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Hydraulic Study of Bubble Migration in Liquid Titanium Alloy Melt during Vertical Centrifugal Casting Process

  • Qin Xu EMAIL logo , Xing Wang and Shiping Wu
Published/Copyright: October 16, 2018
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High Temperature Materials and Processes
From the journal High Temperature Materials and Processes Volume 38 Issue 2019

Abstract

The bubble migration in liquid titanium melt during vertical centrifugal casting process has been investigated by hydraulic experiments. Results show that the gas bubble in the simple cavity ultimately migrates like a line parallel to the wall in the opposite direction to the rotational casting mould. The deviation distance of the bubble in the simple geometry cavity tends to increase with the increment of the mould rotational speed during the migration process. And the gas bubble is much easier to migrate like a line when its initial position is nearer to the casting mould wall which is opposite to the mould rotational direction. The migration trajectories of bubbles located at different position in the complex cavity are more complicated than that in the simple cavity. The casting mould in the complex cavity can hamper both the radial movement and the circular movement of the bubble. And gas bubbles will gather, re-nucleate and form new bigger bubbles beside the casting mould wall. The re-formed gas bubbles in the complex cavity become bigger than which escape from bubble generation chamber.

Keywords: titanium alloy; vertical centrifugal casting; bubble migration; hydraulic simulation

Titanium alloys have been widely used in both military and commercial aircraft for its excellent properties, such as low density, high specific strength and good creep-resisting property under high temperature [1, 2, 3]. However, the melting temperature of titanium alloys is high, and the viscosity of the melt is high, consequently the fluidity of the melt is poor [3]. Therefore, it is rather difficult to improve the filling property of the melt by increasing the pouring temperature. While the filling property can be improved by the centrifugal force developed by the high rotation speed during vertical centrifugal casting process for the filling time and the temperature decline degree can be reduced by the high centrifugal force, and hence improve the melt fluidity. Therefore, most of the titanium castings with big size and complex geometry structure are mainly produced by vertical centrifugal casting technology [4]. On the other aspect, titanium alloys show very high chemical activity at high temperature, and gases have high solubility in molten titanium alloys [5, 6]. The state of gases in the titanium alloy melts are mainly in the form of “solution” or “solid solution” state [7, 8]. When the titanium alloys solidify, the gas solubility become smaller for the temperature drop of the liquid titanium alloy melts. Consequently, the gas solubilized in the melt escape from the liquid melt and bubbles eventually form in the alloys. Then some of the bubbles precipitate on the solid surface and form surface or subsurface porosity, while some of them are remained in the casting and form inner pores [9, 10].

Many researchers have observed the blowholes formed in the titanium alloys by x-ray radiography [7, 11], Neutron radiography inspection [8], numerical simulation analysis [12] and theoretical analysis [13], etc. Watanabe I. et al. [7] detected the casting porosity by x-ray radiography and calculated the porosity level by quantitative image analysis. Hero et al. [11] studied the porosity by x-ray radiography and density measurements. W.J. Richards et al. [8] inspected mold face coat inclusions in titanium investment castings by the neutron radiographic system of which the detection ability of the defects in the precision titanium alloy castings was highly improved. Chai et al. [12] studied the high Nb-TiAl alloy blade casts produced by investment casting process with numerical simulation method and results show that the shrinkage porosities in gravity casting are much more and dispersed than those in centrifugal casting. Sui et al. [13] studied the gas solubility, nucleation conditions, and nucleation rate, etc. in centrifugal casting liquid metal filling process by theoretical analysis.

The existence of gas holes and porosity in castings can greatly reduce their mechanical properties, air tightness, physical and chemical properties, and even can result in the rejection of casting. Measures must be taken to reduce or even prevent the gas defects in the titanium alloy castings. Watanabe’s results show that smaller amount of porosity can be obtained by choosing an argon pressure difference and the smallest amount of porosity (approximately 0.8 %) will be getting in the specimens cast at 150 torr [7]. The experiments show that castings without a Ti foil contained little porosity, but the porosity can be averted by keeping smaller pressure differences between the melting furnace and the casting cavity [11]. A. Choudhury et al. found that by increasing the preheat temperature to 1,000℃ can prevent the porosity in the TiAl alloy exhaust valve produced by the vertical centrifugal casting process [5]. Guttal S et al. [14] measured the influence of the sprue number and position on the porosity of cast titanium crowns. Results show that castings with double sprues have less internal porosity than those with single sprue. Fu P. X. and K.Liu et al. [15] studied the centrifugal casting process of TiAl exhaust valves and revealed that to moderately increase the gate size can effectively keep the feeding path open and there are no porosity in the casting with runner and gating systems in a staggered arrangement. WU MH et al. [16, 17] calculated the filling and solidification with different sprue designs (e.g., tree, ball, and runner-bar) by the MAGMASOFT software, and gas pore sensitivity were estimated based on the filling and solidification results. Results show that the sprue design is one of the most important factors in improving the property of casting titanium dentures.

