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Cellular Automaton Modeling of Phase Transformation of U-Nb Alloys during Solidification and Consequent Cooling Process

  • Qingfu Tang , Dong Chen , Bin Su EMAIL logo , Xiaopeng Zhang , Hongzhang Deng and Zhenhong Wang
Published/Copyright: May 11, 2019
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High Temperature Materials and Processes
From the journal High Temperature Materials and Processes Volume 38 Issue 2019

Abstract

The microstructure evolution of U-Nb alloys during solidification and consequent cooling process was simulated using a cellular automaton (CA) model. By using this model, ϒ phase precipitation and monotectoid decomposition were simulated, and dendrite morphology of ϒ phase, Nb microsegregation and kinetics of monotectoid decomposition were obtained. To validate the model, an ingot of U-5.5Nb (wt.%) was produced and temperature measuring experiment was carried out. As-cast microstructure at different position taken from the ingot was investigated by using optical microscope and SEM. The effect of cooling rate on ϒ phase precipitation and monotectoid decomposition of U-Nb alloys was also studied. The simulated results were compared with the experimental results and the capability of the model for quantitatively predicting the microstructure evolution of U-Nb alloys during solidification and consequent cooling process was assessed.

Keywords: U-Nb alloys; dendrite growth; monotectoid decomposition; cellular automaton; numerical simulation

1 Introduction

Uranium is widely used in the nuclear industry, especially in nuclear power plants, because of its high density and unique nuclear properties [1–5]. However, the poor corrosion resistance limits its potential use. In industrial applications, niobium is always added to uranium for increased oxidation resistance and enhanced ductility [4]. Due to the structure heredity, as-cast microstructure is very important to its mechanical properties and the design of heat treatment process. The as-cast microstructure including the grain size and fraction of each phase as well as the composition distribution has a great influence on the heat treatment and final properties.However, less attention has been paid to the study of solidification process of U-Nb alloys compared with the research on heat treatment. Therefore, it is necessary to investigate microstructure evolution of U-Nb alloys during solidification process.

To date, there have only been a few published studies on phase transformation of U-Nb alloys during solidification and cooling process.Maet al. [6] investigated the solidification of U-2Nb alloy by means of microscope and SEM, and the behavior of the segregation and the precipitated phase were determined. Chen [7] produced U-5Nb alloy in CaO crucible with a protective coating by vacuum-induced melting. The solidifying microstructure was obtained by quenching method, and microstructural morphology and the type of inclusion were investigated. Jackson et al. [8] investigated the solidification microstructure and solute microsegregation of U-6Nb alloy. The results showed that the most difference of Nb concentration at the grain boundary and the grain interior was about 2.5Nb, and it is hard to eliminate them in subsequent heat treatment process. Chen et al. [5] investigated the effects of the carbon addition on the morphology, composition, size distribution and formation mechanism of inclusions in U-5.5Nb alloy. On the whole, little attention has been paid to the solidification process of U-Nb alloys and it is lack of in-depth understanding on solidification microstructure.

U-Nb alloys are expensive and also radioactive, which limits the experimental research. In recent years, a variety of computer models, such as cellular automaton (CA) [9– 16],Monte Carlo [17, 18] and phase field [19–21], have been developed to simulate the microstructure evolution of solidification process.However, due to the lack of experimental data, there was little study about the microstructure simulation of U-Nb alloys during solidification process. Li et al. [10] developed a two-dimensional CA model to simulate the dendrite morphology and microsegregation of U-6Nb alloy, and the dendrite growth and Nb microsegregation behavior was simulated. Su et al. [16] used a CA model to investigate the solidification microstructure and composition distribution of U-5.5Nb under different thermal conditions of cooling rate. Studies mentioned above focused on the nucleation and growth behaviors of primary phase of U-Nb alloys, while the monotectoid decomposition during the consequent cooling process was usually neglected. The results already known show slower cooling rates allow for Nb diffusion of increasing scale, and a lamellar structure associated with the monotectoid reaction occurs when the cooling rate is less than 0.2 K/s [3]. So, it is necessary to develop a model to simulate the through-process microstructure evolution of U-Nb alloys during solidification and consequent cooling process.

