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Effect of adding yttrium on precipitation behaviors of inclusions in E690 ultra high strength offshore platform steel

  • Xiaojun Xi , Shaoying Li , Shufeng Yang EMAIL logo , Jingshe Li and Mengjing Zhao
Published/Copyright: October 2, 2020
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High Temperature Materials and Processes
From the journal High Temperature Materials and Processes Volume 39 Issue 1

Abstract

The mechanism of inclusions precipitation of the E690 offshore platform steel, with and without addition of yttrium, was studied using the thermodynamic calculation method. The results show that in the E690 steel in the absence of yttrium, the MnS inclusions were precipitated in the liquid phase at the solidification front. By adding the yttrium, MnS inclusions were replaced by spindle and spherical yttrium-containing oxide and sulfide complex inclusions, and the precipitation sequence of yttrium-containing inclusions in the liquid steel was Y2O3, Y2O2S, and YS. However, Y2S3 inclusions cannot be precipitated in the liquid steel under the experimental conditions. It was also found that Al2O3 inclusions can be formed in the liquid steel with and without addition of yttrium. The thermodynamic calculation results are in accordance with the experimental results.

Keywords: yttrium; E690 offshore platform steel; yttrium-containing inclusion; thermodynamic calculation

1 Introduction

The scientific exploration and exploitation of the ocean resources is now proceeding at a greatly accelerated rate [1]. Consequently, the offshore platform steel must possess high mechanical properties, excellent corrosion resistance, and high heat input welding performance. The generation of nonmetallic inclusions, inevitably occurring after the contact and reaction between the active elements in steel and the refractory materials and slags during the steelmaking and casting processes, reduces the properties of steel, such as strength, toughness, and corrosion resistance [2,3,4]. Therefore, it is important to control the inclusions as much as possible to avoid the deterioration of steel.

Several investigations have been carried out to control the inclusions in steel, and the main control methods include the elimination and the modification of inclusions. The elimination of inclusions in steel is the use of appropriate technology in the steelmaking process to remove inclusions from the liquid steel, and the main technologies include gas stirring [5,6,7], electromagnetic purification [8,9], slag washing [10], and filter technique [11]. The methods of inclusions modification include calcium (Ca) treatment [12,13,14,15], magnesium (Mg) treatment [16,17,18], calcium–magnesium treatment [19,20], and so on. Zhang et al. [16,17] reported that Mg has very strong thermodynamic affinities with oxygen and sulfur, and magnesia inclusions present a poor agglomeration character than alumina inclusions. However, Mg treatment can easily cause liquid steel spatter. Ca treatment is commonly used to modify high melting point Al2O3 inclusions into fully or partially liquid calcium aluminates to diminish the clogging of the submerged entry nozzle during the continuous casting process [21]. However, either insufficient or excessive addition of calcium alloys is detrimental because incomplete or superfluous calcium can lead to the formation of solid CaO, CaS, calcium alumina, and other unfavorable inclusions deteriorating the quality of the steel [22,23].

Rare earth (RE) elements have very strong chemical activity because of their unique electronic structures, with a variable valence state of the 4f channel [24]. RE elements have a strong affinity toward O and S and react with these elements to form spindle and spherical RExOy, RExSy, and RExOySz inclusions, thus avoiding the anisotropy of mechanical properties in the final rolled products [25,26,27]. In recent years, extensive research has been carried out on the influence of the RE elements lanthanum and cerium on the microstructures and mechanical properties of various test steels [28,29,30]. Yttrium, another reactive element, not only exhibits some similarities with lanthanum and cerium but also displays its own favorable characteristics [31]. Unfortunately, to the best of the authors’ knowledge, few studies have considered yttrium-modified steel, especially in terms of the inclusions modification of steels with addition of different amounts of yttrium.

In this article, the inclusion changes in E690 steel with addition of different yttrium contents were compared. In addition, the mechanism of inclusions precipitation was clarified by thermodynamic calculation.