As stated previously, the ultimate state of gas porosity, the effect on the casting properties, and how to reduce the gas porosity in titanium alloy castings have received considerable research attentions. However, very little work has been done on the bubble migration in liquid titanium alloy melt which will affect the formation of the gas porosity. Thus, the aim of the present work is to study the bubble migration in the liquid Ti-6Al-4V alloy melt in the simple and complex cavities during vertical centrifugal casting process.

Experimental procedure

The rotational velocity range of centrifugal casting machine used in the model experiment is 0 ~ 1200 rpm, so different rotational velocities can be selected in the experiment and its effect on the bubble migration will be investigated. The high-speed camera used in the study can take 1,000 pictures per second, and can meet the need of the experiment. The schematic diagram of hydraulic simulation apparatus is shown in Figure 1 and the polymethyl methacrylate (PMMA) casting mold for hydraulic simulation of bubble migration is shown in Figure 2. The bubble generation chambers were made on the bottom of the casting mould according to the positions shown in Figure 2(a), (b), (c), (d) and (e). The geometry structure of the bubble generation chamber is shown in Figure 2(f).

Figure 1: Schematic diagram of hydraulic simulation apparatus for bubble migration in titanium melt during vertical centrifugal casting process.
Figure 1:

Schematic diagram of hydraulic simulation apparatus for bubble migration in titanium melt during vertical centrifugal casting process.

Figure 2: PMMA casting mold for physical simulation of bubble migration.
Figure 2:

PMMA casting mold for physical simulation of bubble migration.

In order to study the effect of the geometry structure on the bubble migration in titanium alloy melt during vertical centrifugal casting process, the bubble migration in two different casting mould cavities were studied in the experiment. The cavities are the casting molds with simple geometry structure as a “rectangle” and the casting molds with complex geometry structure as a half of Chinese characters “Happiness”. The schematic of the casting molds with simple geometry structure and complex geometry structure are shown in Figure 3(a) and Figure 3(b), respectively. Different mould rotational velocities (shown in Table 1) were used in the experiment, and the casting mould rotates clockwise in the experiment.

Figure 3: The PMMA casting molds and their dimensions.
Figure 3:

The PMMA casting molds and their dimensions.

Table 1:

Selection of mould rotation speed.

Experiment NO.Motor frequency/HZRotational velocity/rpm
15.15160
210.13300
313.46400
416.8500

The simulated medium in the experiment is mainly water. From the reference [18] and the data provided by ProCAST software, we know that the viscosity of water at 6–7℃ is equal to that of the TC4 alloy melt at the liquidus temperature, that is about 1.45×10−3Pa.S. And the viscosity of water at 11–12℃ is equal to that of the TC4 alloy melt with superheat temperature of 100℃, that is about 1.257×10−3Pa.S. The room temperature when we did the hydraulic experiment is about 20℃, and the viscosity of water at 1.01325×105Pa, 20℃ is 1.01×10−3Pa.S. Therefore, the tackifier is added into the simulated water for the viscosity of water is smaller than the real liquid melt, and consequently to make the viscosity of the simulated medium identical to that of the titanium alloy. Thus, they can meet the physical simulation similarity criterion of the titanium alloy during its mold filling in the vertical centrifugal casting process. In order to make the captured images more clearly, white background is set on the bottom of the mould and a certain amount of red dye is added into the simulated medium.

Before the experiment has been carried out, the bubble chamber is preset on the PMMA casting mold. Then a small piece of CaC2 particle is put into the dried bubble chamber and the chamber is tightly sealed. After that, the PMMA casting mold will be fixed on the centrifugal turntable. When the centrifugal turntable is rotating at a certain stable rotating speed, the simulated medium will be poured into the rotating casting mold. At the meantime, the high speed camera is started and the bubble moving process will be shot until the moving trajectory is steady.

