Next Article in Journal
Multiscale 3D Curvature Analysis of Processed Surface Textures of Aluminum Alloy 6061 T6
Previous Article in Journal
Synergistic Effect on the Thermomechanical and Electrical Properties of Epoxy Composites with the Enhancement of Carbon Nanotubes and Graphene Nano Platelets
 
 
Search for Articles:
Title / Keyword
Author / Affiliation / Email
Journal
Article Type
 
 
Advanced Search
 
Section
Special Issue
Volume
Issue
Number
Page
 
Journals
Materials
Volume 12
Issue 2
10.3390/ma12020256
materials-logo
Submit to this Journal Review for this Journal Propose a Special Issue
► Article Menu

Article Menu

share Share announcement Help format_quote Cite question_answer Discuss in SciProfiles
first_page
settings
Order Article Reprints
Font Type:
Arial Georgia Verdana
Font Size:
Aa Aa Aa
Line Spacing:
Column Width:
Background:
Article

The Influence of A Mo Addition on the Interfacial Morphologies and Corrosion Resistances of Novel Fe-Cr-B Alloys Immersed in Molten Aluminum

by
Zicheng Ling
1,
Weiping Chen
1,*,
Weiye Xu
1,
Xianman Zhang
2,
Tiwen Lu
1 and
Jian Liu
1
1
Guangdong Key Laboratory for Advanced Metallic Materials Processing, South China University of Technology, Guangzhou 510640, China
2
Mechanical and Electrical Engineering College, Hainan University, Haikou 570228, China
*
Author to whom correspondence should be addressed.
Materials 2019, 12(2), 256; https://doi.org/10.3390/ma12020256
Submission received: 12 November 2018 / Revised: 28 December 2018 / Accepted: 9 January 2019 / Published: 14 January 2019
(This article belongs to the Section Corrosion)
Browse Figures
Review Reports Versions Notes

Abstract

:
The influence of a Mo addition on the interfacial morphologies and corrosion resistances of novel Fe-Cr-B alloys in molten aluminum at 750 °C was systematically investigated using scanning electron microscopy, X-ray diffractometer, electron probe microanalysis, and transmission electron microscopy. The results indicated that Mo could not only strengthen the matrix but also facilitate the formation of borides. Furthermore, the microstructures of Mo-rich M2B boride changed from a local eutectic net-like structure to a typical coarse dendritic structure and a blocky hypereutectic structure with increasing Mo addition. This was true of the blocky Mo-rich M2B boride, rod-like Cr-rich M2B boride and the corrosion products, which had a synergistic effect on retarding of the diffusion of molten aluminum. Notably, the corrosion resistance of the Fe-Cr-B-Mo alloy, with an 8.3 wt.% Mo addition, was 3.8 times higher than that of H13 steel.

1. Introduction

It is acknowledged that molten aluminum is one of the most aggressive metal melts due to its high chemical activity it can inevitably react with most other metals [1,2]. In the aluminum industry, especially in cast dies and hot dip aluminizing production process, a wide range of metallic components, such as crucibles, die-casting molds and charging cylinders, are in contact with molten aluminum or its alloys. These components suffer from serious corrosion while melting and can even fail [3,4]. Thus, frequently changing these components wastes money and time. Therefore, a larger number of works [5,6,7,8] have been conducted to explore new materials with high corrosion resistance to molten aluminum. Meanwhile, the corrosion mechanism of steels in molten aluminum has also been widely studied in recent years [9,10,11]. The corrosion mechanism of steel in molten aluminum can be summarized by the following two points: one is the dissolution of iron and steel the other is the nucleation and growth of the Fe-Al intermetallic compounds (IMCs), such as the phase of η-Fe2Al5 and θ-FeAl3 [12]. Additionally, the corrosion process between steel substrate and molten aluminum is mainly controlled by the inter-diffusion of Fe and Al atoms [12] and the driving force is the different chemical potential between the steel substrate and the molten aluminum [1]. Thus, limiting the atomic inter-diffusion between the substrate and molten aluminum plays a key role in ameliorating the materials’ corrosion resistances. Additionally, the cracks in the corrosion layer, resulted from the phase transition stresses and the different thermal expansion coefficients among the IMCs also lead to corrosion product spalling [13].
Previous studies have proposed methods to increase the corrosion resistance and operating life of cast. There are certain die materials with surface treatment technology, such as surface coating [6,14], surface alloying [7,15], and surface duplex treatments [16,17]. However, surface treatments are restricted to the surface coating uniformity, the thermal expansion properties, and the wettability similarity with substrate materials. However, the brittle and thin protective coating layer is susceptible to rapid corrosion and even abrasion in molten aluminum, which may be unavoidable to spalling and may even lead to failure. Recently, much attention has been paid to Fe-B alloys due to their unique net-like structures and properties. For example, in related studies, cast B-added steel has a high hardness and corrosion resistance to molten zinc due to its 3D net-like boride [18,19]. Additionally, it has proved that boronising on steel and iron can improve the corrosion resistance in molten aluminum because of the formation of Fe2B or Fe2B/FeB [20]. However, the intrinsic brittleness of the Fe2B phase restricts its related material development and applications.
To provide insight into the abovementioned problem, several attempts [21,22,23,24,25,26,27,28] have been made to modify the undesired microstructure by alloying with metals, such as Cr [21,22], Ti [23,24], W [25], and Mo [26], to stabilize the M2B-type borides. Among these metals, Mo not only has a low solubility in molten aluminum [27], but also increases the hardenability via co-addition into the B-added steels [28]. Although the Fe-Cr-B-Mo cast steels with different B additions were studied in our previous study [8], the role of how different Mo additions affect the interfacial morphologies and corrosion resistances of Fe-Cr-B alloys in molten aluminum is still unknown. Therefore, the present work aims to prepare a kind of novel Fe-Cr-B alloy with different contents of Mo and their interfacial morphologies and corrosion resistances in molten aluminum were also investigated.