2 Experiments

The test steels were prepared by vacuum induction melting furnace (VAIR). The pure iron with a chemical composition (wt%) of 0.002C, 0.005Si, 0.02Mn, 0.01Cr, 0.01Ni, and balance Fe was used as the raw material, in which Si, Mn, Cr, Ni, Nb, V, Ti, graphite, and yttrium ferroalloy were subsequently added. The final chemical compositions of test steels are presented in Table 1. Here, the yttrium ferroalloy is composed of 65 wt% Y and 35 wt% Fe in this study. Ingots were forged and cut into 90 mm × 90 mm × 120 mm slabs. After homogenization at 1,200°C for 30 min, 7-pass hot rolling was carried out to obtain a final thickness of 16 mm by using a rolling mill (model 350 Reversing, Shanxi Rolling Equipment Factory, China). Here, the finish rolling temperature at 810°C, which is measured by an infrared thermometer (model IR-HOH, Beijing Duhelichuang Technology Co., Ltd, China). Finally, the thick plates were air cooled to 700°C and water cooled to 430°C at a rate of 25°C s−1 and then air cooled to room temperature.

Table 1

Chemical compositions of test steels with and without addition of yttrium (wt%)

No.CSiMnPSOAlNbVTiNiCrCuMoY
10.0700.251.00.00800.00200.00280.0290.0300.0300.0120.600.700.300.350
20.0740.281.10.00800.00200.00190.0220.0290.0240.0220.630.770.450.390.015
30.0700.251.00.00770.00140.00150.0310.0270.0210.0190.780.600.410.320.036
40.0770.31.10.00700.00160.00170.0370.0320.0280.0190.620.670.460.390.055

To clarify the precipitation behaviors of inclusions in the test steels, 10 × 10 × 10 mm3 cubic samples were cut from the steel plates and then ground and polished using 3.5 and 0.5 µm diamond compounds. The types of inclusions and their morphology were extensively analyzed by the scanning electron microscopy (model ProX) and energy-dispersive spectrometry (model ProX). In addition, the mechanism of inclusions precipitation was also studied using thermodynamic calculation.

3 Results and discussion

3.1 Effect of yttrium on the morphology and type of inclusions

Figure 1 shows the morphology and the type of inclusions formed in the test steels with and without addition of yttrium. In the absence of the yttrium, MnS is the dominating inclusion, as shown in Figure 1(a). In addition, Al2O3 inclusions can be precipitated in the steel without the addition of yttrium, and MnS inclusions adhere to the surface of the Al2O3 inclusions. During the rolling process, the MnS inclusions extend along the rolling direction, resulting in the Al2O3 inclusions embedded in the MnS inclusions. By adding the yttrium, the strip-like sulfide inclusions were replaced by yttrium-containing complex inclusions with the size lower than 10 µm, as shown in Figure 1(b–d). Compared with Mn and Fe, yttrium has a stronger affinity toward O and S and is more prone to react with these elements to form yttrium-containing oxide and sulfide. In addition, Al2O3 inclusions were found in the test steels with addition of yttrium. This is because of the formation of Al2O3 inclusions in steel before the addition of yttrium.

Figure 1 Morphology and type of inclusions formed in test steels. (a) No. 1 steel; (b) No. 2 steel; (c) No. 3 steel; and (d) No. 4 steel.
Figure 1

Morphology and type of inclusions formed in test steels. (a) No. 1 steel; (b) No. 2 steel; (c) No. 3 steel; and (d) No. 4 steel.

3.2 Thermodynamic calculation of inclusions precipitation in test steels

The formation of inclusions in steel is a complex process, and it is difficult to determine the precipitation condition and the process of inclusions by means of experimental methods. Therefore, this article uses the thermodynamic calculation to study the precipitation regularity of inclusions so as to better control the precipitation of inclusions in steel.

The liquidus temperature (TL) and the solidus temperature (TS) of steel can be calculated by equations (1) and (2), respectively [32]. Table 2 presents the liquidus temperature and solidus temperature of test steels with and without addition of yttrium.

(1)TL=1809−83wt%(C)−7.8wt%(Si)−5wt%(Mn)−32wt%(P)−31.5wt%(S)−1.5wt%(Cr)−2wt%(Mo)−2wt%(V)−3.6wt%(Al)−18wt%(Ti).
(2)TS=1809−344wt%(C)−12.3wt%(Si)−6.8wt%(Mn)−124.5wt%(P)−183.5wt%(S)−1.4wt%(Cr)−4.1wt%(Al)−4.3wt%(Ni).
Table 2

Liquidus temperature and solidus temperature of test steels with and without addition of yttrium (K)

Test steelNo. 1No. 2No. 3No. 4
Liquidus temperature1,7931,7921,7941,792
Solidus temperature1,7701,7681,7701,767

3.2.1 Thermodynamic calculation of inclusions precipitation in liquid steel

In No. 1 test steel, namely, the steel without addition of yttrium, MnS, and Al2O3 are the dominating inclusions. By adding the yttrium, because the RE yttrium has a strong affinity towards S and O, and therefore, Y2O3, Y2O2S, Y2S3, and YS may form in the molten steel. The standard Gibbs free energy change for the formation of these various inclusions in the liquid steel is reported in equations (3)–(8) [33].