Experimental results and discussions

To the best of our knowledge, titanium alloys are usually melted and poured in the vacuum induction furnace at Ar atmosphere. So gas porosities in titanium alloy castings cannot form in the filling process by air entrapment. However, the liquid titanium alloy melt will first expose to the outer wall of the mould during the filling process and it shows very high chemical activity with the casting mould wall at high temperature. And gas porosities always form at the outer surface of casting by the reaction of the liquid melt and the casting mould after the melt fill the cavity. Therefore, we will study the bubble migration of the reactive gas pores in the titanium castings during vertical centrifugal casting process in the present paper.

Bubble migration trajectory in the simple cavity

Figure 4 shows the migration trajectory of bubble at position a), b) and c) in the simple cavity shown in Figure 2 when the casting mould rotated clockwise at speed of 300 rpm. From Figure 4(a) and (b) we can see that the migration of bubble located at position a) and b) in Figure 2 during vertical centrifugal casting process can be divided into the radial movement forward to the casting rotating shaft and the circular movement opposite to the direction of the rotating mould. After a period of time, the bubbles continue to migrate like a line parallel to the casting mould wall in the direction opposite to the rotational casting mould. From Figure 4(c) we can see that the gas bubble migrates to the rotating shaft like a line close to the casting mould wall in the opposite direction to the rotational casting mould when the bubble posited at position c).

Figure 4: Migration trajectory of bubble at different position in simple cavity (clockwise, 300 rpm).
Figure 4:

Migration trajectory of bubble at different position in simple cavity (clockwise, 300 rpm).

As is shown in Figure 2, the bubble at position a) in the simple cavity is posited at the location close to the mold wall near the rotation direction of the rotating mould, while the bubble at position b) is posited at the location at the center line of the two casting mould wall. And the bubble at position c) is posited at the location near the mold wall opposite to the rotation direction of the casting mould. For the casting mold wall has a blocking effect on the circular movement, therefore, the migration trajectory of the bubble at position a) in Figure 2 is a line close to the casting mould wall in the opposite direction to the rotation of the mould and the ultimate migration trajectory of the bubble at position b) and c) in Figure 2 is like a line close to the casting mould wall in the opposite direction of the casting mould.

Bubble migration trajectory in the complex cavity

Figure 5 shows the migration trajectory of bubble at position d) and e) in the complex cavity shown in Figure 2 when the mould rotated clockwise at speed of 300 rpm. Compared with the bubble migration trajectories in the simple cavity, the migration trajectories of bubbles at different position in complex cavity become more complicated. The gas bubbles in the simulated liquid at position d) first migrate along the casting mould wall in the direction opposite to the rotation of the mould, and then they gather at the white ellipse zone shown in Figure 5(a) for the blocking effect of the complex geometry shape of the casting mould on the bubble migration. After the gases reaching a certain amount, they re-nucleate and form new bigger bubbles along the casting mould wall and continue to move toward the rotating shaft of the casting mould. On the other aspect, we can see that the re-formed gas bubbles in the complex cavity become much bigger than which escape from bubble generation chamber.

Figure 5: Migration trajectory of bubble at different position in complex cavity (clockwise, 300 rpm).
Figure 5:

Migration trajectory of bubble at different position in complex cavity (clockwise, 300 rpm).

While the migration of gas bubbles at position e) can be divided into the radial movement forward to the casting rotating shaft and the circular movement opposite to the direction of the rotating mould during their initial moving stage. Then the gas bubbles will change their migration direction and begin to move along the casting mould wall which located at the opposite direction of the rotational casting mould for the blocking effect of the mould wall at the white ellipse zone shown in Figure 5(b). When the bubbles migrate to the end of this mould wall, the blocking effect disappears, and the bubbles will continue to move to the casting rotating shaft again. The bubble migration thereafter is similar to the bubble migration at position d). However, the moving speed of the bubble is much lower.

Through the above analysis we can know that the migration process of bubbles located at position e) is more complicated than that of bubbles form at position d). We can also find a very interesting phenomenon, the mould wall at the white ellipse zone shown in Figure 5(a) and Figure 5(b) all have blocking effect on the bubble migration, however, the gas bubbles gather at the ellipse zone in Figure 5(a) while not gather in Figure 5(b). This can be attributed to the different blocking effect of the mould wall on the bubble migration. The mould wall at the ellipse zone in Figure 5(a) hampered both the radial movement and the circular movement, while the mould wall at the ellipse zone in Figure 5(b) only hampered the radial movement of the gas bubble. And the bubble at the ellipse zone in Figure 5(b) can also move circumferentially to the wall in the opposite direction of the rotating mould. Therefore, the gas bubbles cannot gather at the ellipse zone in Figure 5(b).