In this paper, a CA model has been developed to simulate the microstructure evolution of U-Nb alloys during solidification and consequent cooling process. By using the developed model, ϒ phase precipitation, Nb microsegregation behavior and monotectoid decomposition of U-Nb alloys were simulated, and the characteristic of solidified microstructure was predicted. Experiments were carried out, and the capability of the model for describing the microstructure evolution was discussed.

2 Model description

The phase diagram of U-Nb alloys is illustrated in Figure 1, and analysis of the solidification path was made with U-6Nb (U-14 at.%Nb) as an example. When T < TL (TL is liquidus temperature), the molten metal transforms into ϒ phase until this stage is complete. When the temperature reaches Tm (Tm is monotectoid temperature), the monotectoid decomposition, ϒ1→ α + ϒ2, occurs. The lamellar structure associated with the monotectoid microstructure nucleating at inclusions and prior-ϒ grain boundaries. In the present model, the dendrite growth process of ϒ phase, Nb microsegregation behavior and consequent monotectoid decomposition can be simulated, and the as-cast microstructure can be obtained.

Figure 1 The phase diagram of the U-Nb system reviewed by Koike et al. [1].
Figure 1

The phase diagram of the U-Nb system reviewed by Koike et al. [1].

The CA method was used in the simulation. A two-dimensional computational domain was discretized into square cells with the cell size of Δx. Each cell has the following variables: (1) grain identifying variable; (2) cell status, which is one of L, ϒ, M, and L/ϒ interface, where L is molten metal, ϒ phase precipitation from molten metal, M is monotectoid microstructure; (3) concentration (CL and CS); and (4) solid fraction (fS). The state of the cells can be identified as solid (fS = 1), liquid (fS = 0) and L/ϒ interface (0 < fS < 1). At the beginning of the simulation, each cell was given the same initial temperature above the liquidus of the alloy and all the cells were the liquid state. The state transformation from liquid to interface can be achieved through the following ways: stochastic nucleation event, artificially setting certain cell’s state as interface or captured by its neighboring solid cells [12]. The present model combines a continuous function CA description of grain growth with a finite difference (FD) computation of solute diffusion. Both the CA and FD components of the model run on the same regular spatial square grid and with the same time step. The temperature at each time-step was given by the cooling curve of the specimen,which was obtained either from a temperature simulation or from a temperature measurement. In order to simulate the microstructure evolution during solidification, the governing equations used to calculate the distribution of concentration and temperature, interface curvature, growth kinetics, solid fraction, and nucleation process will be described below.

3 The nucleation model

Nucleation process was described by a continuous Gaussian nucleation distribution model [22], and the total density of nuclei n(ΔT) at a given undercooling ΔT can be expressed as follows:

(1)nΔT=∫0ΔT1−fSolidΔT′dndΔT′dΔT′
(2)dnΔTdΔT′=Nmax2πΔTσexp−12ΔT′−ΔTNΔTσ2,

where ΔT is the undercooling, n(ΔT) is the nucleus density,Nmax is the maximum nucleus density, ΔTσ is the standard deviation of the distribution, ΔTN is the mean nucleation undercooling, ΔT′ is the undercooling integral element, and fSolid(ΔT′) is the fraction of solid phase.

When T < TL, the total ϒ phase nucleus density can be calculated by Eq. (1) and Eq. (2), and the total number of ϒ grains in the calculation domain can be obtained. The sites of newly formed ϒ phase nuclei are randomly selected from liquid cells and a random integer representing a new crystallization orientation is given to the orientation variable. The capture process for a cell begins only when the cell is selected as ϒ phase nucleus (or totally solidified), it will alter its surrounding liquid neighbors into L/ϒ interface state. In the CA model, the nearest four cells orthogonally (Von Neumann neighborhood) and the next nearest four cells diagonally (Moore neighborhood) are generally regarded as the neighboring cells,whose states will be changed with the parent cell in the center.

4 The solute diffusion

The growth process is mainly controlled by solute redistribution during solidification. Initially, the computational domain begins at a uniform composition, and as the solidification proceeds, the growing cells absorb solute from its neighboring liquid cells. Solute diffusion within the entire domain is then calculated based on the following equation:

(3)∂Ci∂t=∇⋅Di∇Ci+Ci1−k0∂fS∂t

where C is the composition with its subscript i denoting solid or liquid, D is the solute diffusion coefficient, and k0 is the solute partition coefficient.