(3)[Mn]+[S]=MnS(s)ΔG3θ=−1,58,365+93.996T(Jmol−1)
(4)2[Al]+3[O]=Al2O3(s)ΔG4θ=−12,25,000+393.8T(Jmol−1)
(5)2[Y]+3[O]=Y2O3(s)ΔG5θ=−17,92,600+658.0T(Jmol−1)
(6)2[Y]+2[O]+[S]=Y2O2S(s)ΔG6θ=−15,21,000+536.0T(Jmol−1)
(7)2[Y]+3[S]=Y2S3(s)ΔG7θ=−11,71,000+441.0T(Jmol−1)
(8)[Y]+[S]=YS(s)ΔG8θ=−3,21,080+91.0T(Jmol−1)

In the liquid steel, the reaction equation of metal element E reacts with nonmetal element F to generate ExFy can be expressed through equation (9).

(9)xE+yF=ExFy

When equation (9) reaches equilibrium, the Gibbs free energy (ΔG) is equal to zero. Therefore, the relation between the standard Gibbs free energy (ΔGθ) and the equilibrium constant (K) can be expressed as equation (10).

(10)lnK=−ΔGθRT=−C2−C1T,

where R is the gas constant, in J mol−1 K−1; C1 and C2 are constants; and T is the temperature (K).

According to equation (9), the equilibrium constant can also be described by equation (11).

(11)K=αExFyαEx⋅αFy=1fEx⋅w(E)x⋅fFy⋅w(F)y,

where αi is the activity of component i; fi is the activity coefficient of element i; and w(i) is the mass fraction of component i (wt%).

Substituting equation (11) into equation (10) can result in equation (12).

(12)xlnfE+ylnfF+ln(w(E)x⋅w(F)y)=C2+C1T

Therefore, the equilibrium solubility product of ExFy in the liquid steel can be expressed as equation (13).

(13)ln(w(E)x⋅w(F)y)=C2+C1T−xlnfE−ylnfF

In the E690 liquid steel, the activity coefficient is related to the temperature and interaction coefficient of various elements in the liquid steel. However, E690 offshore platform steel belongs to high-strength low alloy steels, the mass fraction of each solute element tends to 0, and the mass fraction of the solvent iron approaches 1. The second-order interaction coefficients have little effect on the activity coefficient of solute; therefore, the activity coefficients of the components E and F are calculated directly by using the Wagner model characterized by the first-order interaction coefficients [32]. The activity coefficient of each solute element in the liquid steel is calculated by equation (14).

(14)lnfi=2.303∑j=1neijw[j],

where eij is the first-order interaction parameter between i and j and w[j] is the mass percentage of element j.

Table 3 presents the first-order interaction coefficient eij of various solute elements in the liquid steel. Substituting the data in Table 3 into equation (14), the activity coefficients of O, S, Y, Al, and Mn in the liquid steel are calculated and presented in Table 4.

Table 3

First-order interaction coefficients eij of various elements in liquid steel

eijCSiMnPSOCrNiMoCuAlY
O−0.45−0.131−0.0210.07−0.133−0.2−0.040.0060.0035−0.013−3.9−16.3
S0.1120.063−0.0260.029−0.028−0.27−0.01100.0027−0.00840.035−0.55
Y−0.22———−7.34−90.7—————−0.006
Al0.0910.00560.0120.050.03−6.60.0250.008—0.0080.045—
Mn−0.070.390−0.0035−0.048−0.0830.003−0.0070.0045—0.07—
Table 4

The activity coefficients of O, S, Y, Al, and Mn in liquid steel

No.OSYAlMn
10.56740.9702—1.07251.2421
20.33150.94580.62601.09971.2750
30.14520.92740.68871.09351.2383
40.06460.90590.65581.09941.2999

Substituting the activity coefficients of O, S, Y, Al, and Mn into equation (13), the logarithm of the equilibrium solubility product of MnS, Al2O3, Y2O3, Y2O2S, Y2S3, and YS can be obtained. Figures 2–7 show the logarithm of the equilibrium solubility product and the actual solubility product as a function of temperature for MnS, Al2O3, Y2O3, Y2O2S, Y2S3, and YS.

