the model with cooling source had lower transient von Mises stress than that without cooling source. When Dis was 15 mm, because of the strong cooling effect and the smallest distance, the transient von Mises stress decreased to the lowest level of four different distances in the temperature range of 1,200–970°C. As Dis is increased, metal compression between cooling source and heat source became weaker and the decrease in von Mises stress became less obvious. However, with the increase in the Dis, the von Mises stress decreased gradually and reached the bottom when Dis is 35 mm, and then it increased in the temperature range of 680–550°C. The most potent Dis that reduces the transient von Mises stress at the range of different temperatures is different.

The transverse stress distributions along weld center line of different Dis at t = 30 s are shown in Figure 13. At this moment (t = 30 s), the heat source is moved to the place where x = 60 mm. The transverse stress of weld metal was tensile stress and increased gradually from x = 45 mm to x = 60 mm when Dis is infinity. With the decrease in the Dis, the cooling source changed the transverse stress from tensile to compressive. This is because the cooling source increases the cooling rate of weld metal which is near the cooling source, which causes the compression. The value of compressive stress between x = 45 mm and x = 60 mm reached to maximum when the Dis is 25 mm. When the Dis decreases from 35 to 15 mm, the compressive stress between x = 45 mm and x = 55 mm decreased first and then increased, and the compressive stress between x = 55 mm and x = 60 mm increased. Furthermore, the compression zone became wider as the Dis increased from 15 to 35 mm. Hence, the distributions of the compressive stresses extended to a wider range on weld metal, which is helpful to reduce hot cracking susceptibility.

Figure 13 Transverse stress distributions along weld center line of different distances between cooling source and heat source when t = 30 s.
Figure 13

Transverse stress distributions along weld center line of different distances between cooling source and heat source when t = 30 s.

The above results indicated that appropriate Dis can reduce the transient von Mises stress, change the transverse tensile stress to transverse compressive stress and wide the compressive stress region. The transient von Mises stress and transverse stress were taken into consideration. The appropriate value of Dis is 35 mm.

4.3 Effect of radius of trailing cooling on transient stress

There are few investigations into the effect of radius of trailing cooling, r, on transient stress. Therefore, a simulation experiment was conducted under the condition of Dis = 15 mm to investigate the change of transient von Mises stress for different r in the welding process. Figure 14 shows the transient von Mises stress at points x = 50 mm, y = 0 mm and z = 4 mm for different r.

Figure 14 Effect of radius of trailing cooling source on the transient von Mises stress.
Figure 14

Effect of radius of trailing cooling source on the transient von Mises stress.

The model without cooling source can been seen as r toward infinitesimal. It is shown that the difference in the r does not change the transient von Mises stress in the temperature range of 1,350–1,200°C. With the increase in r, the transient von Mises stress decreased gradually, reaching a minimum at 12 mm, and then it kept stable in the temperature range of 1,200–550°C. Furthermore, in this temperature range, the weld metal was in a state of low ductility, and the decrease in the instantaneous von Mises stress can reduce the degree of stretching of the liquid film, which is beneficial to reduce the occurrence of hot cracking of the nickel-based alloy weld.

The transverse stress distributions along the weld center line of different r when t = 30 s are shown in Figure 15. At this moment (t = 30 s), the heat source moved to the place where x = 60 mm, and the cooling source moved to the place where x = 45 mm. It is obvious that the transverse stresses exist in the form of compressive stresses between x = 45 mm and x = 60 mm. However, the transverse stresses changed very little as r increased. As the connection between von Mises stress and principal stresses on three directions was complicated, there may be other factors that affected cooperatively with the compression induced by rapid cooling to reduce the transient von Mises stress.

Figure 15 Transverse stress distributions along weld center line of different radiuses of trailing cooling source when t = 30 s.
Figure 15

Transverse stress distributions along weld center line of different radiuses of trailing cooling source when t = 30 s.

The above results indicate that the transient von Mises stress decreases most when r increases to 12 mm. The capability of reducing von Mises stress and hot cracking susceptibility improves little when r is larger than 12 mm.

4.4 Effect of combined cooling source on transient stress

In order to research the effect of combined cooling source on hot cracking susceptibility of nickel-based alloy weld, two cooling ways were discussed as shown in Figure 3. One of the methods is that the liquid nitrogen just flows into the cooling pipe located in position 1, and the other way is that the liquid nitrogen flows into two cooling pipes located in positions 1 and 2.