To summarize, the bubble migration is influenced not only by complexity of the casting mould cavity and the number of the barriers in the mould cavity, but also by the different blocking effect of the casting mould wall on the bubble migration.

Effect of mould rotational speed on the bubble migration trajectory

Figure 6 shows the migration trajectory of bubble at position b) in the simple cavity shown in Figure 2 under different mould rotational speed when the mould rotates clockwise. The results show that whether the rotational speed is high or low, the bubble migration trajectory in the titanium alloy melts under vertical centrifugal casting process can all be divided into the radial movement forward to the casting rotating shaft and the circular movement opposite to the direction of the rotating mould. And the casting mould wall has an impeditive effect on the circular movement during the bubble moving process. Therefore, the gas bubble ultimately migrates to the casting rotating shaft like a line close to the casting mould wall in the opposite direction of the rotation casting mould. On the other aspect, the distance from the position where the bubble starts to migrate like a line to its initial position in the simple cavity is different when the rotational speed of the casting mould is different. In this paper, the distance from the position where the bubble begin to migrate like a line to the bubble initial position (that is the position of the bubble generation chamber) will be described as “Deviation distance” and it will be discussed in detail in section “The deviation distance of bubble in the simple cavity”.

Figure 6: Migration trajectory of bubble with different mould rotational speed (clockwise).
Figure 6:

Migration trajectory of bubble with different mould rotational speed (clockwise).

Figure 7(a) and (b) show the migration trajectories of bubble at position d) in the complex cavity shown in Figure 2 when the mould rotates clockwise at 300 rpm and 400 rpm respectively. As has been described in section “Bubble migration trajectory in the complex cavity”, the gas bubbles re-nucleate and form new bigger bubbles along the casting mould wall in the white ellipse zone. The number of the re-formed bubbles becomes less and the volume of the re-formed bubbles becomes much bigger than that when the bubbles escape from bubble generation chamber. Furthermore, from Figure 7 we can also see that the number of the re-formed bubbles become less and the volume of the re-formed gas bubbles become smaller with the increment of the casting mould rotational speed. This can be attributed to the pressure difference at different position under different casting rotational speed.

Figure 7: Migration trajectory of bubble at different position in complex cavity (clockwise).
Figure 7:

Migration trajectory of bubble at different position in complex cavity (clockwise).

The deviation distance of bubble in the simple cavity

As has been stated before, because of the blocking effect of the casting mould wall on the bubble migration, the bubbles in the simple cavity tend to migrate like a line parallel to the casting mould wall in the direction opposite to the rotational casting mould. In this paper, the distance from the bubble initial position to the position where the bubbles begin to migrate like a line is described as “Deviation distance”, and is denoted by “x” in Figure 6(a).

Figure 8 show the deviation distance of bubble in the simulated liquid under different rotational speed at position b) in the simple cavity shown in Figure 2 when the mould rotates clockwise. From Figure 8 we can see that the deviation distance of bubble increase with the increment of the casting rotational speed. When the casting mould rotates at 150 rpm, the bubble deviation distance is about 55 mm, while the bubble deviation distance increase to 95.5 mm when the casting mould rotates at 300 rpm. Consequently, the gas bubbles in the titanium alloy melt are easily to form surface or subsurface blowholes near the casting mould wall when the casting mould rotational speed is lower. Thus, the increment of the casting rotational speed can make bubble more easily migrate from the cavity to the gating system. And it can therefore reduce the gas porosity in the titanium alloy melt during its vertical centrifugal casting process by increasing the mould rotational speed. The relationship between the deviation distance “x” and the casting mould rotational speed ω can be expressed approximately exponentially as follows,

(1)x=−185∗exp(−ω/433)+184
Figure 8: Deviation distance of bubble under different rotational speed (position in Figure 2(b)).
Figure 8:

Deviation distance of bubble under different rotational speed (position in Figure 2(b)).

Figure 9 show the deviation distance of bubble at different bubble initial position in the simple cavity shown in Figure 2 when the mould rotates clockwise at 300 rpm. From Figure 9 we can see that when the initial position of the gas bubble located at position a), the deviation distance of bubble is about 112 mm. And when the initial position of the gas bubble located at position c), the deviation distance of bubble sharply decrease to about 2 mm. That is, when the initial position of the bubble located at the position which is more close to the casting mould wall opposite to the mould rotational direction, the deviation distance of bubble is much smaller. Consequently, the gas bubble is much easier to migrate like a line while the initial position of the bubble is nearer to the casting mould wall opposite to the mould rotational direction. And the bubbles are easier to remove from the liquid melt. Therefore, it is much difficult to form gas pores in the castings in the practical casting process.