Figure 2 Logarithm of the solubility product as a function of temperature for MnS in the liquid steel.
Figure 2

Logarithm of the solubility product as a function of temperature for MnS in the liquid steel.

Figure 3 Logarithm of the solubility product as a function of temperature for Al2O3 in the liquid steel.
Figure 3

Logarithm of the solubility product as a function of temperature for Al2O3 in the liquid steel.

Figure 4 Logarithm of the solubility product as a function of temperature for Y2O3 in the liquid steel.
Figure 4

Logarithm of the solubility product as a function of temperature for Y2O3 in the liquid steel.

Figure 5 Logarithm of the solubility product as a function of temperature for Y2O2S in the liquid steel.
Figure 5

Logarithm of the solubility product as a function of temperature for Y2O2S in the liquid steel.

Figure 6 Logarithm of the solubility product as a function of temperature for Y2S3 in the liquid steel.
Figure 6

Logarithm of the solubility product as a function of temperature for Y2S3 in the liquid steel.

Figure 7 Logarithm of the solubility product as a function of temperature for YS in the liquid steel.
Figure 7

Logarithm of the solubility product as a function of temperature for YS in the liquid steel.

During the cooling process of the liquid steel, the solubility of inclusions in steel is gradually reduced. When the actual solubility product of the inclusion generating elements is larger than the equilibrium solubility product, the inclusion can be formed. As shown in Figures 2 and 3, for test steels No.1 to No.4, MnS inclusions cannot be generated in the liquid steel, while Al2O3 inclusions can be precipitated. Therefore, for test steels with addition of yttrium, as yttrium has a strong affinity toward O and S and react with these elements, Y2O3, Y2O2S, Y2S3, and YS may form in the liquid steel. Wang and Du [34] investigated the thermodynamics of deoxidation and desulfuration of yttrium in the liquid steel. Their research results show that when yttrium is added to the liquid steel, it reacts with oxygen first; when the precipitated Y2O3 inclusions are not removed from the liquid steel, S in the liquid steel reacts with the precipitated Y2O3 inclusions to generate Y2O2S inclusions; at very late times, when the oxygen content in the liquid steel is very low, yttrium in the liquid steel will react with sulfur to generate Y2S3 or YS inclusions. Wang and Du [34] also reported that under the reaction equilibrium conditions, the product of the reaction between yttrium and S is mainly YS. As shown in Figures 4–7, Y2O3, Y2O2S, and YS inclusions can be precipitated and Y2S3 inclusions cannot be formed in the liquid steel with addition of different amounts of yttrium. When the yttrium content in the liquid steel is 0.015 wt%, there are no YS inclusions in the liquid steel. This is because all the yttrium in the liquid steel reacts with O to generate Y2O3 inclusions, and the partial Y2O3 inclusions react with S to form Y2O2S inclusions. However, when the yttrium content in the liquid steel increases up to 0.036 wt%, the residual yttrium after reacting with O in the liquid steel will react with S to precipitate YS inclusions. The calculated results are in accordance with the experimental results.

3.2.2 Thermodynamic calculation of MnS precipitation in solid–liquid dual phase zone

Because there is no MnS inclusions precipitation in the liquid steel, it is necessary to calculate the thermodynamics of MnS inclusions precipitation at the solidification front. When the liquid steel begins to crystallize into δ-ferrite, a solid–liquid dual phase zone is formed. In the solidification process of the liquid steel, the forming elements of MnS inclusions in steel tend to be enriched in the liquid phase at the solidification front, leading to an increase in the actual solubility product [32]. Provided that the forming elements of MnS inclusions in the solid phase are nondiffused, the liquid phase is uniformly mixed, and the solid–liquid interface is in a local equilibrium state. Under these conditions, the contents of S and Mn can be used in the Scheil model, namely, equations (15) and (16).