5 The S/L interface growth kinetics

During solidification process, the solute diffusion plays an important role in determining the dendritic growth and microstructural characteristics. The local interface equilibrium composition at the interface can be calculated by the following equations:

(4)CL∗=C0+T∗−TL+ΔTR/mL
(5)CS∗=k0CL∗

where T* is the interface temperature, TL is the liquidus temperature, C*L and C*S are the equilibrium liquid and solid composition, respectively, C0 is the initial composition, ΔTR is the curvature undercooling, and mL is the slope of the liquidus line.

The curvature undercooling can be calculated by the following expression [9]:

(6)ΔTR=Γ1−15ϵ4φ−θ⋅K

where Г is the Gibbs–Thomson coefficient, ε is the degree of anisotropy of the interfacial energy, φ is the inclined angle of the normal to the interface with respect to the coordinate axis, θ is the angle between the preferred growth direction and the coordinate axis, and K is the curvature of the interface.

The average curvature for an interface cell is affected by its neighboring cells, and is calculated with the following expression [23]:

(7)K=1−2fS+∑i=1NfSi/N+1/Δx

where fS (i) and N are the solid fraction and the number of the neighboring cells. In the present model, N equals 8.

Solute conservation at the L/ϒ interface is given by [9]:

(8)vnCL∗(1−ko)=−DL∂CL∂x+∂CL∂y+DS∂CS∂x+∂CS∂y

where vn is the normal velocity of the interface.

The two-dimensional sketch of virtual front-tracking algorithm for orthogonal grid previously proposed was adopted in the present model [9, 13]. Figure 2 illustrates the process of virtual reconstruction of sharp S/L interface. The normal direction of each interfacial cell is determined by:

Figure 2 Schematic of the virtual front-tracking scheme [13].
Figure 2

Schematic of the virtual front-tracking scheme [13].

(9)n=−∇fS/||∇fS||=nxI+nyj

with i and j defining as the unit vectors along x-axis and y-axis, respectively. The length of the normal vector L is measured from the center of the interfacial cell along its normal direction and is proportional to the solid fraction fS:

(10)L=M⋅fS⋅Δx

where M denotes the coefficient to ensure the reconstructed interface continuous. The capturing rules are analyzed in detail in [9].

After calculating vn, the solid fraction increment of the interface in one time step Δt is calculated using the following equations [9]:

(11)ΔfS=vnΔtL
(12)L=Δxmax|cos⁡φ|,|sin⁡φ|,
(13)thenfSto+Δt=fSto+ΔfS,

where ΔfS is the increment of solid fraction, fSt0and fSt0+Δtare the solid fraction at the current time step and the next time step, respectively. When fS equals 1, the L/ϒ interface cell becomes solid and captures the neighboring liquid cells, and the captured cells change its state to L/ϒ interface.

6 The monotectoid transformation

With the temperature decreasing, the molten metal will transform into ϒ phase totally. The simulated prior-ϒ microstructure was used as the initial condition for simulation of monotectoid decomposition process. Monotectoid decomposition starts to nucleate at inclusions and prior-ϒ grain boundaries when the temperature drops to TM. In this work, the effect of inclusions was neglected in the simulation. It is assumed that the nucleation of monotectoid decomposition occurs at some sites on the prior-ϒ grain boundaries. Based on the classical nucleation theory, the nucleation model for monotectoid decomposition can be described as follows [24, 25]:

(14)I=K1DγkT−12exp−K2kTΔG2

where K1 is a constant related to the nucleation site density, K2 is a constant related to interface energy, Dϒ the niobium diffusion coefficient in ϒ phase, k is the Boltzmann’s constant, ΔG is the driving force for the nucleation of monotectoid decomposition. The nucleation density for monotectoid microstructure, nM, can be expressed as:

(15)nM=∫TTMIT′φT′dT′

where φ(T′) is the cooling rate.