Figure 9: Deviation distance of bubble at different position (300 rpm).
Figure 9:

Deviation distance of bubble at different position (300 rpm).

Conclusions

(1) The bubble migration in the simple cavity during vertical centrifugal casting process can be divided into the radial movement forward to the casting rotating shaft and the circular movement opposite to the direction of the rotating mould.

(2) The casting mould in the complex cavity can hamper both the radial movement and the circular movement of the bubble. And gas bubbles will gather, re-nucleate and form new bigger bubbles beside the casting mould wall when the wall hampered both the radial movement and the circular movement, while the bubbles only change the migration direction when the wall only hampered the radial movement.

(3) The deviation distance of the bubble in the simple geometry cavity tends to increase with the increment of the mould rotational speed during the migration process. When the initial position of the bubble lies near the wall opposite to the mould rotational direction, the bubble is prone to move in a linear way.

Xu Qin, Female, Ph.D., lecture. Directions of research: theory and technology of materials solidification and structure control; numerical simulation of mould filling and solidification.

Funding statement: This work was supported by Foundation items: The Initial Scientific Research Fund of Young Teachers in Henan University of Technology (Grant No. 2018QNJH25) and the National Natural Science Foundation of China (Grant No.51605144).

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Received: 2018-01-04
Accepted: 2018-07-30
Published Online: 2018-10-16
Published in Print: 2019-02-25

© 2019 Walter de Gruyter GmbH, Berlin/Boston

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

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  76. Novel Combined Feeding Approach to Produce Quality Al6061 Composites for Heat Sinks
  77. Research Article
  78. Micromorphology change and microstructure of Cu-P based amorphous filler during heating process
  79. Controlling residual stress and distortion of friction stir welding joint by external stationary shoulder
  80. Research on the ingot shrinkage in the electroslag remelting withdrawal process for 9Cr3Mo roller
  81. Production of Mo2NiB2 Based Hard Alloys by Self-Propagating High-Temperature Synthesis
  82. The Morphology Analysis of Plasma-Sprayed Cast Iron Splats at Different Substrate Temperatures via Fractal Dimension and Circularity Methods
  83. A Comparative Study on Johnson–Cook, Modified Johnson–Cook, Modified Zerilli–Armstrong and Arrhenius-Type Constitutive Models to Predict Hot Deformation Behavior of TA2
  84. Dynamic absorption efficiency of paracetamol powder in microwave drying
  85. Preparation and Properties of Blast Furnace Slag Glass Ceramics Containing Cr2O3
  86. Influence of unburned pulverized coal on gasification reaction of coke in blast furnace
  87. Effect of PWHT Conditions on Toughness and Creep Rupture Strength in Modified 9Cr-1Mo Steel Welds
  88. Role of B2O3 on structure and shear-thinning property in CaO–SiO2–Na2O-based mold fluxes
  89. Effect of Acid Slag Treatment on the Inclusions in GCr15 Bearing Steel
  90. Recovery of Iron and Zinc from Blast Furnace Dust Using Iron-Bath Reduction
  91. Phase Analysis and Microstructural Investigations of Ce2Zr2O7 for High-Temperature Coatings on Ni-Base Superalloy Substrates
  92. Combustion Characteristics and Kinetics Study of Pulverized Coal and Semi-Coke
  93. Mechanical and Electrochemical Characterization of Supersolidus Sintered Austenitic Stainless Steel (316 L)
  94. Synthesis and characterization of Cu doped chromium oxide (Cr2O3) thin films
  95. Ladle Nozzle Clogging during casting of Silicon-Steel
  96. Thermodynamics and Industrial Trial on Increasing the Carbon Content at the BOF Endpoint to Produce Ultra-Low Carbon IF Steel by BOF-RH-CSP Process
  97. Research Article
  98. Effect of Boundary Conditions on Residual Stresses and Distortion in 316 Stainless Steel Butt Welded Plate
  99. Numerical Analysis on Effect of Additional Gas Injection on Characteristics around Raceway in Melter Gasifier
  100. Variation on thermal damage rate of granite specimen with thermal cycle treatment
  101. Effects of Fluoride and Sulphate Mineralizers on the Properties of Reconstructed Steel Slag
  102. Effect of Basicity on Precipitation of Spinel Crystals in a CaO-SiO2-MgO-Cr2O3-FeO System
  103. Review Article
  104. Exploitation of Mold Flux for the Ti-bearing Welding Wire Steel ER80-G
  105. Research Article
  106. Furnace heat prediction and control model and its application to large blast furnace
  107. Effects of Different Solid Solution Temperatures on Microstructure and Mechanical Properties of the AA7075 Alloy After T6 Heat Treatment
  108. Study of the Viscosity of a La2O3-SiO2-FeO Slag System
  109. Tensile Deformation and Work Hardening Behaviour of AISI 431 Martensitic Stainless Steel at Elevated Temperatures
  110. The Effectiveness of Reinforcement and Processing on Mechanical Properties, Wear Behavior and Damping Response of Aluminum Matrix Composites
https://doi.org/10.1515/htmp-2018-0002
Keywords for this article
titanium alloy; vertical centrifugal casting; bubble migration; hydraulic simulation
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Articles in the same Issue