(15)w(S)L=w(S)/[P(KS−1)+1]
(16)w(Mn)L=w(Mn)⋅(1−P)(KMn−1),

where w(S)L and w(Mn)L indicate the mass fractions of S and Mn in the liquid phase at the solidification front, respectively; w(S) and w(Mn) are the mass fractions of S and Mn in the liquid phase when the liquid steel begins to solidify, respectively, in wt%; KS and KMn are the equilibrium distribution coefficients of S and Mn, respectively. Zhang et al. [35] reported that the equilibrium distribution coefficients of S and Mn are 0.035 and 0.785, respectively; P is the solid phase fraction, and its relationship with temperature can be expressed in equation (17).

(17)P=(Tm−TS)⋅(TL−Tf)(TL−TS)⋅(Tm−Tf),

where Tm is the melting point of pure iron, and its value is 1,809 K; Tf is the temperature at the solidification front (K); and TS and TL are the solidus temperature and liquidus temperature (K), respectively.

According to equations (15) and (16), the actual solubility product in the liquid phase at the solidification front can be calculated. Zhang et al. [35] and Ueshima et al. [36] reported that the equilibrium solubility product for MnS inclusions in the liquid phase at the solidification front can be calculated by equation (18).

(18)ln[w(Mn)⋅w(S)]=−19873.92/T+10.93−lnfMn−lnfS

Figure 8 shows the logarithm of the equilibrium solubility product and the actual solubility product as a function of temperature for MnS inclusions in the liquid phase at the solidification front.

Figure 8 Logarithm of the solubility product as a function of temperature for MnS in the liquid phase at the solidification front.
Figure 8

Logarithm of the solubility product as a function of temperature for MnS in the liquid phase at the solidification front.

The contents of S and Mn in the solid phase at the solidification front can be used in the Scheil model and expressed through equations (19) and (20) [37].

(19)w(S)S=KS⋅w(S)/[P(KS−1)+1]
(20)w(Mn)S=KMn⋅w(Mn)⋅(1−P)(KMn−1),

where w(S)S and w(Mn)S indicate the mass fractions of S and Mn in the solid phase at the solidification front, respectively.

According to equations (19) and (20), the actual solubility product in the solid phase at the solidification front can be calculated. In addition, Zhang et al. [35] and Ueshima et al. [36] reported that the equilibrium solubility product for MnS inclusions in the solid phase at the solidification front can be calculated by equation (21).

(21)ln[w(Mn)⋅w(S)]=−21274.24/T+6.97

Figure 9 shows the logarithm of the equilibrium solubility product and the actual solubility product as a function of the temperature for MnS inclusions in the solid phase at the solidification front.

Figure 9 Logarithm of the solubility product as a function of temperature for MnS in the solid phase at the solidification front.
Figure 9

Logarithm of the solubility product as a function of temperature for MnS in the solid phase at the solidification front.

As shown in Figures 8 and 9, when the test steels with addition of yttrium, no separate MnS inclusions are formed in the solid–liquid dual phase zone. This is because yttrium has a strong affinity toward O and S and reacts with O and S to form Y2O3, Y2O2S, and YS inclusions. For test steels without addition of yttrium, MnS inclusions can be precipitated in the liquid phase at the solidification front. While the equilibrium solubility product was greater than the actual solubility product, and no MnS inclusions can be precipitated in the solid phase at the solidification front. The calculated results are in accordance with those reported by Zhang et al. [35], who indicated that MnS inclusions precipitated at the end of solidification, rather than in the liquid steel.

3.2.3 Thermodynamic calculation of MnS precipitation in solid steel

It can be seen from the iron–carbon phase diagram that when the liquid steel solidifies completely, the liquid phase and ferrite transform into austenite almost at the same time. Because the solubility of MnS inclusions in the austenite phase is very small, the solid phase can be considered to be in accordance with Henry’s laws (1 wt% standard state). The equilibrium solubility product can be calculated through equation (21). Figure 10 shows the logarithm of the equilibrium solubility product and the actual solubility product as a function of temperature for MnS inclusions in solid steel.

Figure 10 Logarithm of the solubility product as a function of temperature for MnS in the solid steel.
Figure 10

Logarithm of the solubility product as a function of temperature for MnS in the solid steel.

As shown in Figure 10, it was found that the actual solubility product is always larger than the equilibrium solubility product. This means that MnS inclusions can be precipitated in solid steel. However, MnS inclusions precipitation is a chemical reaction controlled by S and Mn diffusion in the solid steel because the diffusion rate of S and Mn in the solid steel is very slow. Therefore, the precipitation of MnS inclusions in solid steel is mainly controlled by dynamic conditions.