2. Materials and Methods

2.1. Material Preparation

The investigated novel Fe-Cr-B alloys with different contents of Mo were melted in a 250 kg–capacity medium-frequency induction furnace. The initial charge materials were clean A3 steel and ferroalloys, such as Fe-70 wt.% Cr and Fe-60 wt.% Mo; then, Fe-32 wt.% B was added into the slag to minimize the oxidation loss. When all the alloys were melted, they were then transferred into the pre-heated teapot ladle with a small amount of pure Al to deoxidize at 1530 °C. After removal of the slag, the high-temperature melt was poured into sodium silicate-CO2 bonded sand molds at 1450 °C, obtaining the Y-block ingots following ASTM A781/A 781-M95. Notably, all the prepared alloys were adopted the multiple pouring in one furnace by adding the charge materials. After these ingots were cooled to room temperature, they were cut from the lower part of the Y-block ingots using a wire-electrode with dimensions of 10 mm × 10 mm × 10 mm. Additionally, the H13 steel was selected as a standard sample. The chemical compositions of the designed alloys were analyzed using inductively coupled plasma atomic emission spectroscopy (ICP-AES); the results for the H13 steel are also given in Table 1.

2.2. Material Preparation

All surfaces of the test samples were ground using 1500 mesh SiC paper, washed with ethanol in an ultrasonic cleaner and then weighted on an electronic balance prior to the corrosion test. A schematic diagram of the corrosion tester is shown in Figure 1. First, five surfaces of the test samples were coated with alumina and then wrapped in graphite paper before being inserted into a graphite mold. Second, the uncovered surfaces were exposed to the 3.0 kg unsaturated molten aluminum (99.99 wt.%) at 750 °C for various immersion times (0.5 h, 1 h, 4 h, 6 h, and 8 h). Additionally, three parallel samples of each type alloy were used. During the corrosion test experiments, to monitor the process temperature, a K-type thermocouple covered by alumina was immersed into the molten aluminum. Finally, before determining the weight loss, the air-cooled samples were put into a 10% NaOH solution to remove the residual molten aluminum. In this study, the corrosion rates of the samples were assessed by the weight loss per square centimeter of the sample per minute, i.e., (mg·cm−2min−1).

2.3. Microstructure Characteristics

Cross-sections of the corroded samples were cut perpendicular to the corrosion layer, followed by a standard grinding and polishing for the metallographic examinations. Additionally, the polished samples were etched in a solution (4 mL HNO3 + 4 mL HF + 92 mL H2O). The microstructures of the as-cast specimens and corroded specimens were observed using scanning electron microscopy (SEM, Carl Zeiss NTS GmbH, Oberkochen Germany) equipped with a back-scattered electron (BSE). The phase analyses of the designed Fe-Cr-B alloys and the interfacial corrosion products were performed using an X-ray diffractometer (XRD, Bruker D8 ADVANCE, Karlsruhe, Germany) with Cu Kα radiation. Besides, the chemical compositions of the different phases of the Fe-Cr-B alloys and corrosion layers, electron probe microanalyses with a wavelength dispersive X-ray (WDX) analysis (EPMA, JXA-8230, JEOL, Tokyo, Japan) were performed. To further understand the phase compositions of pristine matrix and the corrosion products, thin foil samples were prepared by mechanical thinning followed by ion milling, then which were observed under a transmission electron microscope (TEM, TECNAL G2 S-TWIN F20, FEI, Hillsboro, USA) with selected area electron diffraction (SAED) analysis and an energy dispersive spectrometer (EDS).

3. Results and Discussion

3.1. As-Cast Microstructure

The XRD patterns and microstructures of the Fe-Cr-B alloys are shown in Figure 2 and Figure 3, respectively. According to the XRD results (Figure 2), it can be identified that the main phases of M1-M4 are α-(Fe, Cr), M2B-type borides. As shown in Figure 3a–c, the morphologies of these borides display rod-like, dendritic and net-like structures. As shown in Figure 3c, when the Mo content reaches to 6.19 wt.%, the interesting dendritic eutectic borides extensively appear. Moreover, when the Mo content reaches to 8.30 wt.%, a new kind of irregular blocky boride is detected in M4 (Figure 3d). It may be inferred that the blocky borides are the hypereutectic Mo-rich boride. It is clearly found that rod-like borides decrease as the addition of Mo increases (Figure 3b–d). In addition, net-like structures are adjacent to the rod-like borides in some light regions (Figure 3b). Additionally, from the XRD pattern of M4 sample, it can be observed that carbide peaks are more intense than that of M1-M3, which may be inferred that there are more carbides formation owing to the highest content among the designed alloys. Moreover, the chemical compositions of the various borides are measured using EPMA and are shown in Table 2. The results suggest that the rod-like Cr-rich boride (Figure 3a, point 1) has a stoichiometry of Fe1.12Cr0.88B, which is close to the Fe1.1Cr0.9B0.96 phase reported in the literature [29]. The net-like Cr-rich borides (Figure 3a, point 2 and Figure 3b, point 3) have a stoichiometry of Fe1.34Cr0.68B and Fe0.80Cr0.55Mo0.53B, respectively. In contrast, the stoichiometry of the dendritic boride (Figure 3c, point 4) and the blocky boride (Figure 3d, point 5) are Fe0.82Cr0.64Mo0.78B and Fe0.59Cr0.47Mo0.64B, respectively.
Figure 4 shows the bright-field TEM micrographs and corresponding selected area diffraction patterns (SADPs) of borides and matrix in alloy M4. From the Figure 4a,d, it can be noticed that the primary rod-like Cr-rich M2B boride is a body-centered orthorhombic (BCO) structure (such as CrFeB as detected by XRD with the lattice parameters of a = 1.4534 nm, b = 0.7302 nm, c = 0.4215 nm), which is different from the single phase Fe2B with a body-centered tetragonal (BCT) structure with the lattice constant of a = b = 0.5109 nm, c = 0.4249 nm, c/a = 0.832. Notably, it has been reported that when the Cr content is higher than 8 wt.%, the phase of the boride transforms from tetragonal (Fe, Cr)2B to orthorhombic (Cr, Fe)2B [30]. The SADPs taken from the eutectic net-like M2B boride (Figure 4b,e) reveals a BCO structure, which is in agreement with the literature [29]. The TEM analysis on the matrix reveals a body-centered cubic (BCC) structure (Figure 4b,f). It can be inferred that it is a typical ferritic structure with supersaturated alloying elements such as Cr, Mo, and little of C and B. Additionally, the TEM analysis on SADPs in Figure 4c,g indicates that the blocky Mo-rich M2B boride can be indexed to a BCT structure with the lattice parameters of a = b = 0.5547 nm, c = 0.4739 nm, c/a = 0.85. The interplanar distance of the (110) plane for Mo2B is 0.4012 nm, which is in agreement with the XRD results (d(110) = 0.3900 nm). Obviously, the quantitative elemental analysis of various morphologies of borides are confirmed to be M2B-type borides. All the WDX analysis results on the various borides are in agreement with the previous TEM analysis with the corresponding SADPs.
The formation of M2B-type borides is ascribed to the low solution of B in austenite/ferrite and the non-equilibrium segregation of B along the austenite grain boundary during the solidification process [31,32]. Actually, without Mo addition, owing to the similar crystal structural parameters of Fe and Cr atoms, Cr atoms may first substitute for Fe atoms and form the eutectic net-like and even the rod-like Cr-rich boride during the solidification, which is also conformed to the solidification rule of Fe-Cr-B-C phase diagram [30,33]. Then, with the Mo addition, the nucleation and growth of eutectic net-like Mo-rich borides may be followed by depleting the adjacent Cr and B atoms [29]. Applying more Mo addition (when the content reaches to a certain value, which is more than 6.3 wt.%) to the alloy, it occurs the hypereutectic blocky Mo-rich M2B-type boride. Obviously, superfluous Mo atoms would may also dissolve in carbide and ferrite.

