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The Morphology Analysis of Plasma-Sprayed Cast Iron Splats at Different Substrate Temperatures via Fractal Dimension and Circularity Methods

  • Qiulan Wei , Li He , Zhang Liu , Xiao Feng and Ya-Zhe Xing EMAIL logo
Published/Copyright: July 29, 2019
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High Temperature Materials and Processes
From the journal High Temperature Materials and Processes Volume 38 Issue 2019

Abstract

Plasma-sprayed cast iron splats were deposited onto polished aluminum substrates preheated to different temperatures ranging from 25°C to 250°C. The morphology of single splat was observed by a field emission scanning electron microscope. Quantitative characterization methods, including fractal dimension (FD) and circularity analyses of the splat profile, were employed to identify the difference in morphology of the splats with the change of the substrate temperature. The results showed that the substrate temperature has a significant effect on the spreading of molten droplets and the morphology of resultant splats through changing the solidification rate of the droplets. With the increment of substrate temperature, the homogeneous and sufficient spreading of the droplets resulted from low solidification rate reduces the splashing of the droplets. In addition, the evaporation of adsorbed moisture on the substrate improves the wettability between the spreading droplet and the substrate, then benefits the homogeneous spreading of the molten droplet. As a result, a distinct decline in the FD value was observed. It was also suggested that the FD analysis could be used to characterize the morphology of the splat more effectively while the circularity method was heavily dependent on the area of the splat.

Keywords: substrate temperature;; splat morphology;; fractal dimension;; circularity

Introduction

In the field of mechanical manufacturing, atmospheric plasma spray technique has been widely used to prepare metallic and ceramic coatings on mechanical parts to protect the parts surfaces from abrasion, corrosion and heat [1, 2, 3, 4]. It is well known that the plasma-sprayed coatings are built-up by a stream of molten particles which coalesce and solidify after impacting on rough substrate or solidified coatings. It was also confirmed that the formation of a splat is nearly independent [5]. Obviously, the formation of individual splat has great effect on the properties of the coatings, and then affects the lifetime of machinery parts.

As reported up to now, there are lots of factors, including the spray conditions [6, 7], the spray materials [8], the substrate oxidation [6, 8], the roughness [9, 10, 11] of the substrate surface and the wetting of droplet to substrate surface [6, 8], that could influence the splat formation. Small changes in these factors may lead to the large differences in the morphology of the splats, the splat–substrate bonding, the microstructure of the coating and the residual stress in the coating [12, 13], and then dramatically influence the properties of the obtained coatings. Our previous work [14] showed that the metallurgical bond between the cast iron splat and the aluminum substrate appeared when the initial substrate temperature exceeded 190°C. Yang et al. [15, 16] investigated the influence of ambient pressure on splat formation. They found that the splat shape changed to the disk-like shape with the reduction of the ambient pressure, resulting in a significant increase in the adhesion strength. Sakakibara et al. [17] studied the plasma-sprayed yttria-stabilized zirconia particles on a polished stainless steel surface and confirmed that the transition to disk-like splats occurred at a substrate temperature range of 150–200°C. When the temperature of the substrate exceeds this transition temperature, the coating consists of a large proportion of disk-like splats and shows a significant increase in adhesion strength. Generally, the splat forms two morphologies during spraying, one presents a disk-like shape and the other behaves as a splashed splat which deteriorates the quality of the coating. In general, the splashing occurs during the spreading of a droplet even on a flat surface at ambient atmosphere, leading to the formation of an irregular splat [8]. Many studies have been done on the correlation between the properties of the coating and the shape of the splats [18, 19, 20, 21]. All these works suggest that the occurrence of the splashed splats goes against the formation of the good splat–substrate or inter-splat bonding, as well as the adhesion or cohesion strength. The splat–substrate adhesion determines the adhesive strength of the coating, while the inter-splat interface bonding dominates the cohesion strength of the coating. Thereby, if all the first-layer splats adhere to the substrate and the inter-splat bonding is excellent, then the enhancements in both the adhesion strength and the cohesion strength can be expected. On the contrary, the poor adhesion between the splat and the substrate produces when the splashed splats form on the surface of the substrate, because the positions where the splash fingers formed will act as the weak bonding sites [15]. Moreover, the weak bonding sites between the splats lead to a decreased cohesion of the coating by weakening the inter-splat bonding.