The growth velocity of monotectoid decomposition, vϒ/M, can be calculated by [26]:

(16)vγ/M=aΔTM2exp−QRT

where ΔTM is undercooling of monotectoid transformation (ΔTM = TM − T), a is a parameter, R is the universal gas constant, Q is the activation energy for atom motion at the interface. In this work, a and Q were obtained by fitting the model to the experimental results reported in reference [27]. Once a ϒ phase cell changes monotectoid microstructure state, it will begin to grow into the prior-ϒ region at a uniform velocity. The radius of the monotectoid microstructure at time t, Rt, can be obtained:

(17)Rt=Rt−Δt+vγ/M∙Δt

where Rt−Δt is the radius at the previous step.

7 Results and discussion

7.1 The solidification microstructure

The nominal composition of the U-Nb alloys used in this study was 5.5wt.% high purity niobium and 94.5wt.% depleted uranium. The materials were melted in an arc melting furnace under vacuum up to 10 Pa at temperatures of about 1520∘C for 30 min, and then the liquid metal was

directly cast into ingots (100mm in diameter and 200mm in height). In order to investigate the influence of cooling rate on the as-cast microstructure of U-5.5Nb alloy, thermocouples were positioned at the top and the middle of the casting to measure the temperature variation during the solidification process. Samples for microstructure observation were taken from the position of the thermocouples. Standard metallographic techniques were adopted for grinding and polishing. The 5%H3PO4 aqueous solution was applied for electroetching and constant 2V DC

bias was used for the etching. The microstructure of U-Nb alloys was investigated by means of optical microscopy (OM) and scanning electron microscopy (SEM). The fraction of monotectoid decomposition was measured by using Image-pro Plus 6.0 (IPP 6.0) software.

Figure 3 shows the measured cooling curves at different positions inside the casting during solidification. It can be that the top position inside the casting cool faster than the middle position during solidification and consequent cooling process. As-cast microstructure of U-5.5Nb alloy at different position taken from the ingot were shown in Figure 4. Figures 4(a) and 4(c) show optical images of as-cast U-5.5Nb alloy at different positions where thermocouples were placed. Figures 4(b) and 4(d) show the corresponding high-magnification SEM images in high magnification. It can be seen that monotectoid decomposition (dark region in Figures 4(a) and 4(c), while bright region in Figures 4(b) and 4(d)) tends to occur at prior-ϒ grain boundaries and inclusions and it is consistent with the reported results.

Figure 3 The temperature change curves at different positions inside the casting during solidification.
Figure 3

The temperature change curves at different positions inside the casting during solidification.

Figure 4 Optical and SEM images of as-cast U-5.5Nb alloy at different position. (a) and (b) at top, (c) and (d) at middle.
Figure 4

Optical and SEM images of as-cast U-5.5Nb alloy at different position. (a) and (b) at top, (c) and (d) at middle.

7.2 The numerical simulation

The CA model was used to predict two-dimensional microstructure evolution of U-5.5Nb alloy. The computational domain was divided into 900×900 rectangular cells, and the cell size is 1μm. For the simulation the boundary was adiabatic so the heat flux and the atom flux are zero on the boundary. The parameters used in the simulation are shown in Table 1. The nucleation parameters were determined by adjusting simulated microstructure similar to actual microstructure. By using the measured cooling curves in Figure 3 and the developed model, the continuous microstructure evolution of U-5.5Nb alloy during solidification can be simulated, and the as-cast microstructure can be predicted.

Table 1

Properties of the U-5.5Nb alloys used in the following simulations.

Definition and symbolsvalues
Liquidus temperature TL (K)1633
Liquidus slope mL (K·wt.%−1)37.3
Maximum nucleus density Nmax (m−2)7.0×109
Standard deviation of the distribution ΔTσ (K)0.5
Mean nucleation undercooling ΔTN (K)5
Liquid diffusion coefficient DL (m2·s−1)1.05×10−9
Solid diffusion coefficient DS (m2·s−1)3.14×10−10
Partition coefficient k02.0
Gibbs-Thomson coefficient Г (K·m)1.9×10−7
Monotectoid temperature TM (K)920
Growth parameter for monotectoid transformation a (m·s−1·K−2)3.55×108
Activation energy Q (J·mol−1)338039