  1. Frontmatter
  2. Review Article
  3. Research on the Influence of Furnace Structure on Copper Cooling Stave Life
  4. Influence of High Temperature Oxidation on Hydrogen Absorption and Degradation of Zircaloy-2 and Zr 700 Alloys
  5. Correlation between Travel Speed, Microstructure, Mechanical Properties and Wear Characteristics of Ni-Based Hardfaced Deposits over 316LN Austenitic Stainless Steel
  6. Factors Influencing Gas Generation Behaviours of Lump Coal Used in COREX Gasifier
  7. Experiment Research on Pulverized Coal Combustion in the Tuyere of Oxygen Blast Furnace
  8. Phosphate Capacities of CaO–FeO–SiO2–Al2O3/Na2O/TiO2 Slags
  9. Microstructure and Interface Bonding Strength of WC-10Ni/NiCrBSi Composite Coating by Vacuum Brazing
  10. Refill Friction Stir Spot Welding of Dissimilar 6061/7075 Aluminum Alloy
  11. Solvothermal Synthesis and Magnetic Properties of Monodisperse Ni0.5Zn0.5Fe2O4 Hollow Nanospheres
  12. On the Capability of Logarithmic-Power Model for Prediction of Hot Deformation Behavior of Alloy 800H at High Strain Rates
  13. 3D Heat Conductivity Model of Mold Based on Node Temperature Inheritance
  14. 3D Microstructure and Micromechanical Properties of Minerals in Vanadium-Titanium Sinter
  15. Effect of Martensite Structure and Carbide Precipitates on Mechanical Properties of Cr-Mo Alloy Steel with Different Cooling Rate
  16. The Interaction between Erosion Particle and Gas Stream in High Temperature Gas Burner Rig for Thermal Barrier Coatings
  17. Permittivity Study of a CuCl Residue at 13–450 °C and Elucidation of the Microwave Intensification Mechanism for Its Dechlorination
  18. Study on Carbothermal Reduction of Titania in Molten Iron
  19. The Sequence of the Phase Growth during Diffusion in Ti-Based Systems
  20. Growth Kinetics of CoB–Co2B Layers Using the Powder-Pack Boriding Process Assisted by a Direct Current Field
  21. High-Temperature Flow Behaviour and Constitutive Equations for a TC17 Titanium Alloy
  22. Research on Three-Roll Screw Rolling Process for Ti6Al4V Titanium Alloy Bar
  23. Continuous Cooling Transformation of Undeformed and Deformed High Strength Crack-Arrest Steel Plates for Large Container Ships
  24. Formation Mechanism and Influence Factors of the Sticker between Solidified Shell and Mold in Continuous Casting of Steel
  25. Casting Defects in Transition Layer of Cu/Al Composite Castings Prepared Using Pouring Aluminum Method and Their Formation Mechanism
  26. Effect of Current on Segregation and Inclusions Characteristics of Dual Alloy Ingot Processed by Electroslag Remelting
  27. Investigation of Growth Kinetics of Fe2B Layers on AISI 1518 Steel by the Integral Method
  28. Microstructural Evolution and Phase Transformation on the X-Y Surface of Inconel 718 Ni-Based Alloys Fabricated by Selective Laser Melting under Different Heat Treatment
  29. Characterization of Mn-Doped Co3O4 Thin Films Prepared by Sol Gel-Based Dip-Coating Process
  30. Deposition Characteristics of Multitrack Overlayby Plasma Transferred Arc Welding on SS316Lwith Co-Cr Based Alloy – Influence ofProcess Parameters
  31. Elastic Moduli and Elastic Constants of Alloy AuCuSi With FCC Structure Under Pressure
  32. Effect of Cl on Softening and Melting Behaviors of BF Burden
  33. Effect of MgO Injection on Smelting in a Blast Furnace
  34. Structural Characteristics and Hydration Kinetics of Oxidized Steel Slag in a CaO-FeO-SiO2-MgO System
  35. Optimization of Microwave-Assisted Oxidation Roasting of Oxide–Sulphide Zinc Ore with Addition of Manganese Dioxide Using Response Surface Methodology
  36. Hydraulic Study of Bubble Migration in Liquid Titanium Alloy Melt during Vertical Centrifugal Casting Process