3.2. Corrosion Resistance

Figure 5 shows the weight loss rates of the designed Fe-Cr-B alloys and H13 steel immersed in the molten aluminum. Obviously, it can be seen that all the Fe-Cr-B alloys exhibit comparatively better corrosion resistances than that of H13 steel. Except for the immersed times of 0.5 h and 1 h, the variation trends of the curves of M1-M4 samples decrease with the immersion time, which are different from that of H13. Additionally, the result shows that the weight loss rate of the M1-M4 samples with the Mo addition presents a decreasing trend, except for the M3 sample. However, the M1 sample presents a good corrosion resistance, which may be ascribed to the comparatively higher B content (which can form more M2B-type boride) than that of M2-M3. Among them, the corrosion resistance of M4 sample is 3.8 times higher than that of H13 steel at 8 h. Therefore, it can be inferred that the various borides and their morphologies can play a key role in improving the corrosion resistance of Fe-Cr-B-Mo alloys in molten aluminum.

3.3. Cross-Sectional Morphology of the Interfacial Corrosion Layer

The cross-sectional interfacial morphologies of M1-M4 alloys and H13 steel corroded by molten aluminum are shown in Figure 6. The images show that the interfacial morphology of H13 steel (Figure 6e) immersed in molten aluminum is different from that of Fe-Cr-B alloys with various Mo contents (Figure 6a–d). Obviously, the interfacial IMC layers of the M1-M4 samples are composed of some special periodic layered structures (PLSs) (Figure 6a–d). According to the corrosion rate of M1-M4 (Figure 5), it can be inferred that the PLSs can hinder the atomic inter-diffusion between the substrate and the molten aluminum. However, as the corrosion progress goes on, the PLSs can be corroded into particles (close to molten aluminum). Notably, the interfaces between the M1-M4 substrates and the IMC layers are smoother than that of H13 steel. The interfacial morphology of H13 steel (Figure 6e) presents one kind of thick finger-like Fe-Al IMC growing up towards the steel matrix and the other kind of thin needle-shaped Fe-Al IMC adjacent to the molten aluminum. Notably, there are quantity of cracks in the corrosion layer (Figure 6e). These micro-cracks are very harmful to the matrix, which will allow the molten aluminum to more easily infiltrate into the substrate and will hence result in reactions causing the interfacial layer to spall off and break down [34]. For the alloys of M3 and M4 especially, the exfoliated Mo-rich M2B borides are also found (Figure 6b–d). Additionally, there are few micro-cracks in the corrosion layer, and the number of micro-cracks decreases with the increase in Mo addition (Figure 6a–d). As previously mentioned, the phase transition in the corrosion layer and the different thermal expansion coefficient among the various phases result in the formation of micro-cracks [35,36,37].
The high magnifications illustrated in Figure 6a–d show that the matrixes are corroded first. Meanwhile, the rod-like (Cr, Fe)2B and Mo-rich M2B borides extrude into the corrosion layer (Figure 6a–d), which proves that the borides can withstand the corrosion of molten aluminum for a much longer time than H13 steel and can present a better corrosion resistance [8,35]. Additionally, the morphology of boride plays a significant role in improving the corrosion resistance in molten aluminum, especially for the Mo-rich M2B-type boride, from the weight loss rates of the M2-M4 samples (Figure 5). Combining the related cast microstructures (Figure 3b–d), it can be inferred that the net-like Mo-rich borides (Figure 6b,c) cannot withstand molten aluminum for a long time because of their small size. However, the M4 sample presents the best corrosion resistance among all of the samples, which is ascribed to the blocky Mo-rich boride structure (Figure 6d) with its much larger size.
As observed in Figure 7, the relationship between the thicknesses of IMCs and the corrosion times of sample M4 and H13 steel indicates that the curves generally follow a nonlinear law and that the IMC thickness of M4 alloy is much larger than that of the H13 steel for all immersion times. The IMC thickness of M4 (~1437 μm) is 10.8 times than that of H13 steel (~133 μm) after being immersed for 8 h. However, the thickness of the corrosion layer experiences variations of increases and decreases due to the complex interfacial reaction and spallation mechanism. The thickness of IMC layer of M4 sample increases with the increase in immersion time. The reason may be ascribed to the following aspects: On one hand, the 3D net-like structure of borides can protect the Fe-Al IMCs from spalling. On the other hand, the IMC layers can serve as barriers to weaken the inter-diffusion rate of molten aluminum and matrix, which leads to the improvement of the corrosion resistance [34,38]. However, when the immersion time is longer than 4 h, the intermetallic thickness of H13 steel is decreased. The most important reason to explain the phenomenon is the initiation and propagation of micro-cracks in the corrosion layer, which accelerates the IMC corrosion and spallation. The results are consistent with the weight loss rates, as shown in Figure 5.