Figure 16 shows the effect of different cooling methods on von Mises stress. From Figure 16, it can be seen that the transient von Mises stress had little change even if the cooling way changes in the temperature range of 1,350–1,200°C. In the temperature range of 1,200–550°C, the von Mises stress decreased to a lower level with the combined cooling source than others. This means that the combined cooling source has a better effect than welding with a single trailing cooling source on the control of transient stress and hot cracking susceptibility. Combined cooling source provided one more orientation of radiation for weld metal than the single trailing cooling source. This increased the cooling rate of weld metal which was helpful to reduce the transient stress and hot cracking susceptibility.

Figure 16 Effect of different cooling methods on the transient von Mises stress.
Figure 16

Effect of different cooling methods on the transient von Mises stress.

As can be seen from part (a) of Figure 17, the microstructures of weld center are almost large columnar grain structure. When the sheets were welded with the single trailing cooling source, the grains got refined and the coarse columnar grains were changed into equiaxed grains. In addition, comparing (b) and (c) of Figure 17, it can be observed that the grains became finer when the sheets were welded with the combined cooling source. Combined cooling source provided one more orientation of radiation for weld metal than the single trailing cooling source, which resulted in the cooling rate increases. Furthermore, with increasing cooling rate the undercooling of weld increased, which caused grain refinement. This confirmed that the combined cooling source can reduce the hot cracking susceptibility of nickel-based alloy weld joints through adjusting metallurgical and stress factors.

Figure 17 Microstructures of weld with different positions of cooling pipe. (a) Conventional welding; (b) single trailing cooling and (c) combined cooling.
Figure 17

Microstructures of weld with different positions of cooling pipe. (a) Conventional welding; (b) single trailing cooling and (c) combined cooling.

5 Conclusions

In this article, the effect of cooling source parameters on the transient von Mises stress and hot cracking susceptibility of Nicrofer 6023H sheets was investigated by numerical simulation. Conclusions of this investigation are as follows:

  1. Under the single trailing cooling source, the transient von Mises stress first decreases, and then increased with the increase in the cooling intensity and reaches the minimum value at 15,000 W/m2 K. The transverse tensile stress turns into compressive stress, and the weld has the lowest susceptibility to hot crack when the cooling intensity reaches 15,000 W/m2 K.

  2. Under the single trailing cooling source, the most potent Dis that reduces the transient von Mises stress at the range of different temperatures is different. However, the width of the zone of the transverse compressive stress reaches maximum when Dis is 35 mm. This Dis has a better effect in reducing the transient von Mises stress and hot cracking susceptibility.

  3. Under the single trailing cooling source, with the increase in r from 4 mm to 16 mm, the transient von Mises stress first decreases, and then keeps stable and reaches minimum when r is 12 mm.

  4. The combined cooling source has a better effect than the single trailing cooling source on the control of transient stress in the welding process and hot cracking susceptibility. Combined cooling source can reduce the hot cracking susceptibility of nickel-based alloy weld joints by adjusting metallurgical and stress factors.

Acknowledgments

The authors gratefully acknowledge the financial support by the Natural Science Foundation of Hebei Province, P.R. China under Grant No. E2017202011.

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Received: 2019-08-02
Revised: 2019-12-08
Accepted: 2020-05-13
Published Online: 2020-12-05

© 2020 Meng He et al., published by De Gruyter

This work is licensed under the Creative Commons Attribution 4.0 International License.