In conclusion, the morphology of the splats affects the microstructure of the coating, and then affects the performance of the coating. Therefore, it is significant to employ some feature parameters to quantitatively characterize the morphology of the splat. These parameters can establish some quantitative relationships, such as the relationship between the spray parameters and the splat morphology and the relationship between the splat morphology and the properties of the coating. That is to say, a quantitative description of the splat morphology can contribute to establishing a quantitative relationship between the spray parameters and the coating properties. Chen et al. [22] employed the image analysis method to identify the splat in the field emission scanning electron microscope (FESEM) image. The fractal dimension (FD) and the solidity were used to quantitatively characterize the morphology of the splat. Kang et al. [23] defined the aspect ratio and the fractional factor to investigate the influence of the impacting angle on the spreading and the solidification behaviors of a molten droplet. The results showed that both the aspect ratio and the fractional factor increase with the increase in the inclination angle of the substrate. Mulero et al. [24] developed an image inspection system to characterize the splat in terms of its area, perimeter, circularity, eccentricity and solidity, which can quantify the morphology of a thermally sprayed splat.

In the present work, polished aluminum substrates were preheated to different temperatures, then the cast iron splats were plasma-sprayed onto the preheated substrate surface. The morphologies of the splats were quantitatively characterized by the circularity and the FD of the splat periphery. The effect of the substrate temperature on the geometric parameters (circularity and FD) of plasma-sprayed splats was investigated.

Experimental process

Materials and preparation of individual splats

Commercially available Fe-4.1C-1.5Si-1.5B-36.6Cr (in weight percentage) powder (DG.Fe-05, Chengdu Daguang Thermal Spraying Materials Co. Ltd., China) was used as the starting powder The powder consists of spherical particles with a range in size from 20 to 75 μm (as shown in Figure 1). A commercial plasma spray system (GP-80, Aerospace Research Institute of Materials & Processing Technology, China) was employed to deposit the cast iron splats. Pure aluminum disks (99.7%, 20 mm in diameter, 4 mm in thickness) were used as the substrate. Before spraying, all aluminum disks were mirror-polished until their surface roughness (Ra) reached about 0.03 μm, which was measured by a surface roughmeter (TR-240, Beijing Time Group, China). The traverse speed of the plasma torch was fixed at 1,200 mm/s. The flow rate of the powder was fixed at 4 L/min. The substrate was preheated by the plasma jet without carrying powders, and the preheating temperature was monitored using a pyrometer (RAYRPM30L3U, Raytek, USA). When the temperature of the substrate surface reached a set value shown in Table 1, the powders were immediately carried into plasma jet. Table 1 lists all the spray parameters for the deposition of the cast iron splats on the aluminum surface. Obviously, in addition to the difference of the substrate temperature, other preparation conditions for all samples were identical.

Figure 1: The morphology of the feedstock powders.
Figure 1:

The morphology of the feedstock powders.

Table 1:

Spray parameters for the deposition of cast iron splats on the aluminum surface.

SampleArc power (kW)Spray distance (mm)Gas flow rate (L/min)Substrate temperate (°C)
ArH2
A3080326.325 ± 2
B3080326.3150 ± 8
C3080326.3250 ± 10

Morphology and geometric parameters of individual splats

After spraying, the morphology of the splats deposited under different conditions was observed by a commercial FESEM (S-4800, Hitachi, Japan). For each sample, ten images of individual splats were obtained with a resolution of 1,024 × 768 pixels and 24-bits per pixel. The magnification of all selected images is 500×. The calculation process of the geometric parameters of single splat contains the following steps: (1) image denoising, (2) binarization processing, (3) Canny algorithm edge detection, (4) FD calculation of the splat periphery using the box-counting method, (5) circularity calculation of the same splat after the FD calculation. All calculations were conducted with a commercially available software, MATLAB R2014. As reported by Ding and Goshtasby [25], the object boundaries in the image can be obtained by a Canny edge detector. The Canny edge detector classifies a pixel as an edge if the gradient magnitude of the pixel is larger than those of the pixels at both its sides in the direction of the maximum intensity change. Therefore, we used the Canny edge detector to obtain the boundaries of the splat. In the process of edge detection, the splashed parts produced during the spreading of the molten droplet were removed because they were not connected to the main part of the splat.

Circularity specifies the relationship between the area and the perimeter of a splat (see eq. (1) [24]) and signifies the degree of approximation of a splat to a circle. Furthermore, area is calculated by adding the actual number of pixels in the region. Perimeter is defined as the distance around the periphery of the region, and it is measured by calculating the distance between each adjoining pair of the pixels around the border of the region.