3.4. Corrosion Products

As shown in Figure 6a–d, PLSs obviously appear between Cr-rich borides and molten aluminum. To understand the element distributions in PLS, the EPMA line analysis of a typical sample of M3 along the line segment AE is presented in Figure 8. The results indicate that the Cr and Mo elements are mostly distributed in the borides (Figure 8a,c,e). The concentration variations of the Cr, Mo and B elements are different from those of Fe in the IMC layers. Additionally, the PLSs are generated at the interface between the molten aluminum and the Cr-rich borides (Figure 8a,c,d) rather than at the Mo-rich boride interface (Figure 8b–d). It can be inferred that the interfacial reaction takes place between the Cr-rich boride and the molten aluminum. In our previous study [34], the Cr-rich boride reacted with molten aluminum through the following reaction: (Cr, Fe)2B + Al → Cr-Al-B + Fe-Al. Although the Cr-rich boride and the Mo-rich boride present a superior corrosion resistance to molten aluminum, both were eventually corroded and were then embedded in the Fe-Al IMCs, playing a key role in protecting the Fe-Al IMC from spalling off.
To explore the corrosion products of the different borides of M4 alloy immersed in molten aluminum at 750°C for 8 h, the XRD and SEM-EDS analysis results are used to characterize these phenomena. From the XRD pattern of the corrosion layer (Figure 9a), it can be clearly found that the corrosion layer mainly consists of (Fe, Cr, Mo)4Al13, (Fe, Cr, Mo)2Al5 and exfoliated M2B-type boride. Figure 9b shows that net-like eutectic Cr-rich borides are present the PLSs morphology under the attack of molten aluminum. This kind of PLSs is tiny and local, which is different from those of the samples of M1-M3 (Figure 6a–c) that were corroded in molten aluminum. Additionally, the PLSs are changed into tiny particles and even dissolve under the long reaction time and thermal attack from the molten aluminum (Figure 9d,e). By observing Figure 9c, it can be seen that the blocky Mo-rich M2B boride phase distributes into the corrosion layer (owing to the corrosion of the supporting point of matrix) and keeps the original form, which indicates that this phase has outstanding corrosion resistance in molten aluminum. From the Mo-rich borides in the corrosion layer, it can be inferred that the Mo element can enhance the thermal stability of Fe2B in molten aluminum. It has been reported that Cr and Mo atoms can substitute Fe atoms and can form M2B-type borides, which could improve the fracture toughness of the Fe2B phase [21,22,27,39]. Additionally, from the longitudinal interfacial corrosion layer (Figure 9d), it also can be observed that there are some grainy corrosion products. Figure 9e is the high magnification view of these grainy zones marked with rectangle. The average composition of the grainy zone at point 1 measured by WDX is as follows: 39.34 wt.% Cr, 50.56 wt.% Al, 7.72 wt.% B and 2.35 wt.% Fe. It can be inferred that they are the Cr-Al-B IMCs. From the line scanning of these zones in Figure 9f, it can be easily found that the content of Cr and Fe shows an opposite trend of variation, which also proves the composition of the grainy phase.
To further understand the phase composition, the Bright-field TEM micrographs and corresponding SADPs of corrosion products were also be conducted. The corresponding chemical compositions of all the phases are shown in Table 3. The TEM analysis on SADPs taken from columnar zone (Figure 10a,c) can be indexed to a monoclinic structure, and it belongs to C2 space group and Fe4Al13-type structure (a = 1.5489 nm, b = 0.8083nm, c = 1.2476 nm). The interplanar distance of the (200) plane for (Fe, Cr, Mo)4Al13 is 0.7410 nm, which is also in good agreement with the XRD results (d(200) = 0.7378 nm). From the Figure 10b, it can be seen some corrosion products are roughly parallel to each other, and the corresponding SADPs result (Figure 10d) reflects a typical polycrystalline area. According to the chemical composition analysis of E region (Table 3), it is obvious that they are the Cr-Al-B intermetallic. It may be inferred that they belong to the PLSs corrosion products produced from the Cr-rich M2B boride. However, according to the isothermal section of Cr-Al-B system [40], it was acknowledged that there were three ternary stoichiometric intermetallics, AlCr2B2, AlCr3B4 and AlCr3B7. Therefore, the further study will be needed to clarify the formation mechanism of PLS and the crystal structure of Cr-Al-B intermetallic.
Figure 11 shows the elemental X-ray mapping distribution of M4 after the corrosion test for 8 h at 750 °C, as analyzed using EPMA analysis. The results clearly show the distribution of Fe, Cr, B, Mo, and Al atoms. Observing the (Cr, Fe)2B (Figure 11b–d) and Mo-rich M2B (Figure 11c–e) reveals that both of them have the effect of retarding the corrosion rate of molten aluminum by functioning as diffusion barriers. Similarly, Mo-rich and Cr-rich borides also encounter the dissolution, diffusion, and spallation stages as the immersion time extends. As observed in Figure 11a,c,d, the tiny PLSs contain atoms of Cr, Al, and B, which agrees with the EPMA (Figure 8e,f) and TEM analysis results (Figure 10b,d). As previously mentioned, observing Figure 11c–f evidently shows that the Mo-rich borides have an excellent corrosion resistance. On the one hand, these borides can protect the substrate from the high temperature molten aluminum diffusion and dissolution (Figure 11a,e,f). On the other hand, when the substrate is corroded, the Mo-rich borides will lose the attachment points and will drop into the molten aluminum, forming the transition layer. The combination mode of Mo-rich borides and molten aluminum is not a kind of physical bond but is a metallurgical bond, resulting in the formation of Al-B polar covalent bonds and Al-Mo metallic bonds [41]. This kind of bonding has a strong binding force, which likely hinders the IMC from falling off. Additionally, Figure 11a,f shows that there are no Al elements in the cracks, which indicates that the formation of cracks does not occur during the immersion process or that it may occur during the solidification and machining processes. In light of these observations, the Cr-rich borides and Mo-rich borides may play a synergistic role in discouraging the molten aluminum from further diffusion and reducing the interfacial corrosion rate of the metal substrate.
The Nernst-Shchukarev equation [42,43], which describes the dissolution of a solid metal in a molten metal, can be written as
dC/dt = K·A/V·(Cs − C)
where C is the instantaneous concentration of the dissolved metal in the melt, Cs is the saturation concentration, K is the dissolution rate constant, A is the surface area of the solid metal, and V is the volume of the melt. In the integrated form, Equation (1) becomes (initial conditions: C = 0, t = 0)
C = Cs[1 − exp(−K·A·t/V)]
Equations (1) and (2) indicate that if the volume of the molten metal is small, the dissolution of the solid metal will increase, and then the dissolution rate dC/dt will decrease. In contrast, if the volume of molten metal is larger, as in an industrial hot-dip bath, the dissolution rate dC/dt will be constant [43]. As is reported in the literature [28], for the corrosion of Mo, Nb, Cr, and Y that is immersed in a small volume of molten aluminum, the dissolution rate dC/dt decreases with time, which is also consistent with the results in this research (Figure 6).