Articles in the same Issue

  1. Research Article
  2. Electrochemical reduction mechanism of several oxides of refractory metals in FClNaKmelts
  3. Study on the Appropriate Production Parameters of a Gas-injection Blast Furnace
  4. Microstructure, phase composition and oxidation behavior of porous Ti-Si-Mo intermetallic compounds fabricated by reactive synthesis
  5. Significant Influence of Welding Heat Input on the Microstructural Characteristics and Mechanical Properties of the Simulated CGHAZ in High Nitrogen V-Alloyed Steel
  6. Preparation of WC-TiC-Ni3Al-CaF2 functionally graded self-lubricating tool material by microwave sintering and its cutting performance
  7. Research on Electromagnetic Sensitivity Properties of Sodium Chloride during Microwave Heating
  8. Effect of deformation temperature on mechanical properties and microstructure of TWIP steel for expansion tube
  9. Effect of Cooling Rate on Crystallization Behavior of CaO-SiO2-MgO-Cr2O3 Based Slag
  10. Effects of metallurgical factors on reticular crack formations in Nb-bearing pipeline steel
  11. Investigation on microstructure and its transformation mechanisms of B2O3-SiO2-Al2O3-CaO brazing flux system
  12. Energy Conservation and CO2 Abatement Potential of a Gas-injection Blast Furnace
  13. Experimental validation of the reaction mechanism models of dechlorination and [Zn] reclaiming in the roasting steelmaking zinc-rich dust process
  14. Effect of substituting fine rutile of the flux with nano TiO2 on the improvement of mass transfer efficiency and the reduction of welding fumes in the stainless steel SMAW electrode
  15. Microstructure evolution and mechanical properties of Hastelloy X alloy produced by Selective Laser Melting
  16. Study on the structure activity relationship of the crystal MOF-5 synthesis, thermal stability and N2 adsorption property
  17. Laser pressure welding of Al-Li alloy 2198: effect of welding parameters on fusion zone characteristics associated with mechanical properties
  18. Microstructural evolution during high-temperature tensile creep at 1,500°C of a MoSiBTiC alloy
  19. Effects of different deoxidization methods on high-temperature physical properties of high-strength low-alloy steels
  20. Solidification pathways and phase equilibria in the Mo–Ti–C ternary system
  21. Influence of normalizing and tempering temperatures on the creep properties of P92 steel
  22. Effect of temperature on matrix multicracking evolution of C/SiC fiber-reinforced ceramic-matrix composites
  23. Improving mechanical properties of ZK60 magnesium alloy by cryogenic treatment before hot extrusion
  24. Temperature-dependent proportional limit stress of SiC/SiC fiber-reinforced ceramic-matrix composites
  25. Effect of 2CaO·SiO2 particles addition on dephosphorization behavior
  26. Influence of processing parameters on slab stickers during continuous casting
  27. Influence of Al deoxidation on the formation of acicular ferrite in steel containing La
  28. The effects of β-Si3N4 on the formation and oxidation of β-SiAlON
  29. Sulphur and vanadium-induced high-temperature corrosion behaviour of different regions of SMAW weldment in ASTM SA 210 GrA1 boiler tube steel
  30. Structural evidence of complex formation in liquid Pb–Te alloys
  31. Microstructure evolution of roll core during the preparation of composite roll by electroslag remelting cladding technology
  32. Improvement of toughness and hardness in BR1500HS steel by ultrafine martensite
  33. Influence mechanism of pulse frequency on the corrosion resistance of Cu–Zn binary alloy
  34. An interpretation on the thermodynamic properties of liquid Pb–Te alloys
  35. Dynamic continuous cooling transformation, microstructure and mechanical properties of medium-carbon carbide-free bainitic steel
  36. Influence of electrode tip diameter on metallurgical and mechanical aspects of spot welded duplex stainless steel