4 Conclusions

  1. The MnS inclusions were precipitated in the liquid phase at the solidification front in E690 steel in the absence of yttrium and were replaced by yttrium-containing oxide and sulfide complex inclusions on addition of yttrium.

  2. By adding the yttrium, Y2O3, Y2O2S, and YS inclusions were precipitated in the liquid steel, and the precipitation sequence was Y2O3, Y2O2S, and YS. While Y2S3 inclusions cannot be formed in the liquid steel.

  3. In E690 steels with and without addition of yttrium, Al2O3 inclusions can be formed in the liquid steel.

Acknowledgments

The authors gratefully acknowledge the support by the National Natural Science Foundation of China (NSFC, No. 51874116, 51664021 and 51734003).

  1. Conflict of interest: The authors declare no conflict of interest.

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Received: 2019-01-03
Accepted: 2019-01-22
Published Online: 2020-10-02

© 2020 Xiaojun Xi et al., published by De Gruyter

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

Articles in the same Issue

  1. Research Article
  2. Electrochemical reduction mechanism of several oxides of refractory metals in FClNaKmelts
  3. Study on the Appropriate Production Parameters of a Gas-injection Blast Furnace
  4. Microstructure, phase composition and oxidation behavior of porous Ti-Si-Mo intermetallic compounds fabricated by reactive synthesis
  5. Significant Influence of Welding Heat Input on the Microstructural Characteristics and Mechanical Properties of the Simulated CGHAZ in High Nitrogen V-Alloyed Steel
  6. Preparation of WC-TiC-Ni3Al-CaF2 functionally graded self-lubricating tool material by microwave sintering and its cutting performance
  7. Research on Electromagnetic Sensitivity Properties of Sodium Chloride during Microwave Heating
  8. Effect of deformation temperature on mechanical properties and microstructure of TWIP steel for expansion tube
  9. Effect of Cooling Rate on Crystallization Behavior of CaO-SiO2-MgO-Cr2O3 Based Slag
  10. Effects of metallurgical factors on reticular crack formations in Nb-bearing pipeline steel
  11. Investigation on microstructure and its transformation mechanisms of B2O3-SiO2-Al2O3-CaO brazing flux system
  12. Energy Conservation and CO2 Abatement Potential of a Gas-injection Blast Furnace
  13. Experimental validation of the reaction mechanism models of dechlorination and [Zn] reclaiming in the roasting steelmaking zinc-rich dust process
  14. Effect of substituting fine rutile of the flux with nano TiO2 on the improvement of mass transfer efficiency and the reduction of welding fumes in the stainless steel SMAW electrode
  15. Microstructure evolution and mechanical properties of Hastelloy X alloy produced by Selective Laser Melting
  16. Study on the structure activity relationship of the crystal MOF-5 synthesis, thermal stability and N2 adsorption property
  17. Laser pressure welding of Al-Li alloy 2198: effect of welding parameters on fusion zone characteristics associated with mechanical properties
  18. Microstructural evolution during high-temperature tensile creep at 1,500°C of a MoSiBTiC alloy
  19. Effects of different deoxidization methods on high-temperature physical properties of high-strength low-alloy steels
  20. Solidification pathways and phase equilibria in the Mo–Ti–C ternary system
  21. Influence of normalizing and tempering temperatures on the creep properties of P92 steel
  22. Effect of temperature on matrix multicracking evolution of C/SiC fiber-reinforced ceramic-matrix composites
  23. Improving mechanical properties of ZK60 magnesium alloy by cryogenic treatment before hot extrusion
  24. Temperature-dependent proportional limit stress of SiC/SiC fiber-reinforced ceramic-matrix composites
  25. Effect of 2CaO·SiO2 particles addition on dephosphorization behavior
  26. Influence of processing parameters on slab stickers during continuous casting
  27. Influence of Al deoxidation on the formation of acicular ferrite in steel containing La
  28. The effects of β-Si3N4 on the formation and oxidation of β-SiAlON
  29. Sulphur and vanadium-induced high-temperature corrosion behaviour of different regions of SMAW weldment in ASTM SA 210 GrA1 boiler tube steel
  30. Structural evidence of complex formation in liquid Pb–Te alloys
  31. Microstructure evolution of roll core during the preparation of composite roll by electroslag remelting cladding technology