3.5. Corroded Surface

Figure 12a–e shows the morphologies of the corroded surfaces of M1-M4 alloy and H13 steel after removing the residual aluminum using a 10% NaOH solution and Figure 12f shows the morphology after the removal of the intermetallic layer of M4 alloy. It can be seen that the morphologies of M1-M4 alloy and H13 steel are obviously different from each other. Some columnar structures (where the arrows are pointed in Figure 12) appear in the IMC layers. It may be inferred that they are the corroded rod-like (Cr, Fe)2B. Additionally, the PLSs are also shown in Figure 12b, which are embedded into the Fe-Al IMCs. However, owing to the rough surface, not every corrosion layer that can be found in the PLSs. As observed in the Mo addition alloys, M2-M4, especially M4 (Figure 12d), more columnar structures appear in the IMC layer, and they can act as nails to protect the Fe-Al IMCs from spalling off. Interestingly, from the high magnification views that are marked by white rectangles, there exist some fold structures of Mo-rich M2B in the Fe-Al IMC layer. Similarly, to a certain extent, these fold structures can hinder the atomic inter-diffusion of the substrate and molten aluminum. In contrast, the corroded surface morphology of H13 has many micro-cracks (Figure 12e). These micro-cracks exist and can act as liquid channels to accelerate the substrate corrosion and the spallation of Fe-Al IMCs under the attack of molten aluminum [13]. Furthermore, after removing the corrosion layer of the sample M4, it can be clearly found that numbers of rod-like (Cr, Fe)2B and the blocky Mo-rich M2B, which are similar to “tree roots”, fasten the matrix tightly (Figure 12f), which can contribute to hindering the matrix corrosion effectively.
Based on the previous investigation of Fe-Cr-B alloys in molten aluminum, the corrosion process can be divided into the following three processes: the dissolution of matrix, formation, and spallation of Fe-Al IMCs at the interface, and the spallation of the boride phase. On the basis of the experiment results, the novel Fe-Cr-B-Mo alloy with 8.3 wt.% Mo addition exhibits a better corrosion resistance to molten aluminum than that of H13 steel. The reasons for this result may be ascribed to the following two points. First, the M2B-type boride, especially the rod-like (Cr, Fe)2B and the blocky Mo-rich M2B boride, show a slower reaction rate with molten aluminum. Second, both borides can act as roots to capture the Fe-Al IMCs and prevent them from spalling off.

4. Conclusions

This work mainly investigated the influence of Mo addition on interfacial morphologies and the corrosion resistances of Fe-Cr-B alloys in static molten aluminum at 750 °C. The results are summarized as follows:
(1)
Mo addition plays an important role in the morphology of M2B-type borides. The microstructures of Mo-rich M2B borides change from a local net-like eutectic structure to a typical coarse dendritic structure and appear a kind blocky hypereutectic structure with the increase of Mo content.
(2)
The corrosion resistance of the M4 sample with an 8.3 wt.% Mo content is 3.8 times higher than that of H13 immersed in molten aluminum due to its blocky Mo-rich M2B boride and rod-like (Cr, Fe)2B.
(3)
The various M2B-type borides phases result in a synergistic effect that retards the corrosion of molten aluminum and presents a much slower corrosion rate than the matrix.
(4)
The Mo-rich M2B boride, rod-like (Cr, Fe)2B and its corrosion products of PLSs can act as roots to capture the Fe-Al IMCs and to prevent them from spalling off.

Author Contributions

The author W.C. provides helpful discussions and modification on the article; the author X.Z. and J.L. provide helpful discussions on microstructure observation; the authors W.X. and T.L. provide material characterization and the samples processing; the author Z.L. does the experiment and writes the article.

Funding

National Natural Science Foundation of China (Grant Nos. 51701053, 51271080).

Acknowledgments

The authors wish to acknowledge the financial support by the National Natural Science Foundation of China (Grant Nos. 51701053, 51271080).

Conflicts of Interest

The authors declare no conflict of interest.