  37. Effect of multi-pass deformation on microstructure evolution of spark plasma sintered TC4 titanium alloy
  38. Corrosion behaviors of 316 stainless steel and Inconel 625 alloy in chloride molten salts for solar energy storage
  39. Determination of chromium valence state in the CaO–SiO2–FeO–MgO–CrOx system by X-ray photoelectron spectroscopy
  40. Electric discharge method of synthesis of carbon and metal–carbon nanomaterials
  41. Effect of high-frequency electromagnetic field on microstructure of mold flux
  42. Effect of hydrothermal coupling on energy evolution, damage, and microscopic characteristics of sandstone
  43. Effect of radiative heat loss on thermal diffusivity evaluated using normalized logarithmic method in laser flash technique
  44. Kinetics of iron removal from quartz under ultrasound-assisted leaching
  45. Oxidizability characterization of slag system on the thermodynamic model of superalloy desulfurization
  46. Influence of polyvinyl alcohol–glutaraldehyde on properties of thermal insulation pipe from blast furnace slag fiber
  47. Evolution of nonmetallic inclusions in pipeline steel during LF and VD refining process
  48. Development and experimental research of a low-thermal asphalt material for grouting leakage blocking
  49. A downscaling cold model for solid flow behaviour in a top gas recycling-oxygen blast furnace
  50. Microstructure evolution of TC4 powder by spark plasma sintering after hot deformation
  51. The effect of M (M = Ce, Zr, Ce–Zr) on rolling microstructure and mechanical properties of FH40
  52. Phase evolution and oxidation characteristics of the Nd–Fe–B and Ce–Fe–B magnet scrap powder during the roasting process
  53. Assessment of impact mechanical behaviors of rock-like materials heated at 1,000°C
  54. Effects of solution and aging treatment parameters on the microstructure evolution of Ti–10V–2Fe–3Al alloy
  55. Effect of adding yttrium on precipitation behaviors of inclusions in E690 ultra high strength offshore platform steel
  56. Dephosphorization of hot metal using rare earth oxide-containing slags
  57. Kinetic analysis of CO2 gasification of biochar and anthracite based on integral isoconversional nonlinear method
  58. Optimization of heat treatment of glass-ceramics made from blast furnace slag
  59. Study on microstructure and mechanical properties of P92 steel after high-temperature long-term aging at 650°C
  60. Effects of rotational speed on the Al0.3CoCrCu0.3FeNi high-entropy alloy by friction stir welding
  61. The investigation on the middle period dephosphorization in 70t converter
  62. Effect of cerium on the initiation of pitting corrosion of 444-type heat-resistant ferritic stainless steel
  63. Effects of quenching and partitioning (Q&P) technology on microstructure and mechanical properties of VC particulate reinforced wear-resistant alloy
  64. Study on the erosion of Mo/ZrO2 alloys in glass melting process
  65. Effect of Nb addition on the solidification structure of Fe–Mn–C–Al twin-induced plasticity steel
  66. Damage accumulation and lifetime prediction of fiber-reinforced ceramic-matrix composites under thermomechanical fatigue loading
  67. Morphology evolution and quantitative analysis of β-MoO3 and α-MoO3
  68. Microstructure of metatitanic acid and its transformation to rutile titanium dioxide
  69. Numerical simulation of nickel-based alloys’ welding transient stress using various cooling techniques
  70. The local structure around Ge atoms in Ge-doped magnetite thin films
  71. Friction stir lap welding thin aluminum alloy sheets
  72. Review Article
  73. A review of end-point carbon prediction for BOF steelmaking process
https://doi.org/10.1515/htmp-2020-0067
Keywords for this article
nickel-based alloys; hot cracking susceptibility; rapid cooling; finite element method; transient stress
Creative Commons
BY 4.0