  37. Investigation on Double Wire Metal Inert Gas Welding of A7N01-T4 Aluminum Alloy in High-Speed Welding
  38. Oxidation Behaviour of Welded ASTM-SA210 GrA1 Boiler Tube Steels under Cyclic Conditions at 900°C in Air
  39. Study on the Evolution of Damage Degradation at Different Temperatures and Strain Rates for Ti-6Al-4V Alloy
  40. Pack-Boriding of Pure Iron with Powder Mixtures Containing ZrB2
  41. Evolution of Interfacial Features of MnO-SiO2 Type Inclusions/Steel Matrix during Isothermal Heating at Low Temperatures
  42. Effect of MgO/Al2O3 Ratio on Viscosity of Blast Furnace Primary Slag
  43. The Microstructure and Property of the Heat Affected zone in C-Mn Steel Treated by Rare Earth
  44. Microwave-Assisted Molten-Salt Facile Synthesis of Chromium Carbide (Cr3C2) Coatings on the Diamond Particles
  45. Effects of B on the Hot Ductility of Fe-36Ni Invar Alloy
  46. Impurity Distribution after Solidification of Hypereutectic Al-Si Melts and Eutectic Al-Si Melt
  47. Induced Electro-Deposition of High Melting-Point Phases on MgO–C Refractory in CaO–Al2O3–SiO2 – (MgO) Slag at 1773 K
  48. Microstructure and Mechanical Properties of 14Cr-ODS Steels with Zr Addition
  49. A Review of Boron-Rich Silicon Borides Basedon Thermodynamic Stability and Transport Properties of High-Temperature Thermoelectric Materials
  50. Siliceous Manganese Ore from Eastern India:A Potential Resource for Ferrosilicon-Manganese Production
  51. A Strain-Compensated Constitutive Model for Describing the Hot Compressive Deformation Behaviors of an Aged Inconel 718 Superalloy
  52. Surface Alloys of 0.45 C Carbon Steel Produced by High Current Pulsed Electron Beam
  53. Deformation Behavior and Processing Map during Isothermal Hot Compression of 49MnVS3 Non-Quenched and Tempered Steel
  54. A Constitutive Equation for Predicting Elevated Temperature Flow Behavior of BFe10-1-2 Cupronickel Alloy through Double Multiple Nonlinear Regression
  55. Oxidation Behavior of Ferritic Steel T22 Exposed to Supercritical Water
  56. A Multi Scale Strategy for Simulation of Microstructural Evolutions in Friction Stir Welding of Duplex Titanium Alloy
  57. Partition Behavior of Alloying Elements in Nickel-Based Alloys and Their Activity Interaction Parameters and Infinite Dilution Activity Coefficients
  58. Influence of Heating on Tensile Physical-Mechanical Properties of Granite
  59. Comparison of Al-Zn-Mg Alloy P-MIG Welded Joints Filled with Different Wires
  60. Microstructure and Mechanical Properties of Thick Plate Friction Stir Welds for 6082-T6 Aluminum Alloy
  61. Research Article
  62. Kinetics of oxide scale growth on a (Ti, Mo)5Si3 based oxidation resistant Mo-Ti-Si alloy at 900-1300∘C
  63. Calorimetric study on Bi-Cu-Sn alloys
  64. Mineralogical Phase of Slag and Its Effect on Dephosphorization during Converter Steelmaking Using Slag-Remaining Technology
  65. Controllability of joint integrity and mechanical properties of friction stir welded 6061-T6 aluminum and AZ31B magnesium alloys based on stationary shoulder
  66. Cellular Automaton Modeling of Phase Transformation of U-Nb Alloys during Solidification and Consequent Cooling Process
  67. The effect of MgTiO3Adding on Inclusion Characteristics
  68. Cutting performance of a functionally graded cemented carbide tool prepared by microwave heating and nitriding sintering
  69. Creep behaviour and life assessment of a cast nickel – base superalloy MAR – M247
  70. Failure mechanism and acoustic emission signal characteristics of coatings under the condition of impact indentation
  71. Reducing Surface Cracks and Improving Cleanliness of H-Beam Blanks in Continuous Casting — Improving continuous casting of H-beam blanks