References

  1. Balloy, D.; Tissier, J.C.; Giorgi, M.L.; Briant, M. Corrosion mechanisms of steel and cast iron by molten aluminum. Metall. Mater. Trans. A 2010, 41, 2366–2376. [Google Scholar] [CrossRef]
  2. Wang, D.; Shi, Z.; Zou, L. A liquid aluminum corrosion resistance surface on steel substrate. Appl. Surf. Sci. 2003, 214, 304–311. [Google Scholar]
  3. Shankar, S.; Apelian, D. Die soldering: Mechanism of the interface reaction between molten aluminum alloy and tool steel. Metall. Mater. Trans. B 2002, 33, 465–476. [Google Scholar] [CrossRef]
  4. Song, J.; Wang, X.; DenOuden, T.; Han, Q. Evolution of intermetallic phases in soldering of the die casting of aluminum alloys. Metall. Mater. Trans. A 2016, 47, 2609–2615. [Google Scholar] [CrossRef]
  5. Li, Y.; Tang, N.; Tunthawiroon, P.; Koizumi, Y.; Chiba, A. Characterisation of oxide films formed on Co–29Cr–6Mo alloy used in die-casting moulds for aluminium. Corros. Sci. 2013, 73, 72–79. [Google Scholar] [CrossRef]
  6. López, A.J.; Rams, J. Protection of carbon steel against molten aluminum attack and high temperature corrosion using high velocity oxygen-fuel WC–Co coatings. Surf. Coat. Technol. 2015, 262, 123–133. [Google Scholar] [CrossRef]
  7. Tunthawiroon, P.; Li, Y.; Tang, N.; Chiba, A. Enhancement of corrosion resistance of Fe–Cr–Mo alloy to molten Al by thermal oxidation in air. Corros. Sci. 2013, 77, 97–102. [Google Scholar] [CrossRef]
  8. Zhang, X.; Chen, W.; Luo, H.; Li, S.; Zhou, T.; Shi, L. Corrosion resistance and interfacial morphologies of novel Fe-Cr-Mo-B cast steels in molten aluminum. Corros. Sci. 2017, 125, 20–28. [Google Scholar] [CrossRef]
  9. Shahverdi, H.R.; Ghomashchi, M.R.; Shabestari, S.; Hejazi, J. Kinetics of interfacial reaction between solid iron and molten aluminium. J. Mater. Sci. 2002, 37, 1061–1066. [Google Scholar] [CrossRef]
  10. Bouayad, A.; Gerometta, C.; Belkebir, A.; Ambari, A. Kinetic interactions between solid iron and molten aluminium. Mater. Sci. Eng. A 2003, 363, 53–61. [Google Scholar] [CrossRef]
  11. Tanaka, Y.; Kajihara, M. Kinetics of isothermal reactive diffusion between solid Fe and liquid Al. J. Mater. Sci. 2010, 45, 5676–5684. [Google Scholar] [CrossRef]
  12. Bouche, K.; Barbier, F.; Coulet, A. Intermetallic compound layer growth between solid iron and molten aluminium. Mater. Sci. Eng. A 1998, 249, 167–175. [Google Scholar] [CrossRef]
  13. Rezaei, H.; Akbarpour, M.R.; Shahverdi, H.R. Effects of Interfacial Layers Fracture on the Dissolution Mechanism of Solid Fe in Liquid Al. JOM 2015, 67, 1443–1450. [Google Scholar] [CrossRef]
  14. Bobzin, K.; Brögelmann, T.; Brugnara, R.H.; Kruppe, N.C. CrN/AlN and CrN/AlN/Al2O3 coatings deposited by pulsed cathodic arc for aluminum die casting applications. Surf. Coat. Technol. 2015, 284, 222–229. [Google Scholar] [CrossRef]
  15. Khan, F.F.; Bae, G.; Kang, K.; Kumar, S.; Jeong, T.; Lee, C. Development of cermet coatings by kinetic spray technology for the application of die-soldering and erosion resistance. Surf. Coat. Technol. 2009, 204, 345–352. [Google Scholar] [CrossRef]
  16. Wang, D.; Shi, Z. Aluminizing and oxidation treatment of 1Cr18Ni9 stainless steel. Appl. Surf. Sci. 2004, 227, 255–260. [Google Scholar] [CrossRef]
  17. Chang, S.H.; Lin, Y.K.; Huang, K.T. Study on the thermal erosion, wear and corrosion behaviors of TiAlN/oxynitriding duplex-treated AISI H13 alloy steel. Surf. Coat. Technol. 2012, 207, 571–578. [Google Scholar] [CrossRef]
  18. Wang, Y.; Xing, J.; Ma, S.; Liu, G.; He, Y.; Yang, D.; Bai, Y. Effect of Fe2B orientation on erosion–corrosion behavior of Fe–3.5 wt.% B steel in flowing zinc. Corros. Sci. 2015, 98, 240–248. [Google Scholar] [CrossRef]
  19. Ma, S.; Xing, J.; Fu, H.; Yi, D.; Zhi, X.; Li, Y. Effects of boron concentration on the corrosion resistance of Fe–B alloys immersed in 460 C molten zinc bath. Surf. Coat. Technol. 2010, 204, 2208–2214. [Google Scholar] [CrossRef]
  20. Tsipas, D.N.; Triantafyllidis, G.K.; Kiplagat, J.K.; Psillaki, P. Degradation behaviour of boronized carbon and high alloy steels in molten aluminium and zinc. Mater. Lett. 1998, 37, 128–131. [Google Scholar] [CrossRef]
  21. Jian, Y.; Huang, Z.; Xing, J.; Wang, B. Effects of chromium addition on fracture toughness and hardness of oriented bulk Fe2B crystals. Mater. Charact. 2015, 110, 138–144. [Google Scholar] [CrossRef]
  22. Huang, Z.; Xing, J.; Guo, C. Improving fracture toughness and hardness of Fe2B in high boron white cast iron by chromium addition. Mater. Des. 2010, 31, 3084–3089. [Google Scholar] [CrossRef]
  23. Liu, Y.; Li, B.; Li, J.; He, L.; Gao, S.; Nieh, T.G. Effect of titanium on the ductilization of Fe–B alloys with high boron content. Mater. Lett. 2010, 64, 1299–1301. [Google Scholar] [CrossRef]
  24. Fu, H.; Xiao, Q.; Kuang, J.; Jiang, Z.; Xing, J.D. Effect of rare earth and titanium additions on the microstructures and properties of low carbon Fe–B cast steel. Mater. Sci. Eng. A 2007, 466, 160–165. [Google Scholar] [CrossRef]
  25. Huang, Z.; Xing, J.; Lv, L. Effect of tungsten addition on the toughness and hardness of Fe2B in wear-resistant Fe–B–C cast alloy. Mater. Charact. 2013, 75, 63–68. [Google Scholar] [CrossRef]
  26. Han, F.; Hwang, B.; Suh, D.W.; Wang, Z.; Lee, D.L.; Kim, S.J. Effect of molybdenum and chromium on hardenability of low-carbon boron-added steels. Met. Mater. Int. 2008, 14, 667. [Google Scholar] [CrossRef]
  27. Tunca, N.; Delamore, G.W.; Smith, R.W. Corrosion of Mo, Nb, Cr, and Y in molten aluminum. Metall. Trans. A 1990, 21, 2919–2928. [Google Scholar] [CrossRef]
  28. Takahashi, J.; Ishikawa, K.; Kawakami, K.; Fujioka, M.; Kubota, N. Atomic-scale study on segregation behavior at austenite grain boundaries in boron-and molybdenum-added steels. Acta Mater. 2017, 133, 41–54. [Google Scholar] [CrossRef]
  29. Ma, S.; Xing, J.; Fu, H.; Gao, Y.; Zhang, J. Microstructure and crystallography of borides and secondary precipitation in 18 wt.% Cr–4 wt.% Ni–1 wt.% Mo–3.5 wt.% B–0.27 wt.% C steel. Acta Mater. 2012, 60, 831–843. [Google Scholar] [CrossRef]
  30. Röttger, A.; Lentz, J.; Theisen, W. Boron-alloyed Fe–Cr–C–B tool steels—Thermodynamic calculations and experimental validation. Mater. Des. 2015, 88, 420–429. [Google Scholar] [CrossRef]
  31. Jahazi, M.; Jonas, J.J. The non-equilibrium segregation of boron on original and moving austenite grain boundaries. Mater. Sci. Eng. A 2002, 335, 49–61. [Google Scholar] [CrossRef]
  32. Faulkner, R.G. Non-equilibrium grain-boundary segregation in austenitic alloys. J. Mater. Sci. 1981, 16, 373–383. [Google Scholar] [CrossRef]
  33. Christodoulou, P.; Calos, N. A step towards designing Fe–Cr–B–C cast alloys. Mater. Sci. Eng. A 2001, 301, 103–117. [Google Scholar] [CrossRef]
  34. Zhang, X.; Chen, W.; Luo, H.; Zhou, T. Formation of periodic layered structure between novel Fe-Cr-B cast steel and molten aluminum. Scr. Mater. 2017, 130, 288–291. [Google Scholar] [CrossRef]
  35. Ma, S.; Xing, J.; Fu, H.; He, Y.; Bai, Y.; Li, Y.; Bai, Y. Interface characteristics and corrosion behaviour of oriented bulk Fe2B alloy in liquid zinc. Corros. Sci. 2014, 78, 71–80. [Google Scholar] [CrossRef]
  36. Ma, S.; Xing, J.; Fu, H.; Yi, D.; Li, Y.; Zhang, J.; Zhu, B.; Gao, Y. Microstructure and interface characteristics of Fe–B alloy in liquid 0.25 wt.% Al–Zn at various bath temperatures. Mater. Chem. Phys. 2012, 132, 977–986. [Google Scholar] [CrossRef]
  37. Miller, A.E.; Maijer, D.M. Investigation of erosive-corrosive wear in the low pressure die casting of aluminum A356. Mater. Sci. Eng. A 2006, 435, 100–111. [Google Scholar] [CrossRef]
  38. Zhang, X.; Li, X.; Chen, W. Interfacial reactions of duplex stainless steels with molten aluminum. Surf. Interface Anal. 2015, 47, 648–656. [Google Scholar] [CrossRef]
  39. Huang, Z.; Xing, J.; Tao, X. Effect of molybdenum addition on fracture toughness and hardness of Fe2B in Fe–B–C cast alloy. Int. J. Mater. Res. 2012, 103, 1539–1543. [Google Scholar] [CrossRef]