  32. Improvement of toughness and hardness in BR1500HS steel by ultrafine martensite
  33. Influence mechanism of pulse frequency on the corrosion resistance of Cu–Zn binary alloy
  34. An interpretation on the thermodynamic properties of liquid Pb–Te alloys
  35. Dynamic continuous cooling transformation, microstructure and mechanical properties of medium-carbon carbide-free bainitic steel
  36. Influence of electrode tip diameter on metallurgical and mechanical aspects of spot welded duplex stainless steel
  37. Effect of multi-pass deformation on microstructure evolution of spark plasma sintered TC4 titanium alloy
  38. Corrosion behaviors of 316 stainless steel and Inconel 625 alloy in chloride molten salts for solar energy storage
  39. Determination of chromium valence state in the CaO–SiO2–FeO–MgO–CrOx system by X-ray photoelectron spectroscopy
  40. Electric discharge method of synthesis of carbon and metal–carbon nanomaterials
  41. Effect of high-frequency electromagnetic field on microstructure of mold flux
  42. Effect of hydrothermal coupling on energy evolution, damage, and microscopic characteristics of sandstone
  43. Effect of radiative heat loss on thermal diffusivity evaluated using normalized logarithmic method in laser flash technique
  44. Kinetics of iron removal from quartz under ultrasound-assisted leaching
  45. Oxidizability characterization of slag system on the thermodynamic model of superalloy desulfurization
  46. Influence of polyvinyl alcohol–glutaraldehyde on properties of thermal insulation pipe from blast furnace slag fiber
  47. Evolution of nonmetallic inclusions in pipeline steel during LF and VD refining process
  48. Development and experimental research of a low-thermal asphalt material for grouting leakage blocking
  49. A downscaling cold model for solid flow behaviour in a top gas recycling-oxygen blast furnace
  50. Microstructure evolution of TC4 powder by spark plasma sintering after hot deformation
  51. The effect of M (M = Ce, Zr, Ce–Zr) on rolling microstructure and mechanical properties of FH40
  52. Phase evolution and oxidation characteristics of the Nd–Fe–B and Ce–Fe–B magnet scrap powder during the roasting process
  53. Assessment of impact mechanical behaviors of rock-like materials heated at 1,000°C
  54. Effects of solution and aging treatment parameters on the microstructure evolution of Ti–10V–2Fe–3Al alloy
  55. Effect of adding yttrium on precipitation behaviors of inclusions in E690 ultra high strength offshore platform steel
  56. Dephosphorization of hot metal using rare earth oxide-containing slags
  57. Kinetic analysis of CO2 gasification of biochar and anthracite based on integral isoconversional nonlinear method
  58. Optimization of heat treatment of glass-ceramics made from blast furnace slag
  59. Study on microstructure and mechanical properties of P92 steel after high-temperature long-term aging at 650°C
  60. Effects of rotational speed on the Al0.3CoCrCu0.3FeNi high-entropy alloy by friction stir welding
  61. The investigation on the middle period dephosphorization in 70t converter
  62. Effect of cerium on the initiation of pitting corrosion of 444-type heat-resistant ferritic stainless steel
  63. Effects of quenching and partitioning (Q&P) technology on microstructure and mechanical properties of VC particulate reinforced wear-resistant alloy
  64. Study on the erosion of Mo/ZrO2 alloys in glass melting process
  65. Effect of Nb addition on the solidification structure of Fe–Mn–C–Al twin-induced plasticity steel
  66. Damage accumulation and lifetime prediction of fiber-reinforced ceramic-matrix composites under thermomechanical fatigue loading
  67. Morphology evolution and quantitative analysis of β-MoO3 and α-MoO3
  68. Microstructure of metatitanic acid and its transformation to rutile titanium dioxide
  69. Numerical simulation of nickel-based alloys’ welding transient stress using various cooling techniques
  70. The local structure around Ge atoms in Ge-doped magnetite thin films
  71. Friction stir lap welding thin aluminum alloy sheets
  72. Review Article
  73. A review of end-point carbon prediction for BOF steelmaking process
https://doi.org/10.1515/htmp-2020-0089
Keywords for this article
yttrium; E690 offshore platform steel; yttrium-containing inclusion; thermodynamic calculation
Creative Commons
BY 4.0

Articles in the same Issue

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