  72. Rhodium influence on the microstructure and oxidation behaviour of aluminide coatings deposited on pure nickel and nickel based superalloy
  73. The effect of Nb content on precipitates, microstructure and texture of grain oriented silicon steel
  74. Effect of Arc Power on the Wear and High-temperature Oxidation Resistances of Plasma-Sprayed Fe-based Amorphous Coatings
  75. Short Communication
  76. Novel Combined Feeding Approach to Produce Quality Al6061 Composites for Heat Sinks
  77. Research Article
  78. Micromorphology change and microstructure of Cu-P based amorphous filler during heating process
  79. Controlling residual stress and distortion of friction stir welding joint by external stationary shoulder
  80. Research on the ingot shrinkage in the electroslag remelting withdrawal process for 9Cr3Mo roller
  81. Production of Mo2NiB2 Based Hard Alloys by Self-Propagating High-Temperature Synthesis
  82. The Morphology Analysis of Plasma-Sprayed Cast Iron Splats at Different Substrate Temperatures via Fractal Dimension and Circularity Methods
  83. A Comparative Study on Johnson–Cook, Modified Johnson–Cook, Modified Zerilli–Armstrong and Arrhenius-Type Constitutive Models to Predict Hot Deformation Behavior of TA2
  84. Dynamic absorption efficiency of paracetamol powder in microwave drying
  85. Preparation and Properties of Blast Furnace Slag Glass Ceramics Containing Cr2O3
  86. Influence of unburned pulverized coal on gasification reaction of coke in blast furnace
  87. Effect of PWHT Conditions on Toughness and Creep Rupture Strength in Modified 9Cr-1Mo Steel Welds
  88. Role of B2O3 on structure and shear-thinning property in CaO–SiO2–Na2O-based mold fluxes
  89. Effect of Acid Slag Treatment on the Inclusions in GCr15 Bearing Steel
  90. Recovery of Iron and Zinc from Blast Furnace Dust Using Iron-Bath Reduction
  91. Phase Analysis and Microstructural Investigations of Ce2Zr2O7 for High-Temperature Coatings on Ni-Base Superalloy Substrates
  92. Combustion Characteristics and Kinetics Study of Pulverized Coal and Semi-Coke
  93. Mechanical and Electrochemical Characterization of Supersolidus Sintered Austenitic Stainless Steel (316 L)
  94. Synthesis and characterization of Cu doped chromium oxide (Cr2O3) thin films
  95. Ladle Nozzle Clogging during casting of Silicon-Steel
  96. Thermodynamics and Industrial Trial on Increasing the Carbon Content at the BOF Endpoint to Produce Ultra-Low Carbon IF Steel by BOF-RH-CSP Process
  97. Research Article
  98. Effect of Boundary Conditions on Residual Stresses and Distortion in 316 Stainless Steel Butt Welded Plate
  99. Numerical Analysis on Effect of Additional Gas Injection on Characteristics around Raceway in Melter Gasifier
  100. Variation on thermal damage rate of granite specimen with thermal cycle treatment
  101. Effects of Fluoride and Sulphate Mineralizers on the Properties of Reconstructed Steel Slag
  102. Effect of Basicity on Precipitation of Spinel Crystals in a CaO-SiO2-MgO-Cr2O3-FeO System
  103. Review Article
  104. Exploitation of Mold Flux for the Ti-bearing Welding Wire Steel ER80-G
  105. Research Article
  106. Furnace heat prediction and control model and its application to large blast furnace
  107. Effects of Different Solid Solution Temperatures on Microstructure and Mechanical Properties of the AA7075 Alloy After T6 Heat Treatment
  108. Study of the Viscosity of a La2O3-SiO2-FeO Slag System
  109. Tensile Deformation and Work Hardening Behaviour of AISI 431 Martensitic Stainless Steel at Elevated Temperatures
  110. The Effectiveness of Reinforcement and Processing on Mechanical Properties, Wear Behavior and Damping Response of Aluminum Matrix Composites
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