  40. Campbell, C.E.; Kattner, U.R. Assessment of the Cr-B system and extrapolation to the Ni-Al-Cr-B quaternary system. Calphad 2002, 26, 477–490. [Google Scholar] [CrossRef]
  41. Abdelkader, H.S.; Faraoun, H.I. Ab initio investigation of Al/MoB interfacial adhesion. Comput. Mater. Sci. 2011, 50, 880–885. [Google Scholar] [CrossRef]
  42. Dybkov, V.I. Interaction of 18Cr-10Ni stainless steel with liquid aluminium. J. Mater. Sci. 1990, 25, 3615–3633. [Google Scholar] [CrossRef]
  43. Liu, X.; Barbero, E.; Xu, J.; Burris, M.; Chang, K.M.; Sikka, V. Liquid metal corrosion of 316L, Fe3Al, and FeCrSi in molten Zn-Al baths. Metall. Mater. Trans. A 2005, 36, 2049–2058. [Google Scholar] [CrossRef]
Materials 12 00256 g001 550
Figure 1. Schematic diagram of the corrosion test device.
Figure 1. Schematic diagram of the corrosion test device.
Materials 12 00256 g001
Materials 12 00256 g002 550
Figure 2. X-ray diffractometer (XRD) patterns of the as-cast Fe-Cr-B alloys with various Mo additions.
Figure 2. X-ray diffractometer (XRD) patterns of the as-cast Fe-Cr-B alloys with various Mo additions.
Materials 12 00256 g002
Materials 12 00256 g003 550
Figure 3. Back-scattered electron (BSE) images of the Fe-Cr-B alloys with various Mo additions: (a) 0 wt.% Mo; (b) 3.22 wt.% Mo; (c) 6.19 wt.% Mo; (d) 8.30 wt.% Mo.
Figure 3. Back-scattered electron (BSE) images of the Fe-Cr-B alloys with various Mo additions: (a) 0 wt.% Mo; (b) 3.22 wt.% Mo; (c) 6.19 wt.% Mo; (d) 8.30 wt.% Mo.
Materials 12 00256 g003
Materials 12 00256 g004 550
Figure 4. Transmission electron microscopy (TEM) analysis of alloy M4: (a–c) Bright-field TEM micrographs and corresponding SADPs of borides and matrix: (d) corresponding SADPs from primary Cr-rich M2B boride reflected from [0 3 ¯ 3], (e) corresponding SADPs from eutectic Cr-rich M2B boride reflected from [004], (f) corresponding SADPs from α-(Fe, Cr) matrix reflected from [002], (g) corresponding SADPs from Mo-rich M2B boride reflected from [2 2 ¯ 0].
Figure 4. Transmission electron microscopy (TEM) analysis of alloy M4: (a–c) Bright-field TEM micrographs and corresponding SADPs of borides and matrix: (d) corresponding SADPs from primary Cr-rich M2B boride reflected from [0 3 ¯ 3], (e) corresponding SADPs from eutectic Cr-rich M2B boride reflected from [004], (f) corresponding SADPs from α-(Fe, Cr) matrix reflected from [002], (g) corresponding SADPs from Mo-rich M2B boride reflected from [2 2 ¯ 0].
Materials 12 00256 g004
Materials 12 00256 g005 550
Figure 5. Weight loss per square centimeter of the samples per minute in molten aluminum at 750 °C for different corrosion times.
Figure 5. Weight loss per square centimeter of the samples per minute in molten aluminum at 750 °C for different corrosion times.
Materials 12 00256 g005
Materials 12 00256 g006 550
Figure 6. Cross-sectional BSE images of corrosion layers corroded by molten aluminum at 750 °C for 8 h: (a) M1; (b) M2; (c) M3; (d) M4; (e) H13. The top right corner images are the high magnification views of the images that are marked with rectangles.
Figure 6. Cross-sectional BSE images of corrosion layers corroded by molten aluminum at 750 °C for 8 h: (a) M1; (b) M2; (c) M3; (d) M4; (e) H13. The top right corner images are the high magnification views of the images that are marked with rectangles.
Materials 12 00256 g006
Materials 12 00256 g007 550
Figure 7. Relationship between the IMC thickness and the corrosion time compared with the interfacial corrosion morphologies of M4 and H13 that were corroded by molten aluminum at 750 °C.
Figure 7. Relationship between the IMC thickness and the corrosion time compared with the interfacial corrosion morphologies of M4 and H13 that were corroded by molten aluminum at 750 °C.
Materials 12 00256 g007
Materials 12 00256 g008 550
Figure 8. EPMA analysis of the corrosion layer along line segment AE for sample M3 at 750 °C for 8 h in molten aluminum; (a) BEI; (b) Fe; (c) Cr; (d) B; (e) Mo; (f) Al.
Figure 8. EPMA analysis of the corrosion layer along line segment AE for sample M3 at 750 °C for 8 h in molten aluminum; (a) BEI; (b) Fe; (c) Cr; (d) B; (e) Mo; (f) Al.
Materials 12 00256 g008
Materials 12 00256 g009 550
Figure 9. The characterization of the corrosion products layer: (a) the XRD pattern of the cross-sectional corrosion layer; (b,c) BSE images of cross-sectional interfacial layer; (d) the longitudinal interfacial layer; (e) magnification view of the grainy Cr-Al-B IMCs; (f) EDX line analysis in (e).
Figure 9. The characterization of the corrosion products layer: (a) the XRD pattern of the cross-sectional corrosion layer; (b,c) BSE images of cross-sectional interfacial layer; (d) the longitudinal interfacial layer; (e) magnification view of the grainy Cr-Al-B IMCs; (f) EDX line analysis in (e).
Materials 12 00256 g009
Materials 12 00256 g010 550
Figure 10. TEM images of the corrosion products of alloy M4 in molten aluminum for 8h: (a,b) Bright-field TEM micrographs and corresponding SADPs of corrosion products: (c) corresponding SADPs from (Fe, Cr, Mo)4Al13 reflected from [002], (d) corresponding SADPs from Cr-Al-B IMCs.
Figure 10. TEM images of the corrosion products of alloy M4 in molten aluminum for 8h: (a,b) Bright-field TEM micrographs and corresponding SADPs of corrosion products: (c) corresponding SADPs from (Fe, Cr, Mo)4Al13 reflected from [002], (d) corresponding SADPs from Cr-Al-B IMCs.
Materials 12 00256 g010
Materials 12 00256 g011 550
Figure 11. Elemental X-ray mapping distribution of alloy M4 after corrosion test for 8 h at 750 °C: (a) interfacial corrosion layer morphology; (b) Fe; (c) Cr; (d) B; (e) Mo; (f) Al.
Figure 11. Elemental X-ray mapping distribution of alloy M4 after corrosion test for 8 h at 750 °C: (a) interfacial corrosion layer morphology; (b) Fe; (c) Cr; (d) B; (e) Mo; (f) Al.
Materials 12 00256 g011
Materials 12 00256 g012 550
Figure 12. Morphologies of the corroded surface after removing the residual aluminum with a 10% NaOH solution: (a) M1; (b) M2; (c) M3; (d) M4; (e) H13, and the morphology after removing the IMC layer of M4 (f). All the samples were immersed in molten aluminum for 8 h at 750 °C.
Figure 12. Morphologies of the corroded surface after removing the residual aluminum with a 10% NaOH solution: (a) M1; (b) M2; (c) M3; (d) M4; (e) H13, and the morphology after removing the IMC layer of M4 (f). All the samples were immersed in molten aluminum for 8 h at 750 °C.
Materials 12 00256 g012
Table
Table 1. Chemical compositions (in wt.%) of Fe-Cr-B cast steels and the H13 steel.
Table 1. Chemical compositions (in wt.%) of Fe-Cr-B cast steels and the H13 steel.
ElementsCBCrMoSiAlMnCuVFe
M10.253.6813.5400.730.440.320.130.07Bal.
M20.263.4214.733.220.980.790.310.170.05Bal.
M30.263.1215.286.191.130.970.320.250.10Bal.
M40.283.1916.358.301.210.850.340.240.07Bal.
H130.38-5.301.301.00-0.40-0.90Bal.
Table
Table 2. The average composition (in at.%) of M2B-type boride (M = Fe, Cr, Mo) in Fe-Cr-B cast steels measured by using wavelength dispersive X-ray (WDX) at each point in Figure 3a–d.
Table 2. The average composition (in at.%) of M2B-type boride (M = Fe, Cr, Mo) in Fe-Cr-B cast steels measured by using wavelength dispersive X-ray (WDX) at each point in Figure 3a–d.
NumberFeCrBMoCalculated Formula
137.36 ± 1.4129.38 ± 0.3433.26 ± 1.800Fe1.12Cr0.88B
244.55 ± 1.2422.29 ± 1.2333.16 ± 2.400Fe1.34Cr0.68B
327.81 ± 0.9519.16 ± 0.8534.74 ± 0.9618.29 ± 0.78Fe0.80Cr0.55Mo0.53B
425.26 ± 1.0519.79 ± 0.9430.94 ± 1.5024.01 ± 1.30Fe0.82Cr0.64Mo0.78B
521.84 ± 0.8017.36 ± 0.2837.11 ± 1.2523.69 ± 1.45Fe0.59Cr0.47Mo0.64B
Table
Table 3. Chemical composition (in at.%) of the phases (in Figure 10a,b) in the corrosion products of M4 analyzed by TEM-EDS.
Table 3. Chemical composition (in at.%) of the phases (in Figure 10a,b) in the corrosion products of M4 analyzed by TEM-EDS.
RegionsFeCrBMoAlPhases
A23.151.0800.2375.54(Fe, Cr, Mo)4Al13
B19.771.9410.260.2167.82(Fe, Cr, Mo)4Al13
C25.192.0700.4372.31(Fe, Cr, Mo)2Al5
D18.3015.3243.6221.641.12Mo-rich boride
E1.2422.3321.08055.32Cr-Al-B IMC