The simulated results of ϒ phase precipitation from liquid metal at different positions where thermocouples were placed inside the casting are shown in Figure 5 and Figure 6. Figure 5(a) and Figure 6(a) show the simulated dendrite morphology during solidification, where the white area represents liquid metal and different orientation ϒ grains are represented by different colors. Figure 5(b) and Figure 6(b) show the corresponding Nb concentration of U-5.5Nb alloy. Figures 5(c)-5(d) and Figures 6(c)-6(d) show the final microstructure and corresponding Nb concentration when the molten metal has transformed into ϒ phase totally. It can be seen that nucleation occurs in liquid with the lowering of temperature, and the dendrites will grow with the decreasing temperature until they meet each other. With the increase of the cooling rate, the average grain size decreases and the Nb microsegregation increases. The simulated ϒ phase microstructure can be used as the initial condition for simulation of monotectoid decomposition process.

Figure 5 The simulated microstructure (a, c) and corresponding Nb concentration (b, d) of U-5.5Nb alloy at the top of the casting during solidification process.
Figure 5

The simulated microstructure (a, c) and corresponding Nb concentration (b, d) of U-5.5Nb alloy at the top of the casting during solidification process.

Figure 6 The simulated microstructure (a, c) and corresponding Nb concentration (b, d) of U-5.5Nb alloy at the middle of the casting during solidification process.
Figure 6

The simulated microstructure (a, c) and corresponding Nb concentration (b, d) of U-5.5Nb alloy at the middle of the casting during solidification process.

The simulated microstructure of monotectoid decomposition at different positions where thermocouples were placed inside the casting is shown in Figure 7. The blue area denotes ϒ phase region, and the yellow region denotes monotectoid microstructure. It can be seen that monotectoid microstructure nucleate at ϒ grain boundaries and then grow into ϒ grain interior.With the proceeding of the transformation, more and more monotectoid microstructure form and the impingement appears. The calculated area fraction of monotectoid microstructure in Figures

Figure 7 The simulated microstructure of monotectoid decomposition at different positions. (a) at top, (b) at middle.
Figure 7

The simulated microstructure of monotectoid decomposition at different positions. (a) at top, (b) at middle.

Figure 8 The calculated kinetics of monotectoid decomposition at different positions.
Figure 8

The calculated kinetics of monotectoid decomposition at different positions.

7(a) and 7(b) are 22.4%and 49.7%, respectively,which is basically consistent with the experimental result in Figure 4. The results show that the fraction of monotectoid microstructure of as-cast microstructure of U-5.5Nb alloy decreases with the increase of the cooling rate. The calculated kinetics of monotectoid decomposition during cooling process is shown in Figure 8. It can be seen that the transformation rate increases at first and decreases gradually during the cooling process. The fraction of monotectoid microstructure at a given temperature decreases with the increase of the cooling rate. This is because the time for monotectoid decomposition is short with the increase of the cooling rate.

8 Conclusions

A cellular automaton model has been developed to simulate the microstructure evolution of U-Nb alloys during solidification and consequent cooling process. By using the developed model, nucleation and growth of ϒ phase, Nb microsegregation behavior and monotectoid decomposition of U-5.5Nb alloy were simulated. The evolution of dendrite morphology, Nb microsegregation behavior and kinetics of monotectoid decomposition under different cooling rate were obtained. The results showed that with the increase of the cooling rate, the average grain size of ϒ phase decreases and the Nb microsegregation increases. The fraction of monotectoid microstructure of as-cast microstructure decreases with the increase of the cooling rate. The transformation rate of monotectoid decomposition increases at first and decreases gradually during the cooling process, and the fraction of monotectoid microstructure at a given temperature decreases with the increase of the cooling rate. To validate the model, an ingot was produced and metallographic examination was carried out. It was shown that the simulated as-cast microstructure is in good agreement with the experimental result. The developed CA model can be used to simulate the microstructure evolution of U-Nb alloys during continuous cooling process and predict the final microstructure.

Acknowledgement

This work was financially supported by the Science and Technology Development Foundation of the Chinese Academy of Engineering Physics [grant number 2015B0203031], and the Science Challenge Program of China [grant number TZ20160040201].

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Received: 2018-11-27
Accepted: 2019-01-07
Published Online: 2019-05-11
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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  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
https://doi.org/10.1515/htmp-2019-0002
Keywords for this article
U-Nb alloys; dendrite growth; monotectoid decomposition; cellular automaton; numerical 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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