(1)Circularity=4π⋅AreaPerimeter 2

The FD was utilized to quantitatively describe the complexity of the periphery of a splat. A box-counting method was employed to evaluate the FD. In the process of the box-counting method, a series of squares were used to cover the profile of a splat. The relationship between the square size ε and the number of the squares N(ε) can be expressed as [26]:

(2)Nε∝ε−D

where D is the FD of the periphery of a splat, which can be calculated by the linear regression given as [26]:

(3)logNε=−Dlogε+C

Results and discussion

Effect of substrate temperature on geometric parameters of the splats

Figure 2 shows the changes in the FD and the circularity of the splats. With the increment of the substrate temperature, the FD decreased and the circularity increased. When the substrate temperature was 25 ± 2°C, the FD was 1.3201 ± 0.0359 and the circularity was 0.3001 ± 0.0880. As the substrate temperature increased from 25 ± 2°C to 150 ± 8°C, the FD decreased to 1.2348 ± 0.0509 and the circularity increased to 0.5693 ± 0.1493. These changes in the FD and the circularity can be reasonably explained by the evaporated gas-induced splashing model [27]. The substrate surface was easy to be covered by the adsorbates when the substrate temperature remained at room temperature. During the deposition process of the droplet, the substrate surface was heated rapidly by the impacting droplets. As a result, the adsorbates gasified and evaporated from the substrate surface. Then, the air flow generated by the evaporation gas induced the splashing, which increased the complexity of the splat periphery (see Figure 3(a)). As a result, the FD reached the maximum value. As mentioned in the “Morphology and geometric parameters of individual splats” section, the circularity represents the degree of approximation of a splat to a circle. However, a splat is close to a circle, indicating the homogeneous spreading of the molten droplet. Uniform spreading of a molten droplet reduces the complexity of the periphery of the resultant splat, leading to the reduction in the FD value. When the substrate was preheated to 150 ± 8°C, the adsorbates on the substrate surface were evaporated and removed. Consequently, the wettability of the molten droplet on the substrate surface was improved [28], resulting in a relatively uniform spreading of the droplet and the formation of a splat with restrained splash (see Figure 3(b)). This eventually caused the decrease in the FD and the increase in the circularity of the splats. Interestingly, at this temperature (150 ± 8°C), the ranges of the values in the FD and the circularity were much greater than those of the samples prepared at room temperature and 250 ± 10°C. In accordance with the previous report [27], when the substrate was preheated to a temperature above the boiling point of the adsorbates, the obtained splat presented a disk shape. In the present work, all samples were polished in a pollution-free environment. This indicates the adsorbates on the surface of the substrate should be mainly water. That is to say, when the substrate was preheated to above 100°C (boiling point of water), the spreading of the droplets was more homogeneous due to the evaporation of water adsorbed on the substrate surface.

Figure 2: The changes in the FD (a) and the circularity (b) of the splats with the substrate temperature.
Figure 2:

The changes in the FD (a) and the circularity (b) of the splats with the substrate temperature.

Figure 3: Typical splat deposited on the substrate preheated to (a) 25±2°C, (b) 150±8°C and (c) 250±10°C. The left micrographs are FESEM images and the right micrographs are the corresponding images after Canny algorithm edge detection.
Figure 3:

Typical splat deposited on the substrate preheated to (a) 25±2°C, (b) 150±8°C and (c) 250±10°C. The left micrographs are FESEM images and the right micrographs are the corresponding images after Canny algorithm edge detection.

As the substrate temperature further increased to 250 ± 10°C, the FD decreased continuously and the circularity increased continuously. With preheating the substrate to a higher temperature, the cooling rate of the droplets decreased due to the reduced temperature difference between the droplet and the substrate and the oxidation of the substrate surface [14], delaying the solidification of the spreading droplets and then causing the homogeneous and sufficient spreading of the droplets. As a consequence, a regular disk splat was expected (see Figure 3(c)) and both the minimum FD value and the maximum circularity value were obtained in the present temperature range.

Comparison of the FD and the circularity

Relationship between the FD and the circularity

As mentioned in the “Effect of substrate temperature on geometric parameters of the splats” section, both a higher FD and a lower circularity correspond to an irregular splash splat. This indicates a potential relationship between the FD and the circularity. Therefore, we chose 30 splats (ten splats for each sample) to plot the relationship between the FD and the circularity of them, as shown in Figure 4. Meanwhile, the linear fitting of the data was also conducted. Apparently, there was a negative linear correlation between the FD and the circularity due to the high linear fitting correlation coefficient (R = 0.9772).

Figure 4: Relationship between the FD and the circularity of the splats.
Figure 4:

Relationship between the FD and the circularity of the splats.