Articles in the same Issue

  1. Research Article
  2. Electrochemical reduction mechanism of several oxides of refractory metals in FClNaKmelts
  3. Study on the Appropriate Production Parameters of a Gas-injection Blast Furnace
  4. Microstructure, phase composition and oxidation behavior of porous Ti-Si-Mo intermetallic compounds fabricated by reactive synthesis
  5. Significant Influence of Welding Heat Input on the Microstructural Characteristics and Mechanical Properties of the Simulated CGHAZ in High Nitrogen V-Alloyed Steel
  6. Preparation of WC-TiC-Ni3Al-CaF2 functionally graded self-lubricating tool material by microwave sintering and its cutting performance
  7. Research on Electromagnetic Sensitivity Properties of Sodium Chloride during Microwave Heating
  8. Effect of deformation temperature on mechanical properties and microstructure of TWIP steel for expansion tube
  9. Effect of Cooling Rate on Crystallization Behavior of CaO-SiO2-MgO-Cr2O3 Based Slag
  10. Effects of metallurgical factors on reticular crack formations in Nb-bearing pipeline steel
  11. Investigation on microstructure and its transformation mechanisms of B2O3-SiO2-Al2O3-CaO brazing flux system
  12. Energy Conservation and CO2 Abatement Potential of a Gas-injection Blast Furnace
  13. Experimental validation of the reaction mechanism models of dechlorination and [Zn] reclaiming in the roasting steelmaking zinc-rich dust process
  14. Effect of substituting fine rutile of the flux with nano TiO2 on the improvement of mass transfer efficiency and the reduction of welding fumes in the stainless steel SMAW electrode
  15. Microstructure evolution and mechanical properties of Hastelloy X alloy produced by Selective Laser Melting
  16. Study on the structure activity relationship of the crystal MOF-5 synthesis, thermal stability and N2 adsorption property
  17. Laser pressure welding of Al-Li alloy 2198: effect of welding parameters on fusion zone characteristics associated with mechanical properties
  18. Microstructural evolution during high-temperature tensile creep at 1,500°C of a MoSiBTiC alloy
  19. Effects of different deoxidization methods on high-temperature physical properties of high-strength low-alloy steels
  20. Solidification pathways and phase equilibria in the Mo–Ti–C ternary system
  21. Influence of normalizing and tempering temperatures on the creep properties of P92 steel
  22. Effect of temperature on matrix multicracking evolution of C/SiC fiber-reinforced ceramic-matrix composites
  23. Improving mechanical properties of ZK60 magnesium alloy by cryogenic treatment before hot extrusion
  24. Temperature-dependent proportional limit stress of SiC/SiC fiber-reinforced ceramic-matrix composites
  25. Effect of 2CaO·SiO2 particles addition on dephosphorization behavior
  26. Influence of processing parameters on slab stickers during continuous casting
  27. Influence of Al deoxidation on the formation of acicular ferrite in steel containing La
  28. The effects of β-Si3N4 on the formation and oxidation of β-SiAlON
  29. Sulphur and vanadium-induced high-temperature corrosion behaviour of different regions of SMAW weldment in ASTM SA 210 GrA1 boiler tube steel
  30. Structural evidence of complex formation in liquid Pb–Te alloys
  31. Microstructure evolution of roll core during the preparation of composite roll by electroslag remelting cladding technology
  32. Improvement of toughness and hardness in BR1500HS steel by ultrafine martensite
  33. Influence mechanism of pulse frequency on the corrosion resistance of Cu–Zn binary alloy
  34. An interpretation on the thermodynamic properties of liquid Pb–Te alloys
  35. Dynamic continuous cooling transformation, microstructure and mechanical properties of medium-carbon carbide-free bainitic steel
  36. Influence of electrode tip diameter on metallurgical and mechanical aspects of spot welded duplex stainless steel
  37. Effect of multi-pass deformation on microstructure evolution of spark plasma sintered TC4 titanium alloy
  38. Corrosion behaviors of 316 stainless steel and Inconel 625 alloy in chloride molten salts for solar energy storage
  39. Determination of chromium valence state in the CaO–SiO2–FeO–MgO–CrOx system by X-ray photoelectron spectroscopy
  40. Electric discharge method of synthesis of carbon and metal–carbon nanomaterials
  41. Effect of high-frequency electromagnetic field on microstructure of mold flux
  42. Effect of hydrothermal coupling on energy evolution, damage, and microscopic characteristics of sandstone
  43. Effect of radiative heat loss on thermal diffusivity evaluated using normalized logarithmic method in laser flash technique
  44. Kinetics of iron removal from quartz under ultrasound-assisted leaching
  45. Oxidizability characterization of slag system on the thermodynamic model of superalloy desulfurization
  46. Influence of polyvinyl alcohol–glutaraldehyde on properties of thermal insulation pipe from blast furnace slag fiber
  47. Evolution of nonmetallic inclusions in pipeline steel during LF and VD refining process
  48. Development and experimental research of a low-thermal asphalt material for grouting leakage blocking
  49. A downscaling cold model for solid flow behaviour in a top gas recycling-oxygen blast furnace
  50. Microstructure evolution of TC4 powder by spark plasma sintering after hot deformation
  51. The effect of M (M = Ce, Zr, Ce–Zr) on rolling microstructure and mechanical properties of FH40
  52. Phase evolution and oxidation characteristics of the Nd–Fe–B and Ce–Fe–B magnet scrap powder during the roasting process
  53. Assessment of impact mechanical behaviors of rock-like materials heated at 1,000°C
  54. Effects of solution and aging treatment parameters on the microstructure evolution of Ti–10V–2Fe–3Al alloy
  55. Effect of adding yttrium on precipitation behaviors of inclusions in E690 ultra high strength offshore platform steel
  56. Dephosphorization of hot metal using rare earth oxide-containing slags
  57. Kinetic analysis of CO2 gasification of biochar and anthracite based on integral isoconversional nonlinear method
  58. Optimization of heat treatment of glass-ceramics made from blast furnace slag
  59. Study on microstructure and mechanical properties of P92 steel after high-temperature long-term aging at 650°C
  60. Effects of rotational speed on the Al0.3CoCrCu0.3FeNi high-entropy alloy by friction stir welding
  61. The investigation on the middle period dephosphorization in 70t converter
  62. Effect of cerium on the initiation of pitting corrosion of 444-type heat-resistant ferritic stainless steel
  63. Effects of quenching and partitioning (Q&P) technology on microstructure and mechanical properties of VC particulate reinforced wear-resistant alloy
  64. Study on the erosion of Mo/ZrO2 alloys in glass melting process
  65. Effect of Nb addition on the solidification structure of Fe–Mn–C–Al twin-induced plasticity steel
  66. Damage accumulation and lifetime prediction of fiber-reinforced ceramic-matrix composites under thermomechanical fatigue loading
  67. Morphology evolution and quantitative analysis of β-MoO3 and α-MoO3
  68. Microstructure of metatitanic acid and its transformation to rutile titanium dioxide
  69. Numerical simulation of nickel-based alloys’ welding transient stress using various cooling techniques
  70. The local structure around Ge atoms in Ge-doped magnetite thin films
  71. Friction stir lap welding thin aluminum alloy sheets
  72. Review Article
  73. A review of end-point carbon prediction for BOF steelmaking process
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