As mentioned in the “Morphology and geometric parameters of individual splats” section, the circularity signifies the degree of approximation of a splat to a circle, and the FD describes the complexity of the periphery of a splat. Despite the difference in the concepts of two geometric parameters, a strong correlation exists between them (see Figure 4). This is related to the formation mechanism of the splats. Figure 5 shows the schematic diagrams of forming processes of two typical splats with different morphologies. In Figure 5, the arrows signify the spreading direction of the melts, and the length of the arrows represents the spreading speed. When the spreading speeds of the droplet in different directions are identical, a disk splat (see Figure 4(a)), which is close to a circle without complex periphery, is prone to form. Inversely, when the spreading speeds of the droplet in all directions are different, a splash-shaped splat (see Figure 4(b)), which possesses an irregular shape with complex periphery, is easy to form. That is to say, the FD and the circularity are consistent in characterizing the morphology of a plasma-sprayed splat. High circularity of a splat signifies a uniform spreading of the molten droplet, which leads to the reductions in the complexity and the FD value of the resultant splat.

Figure 5: Schematic diagrams of the forming processes of typical morphologies of two splats. The left images present the morphologies of the splats at an early stage of spreading, while the right images present the morphologies of final splats.
Figure 5:

Schematic diagrams of the forming processes of typical morphologies of two splats. The left images present the morphologies of the splats at an early stage of spreading, while the right images present the morphologies of final splats.

Applicability of the circularity

According to the previous analyses, there was a negative correlation between the FD and the circularity (see the fitted line in Figure 4). However, some outliers in the data of individual splats were far away from the straight line. Moreover, these outliers were concentrated in a circularity range of 0.2586–0.5976 and a FD range of 1.2412–1.2918, which were marked by the dotted square box in Figure 4. This indicates that the values in this small range do not fit the straight line. Therefore, in this range, two typical splats (see Figure 3(a) and 3(b), marked by SP1 and SP2 respectively) were selected from sample A and sample B to reveal the changes in the FD and the circularity of the splats. The corresponding values were listed in Table 2. It was found that the FD values of two splats were approximately identical, while the circularity of SP2 was about twice that of SP1. Furthermore, the area of SP2 was 3.7 times that of SP1, and the perimeter of SP2 was 1.4 times that of SP1. These indicate that the area of the splat seriously affects the circularity value. Even if the complexities of the peripheries of two splats were approximately similar, the circularity value increased significantly with the increase in the area of the splat. Generally, the area of the splat is determined by both the particle size of the starting powder and the spreading of the molten droplet. With a certain flattening ratio, thereby, the particle size of the starting powder will be the main factor affecting the area of the splat. As for the present work, the size of the powder used ranges from 20 to 75 μm. Such a wide range of particle size makes the final area of the splat different, leading to a wide range of the circularity value. Therefore, in order to use the circularity to characterize the morphology of the splats, a small difference in the size of the starting powders is required. The comparability in the circularity is only valid for the powders with comparable sizes. In contrast with the circularity, the FD is more suitable for characterizing the morphology of the splats with different sizes.

Table 2:

The main parameters of two splats.

SplatSubstrate temperate (°C)FDCircularityArea (μm2)Perimeter (μm)
SP125±2°C1.28430.25862,162.5104324.0847
SP2150±8°C1.27180.49827,923.0043446.9282

Conclusions

Individual cast iron splats were prepared on the mirror-polished aluminum substrates preheated to different temperatures. The morphologies of the resultant splats were quantitatively characterized by both the FD and the circularity. With increasing the preheating temperature, the FD value of the splats decreased and the circularity value increased. For the splats deposited at room temperature, a maximum FD value, which corresponded to a complex periphery of the splats, was acquired due to the strong splashing of the droplet induced by the evaporation of the adsorbed moisture on the substrate surface. With preheating the substrate to 150 ± 8°C, most of the water on the substrate surface was removed at a high temperature and the wettability between the droplet and the substrate surface was improved. This caused the homogeneous spreading of the droplet and consequently led to a reduced FD value. When the substrate was further preheated to 250 ± 10°C, the homogeneous and sufficient spreading of the droplet caused by lower solidification rate significantly suppressed the splashing of the droplet. As a result, the FD value decreased while the circularity increased accordingly.

Compared with the circularity, the FD was more excellent in characterizing the morphology of splat. The FD and the circularity were intrinsically consistent when using them to characterize the morphology of the splat. However, the circularity is heavily dependent on the area of the splat. Therefore, reducing the size difference of the original powders can enhance the applicability of the circularity in characterizing the morphology of the splats.

Funding statement: This work was supported by the Special Scientific Research Project of Shaanxi Provincial Department of Education (18JK0081).

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Received: 2018-08-24
Accepted: 2018-12-05
Published Online: 2019-07-29
Published in Print: 2019-02-25

© 2019 Wei et al., published by De Gruyter

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

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  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-2019-0021
Keywords for this article
substrate temperature;; splat morphology;; fractal dimension;; circularity
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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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