Share and Cite

MDPI and ACS Style

Ling, Z.; Chen, W.; Xu, W.; Zhang, X.; Lu, T.; Liu, J. The Influence of A Mo Addition on the Interfacial Morphologies and Corrosion Resistances of Novel Fe-Cr-B Alloys Immersed in Molten Aluminum. Materials 2019, 12, 256. https://doi.org/10.3390/ma12020256

AMA Style

Ling Z, Chen W, Xu W, Zhang X, Lu T, Liu J. The Influence of A Mo Addition on the Interfacial Morphologies and Corrosion Resistances of Novel Fe-Cr-B Alloys Immersed in Molten Aluminum. Materials. 2019; 12(2):256. https://doi.org/10.3390/ma12020256

Chicago/Turabian Style

Ling, Zicheng, Weiping Chen, Weiye Xu, Xianman Zhang, Tiwen Lu, and Jian Liu. 2019. "The Influence of A Mo Addition on the Interfacial Morphologies and Corrosion Resistances of Novel Fe-Cr-B Alloys Immersed in Molten Aluminum" Materials 12, no. 2: 256. https://doi.org/10.3390/ma12020256

APA Style

Ling, Z., Chen, W., Xu, W., Zhang, X., Lu, T., & Liu, J. (2019). The Influence of A Mo Addition on the Interfacial Morphologies and Corrosion Resistances of Novel Fe-Cr-B Alloys Immersed in Molten Aluminum. Materials, 12(2), 256. https://doi.org/10.3390/ma12020256

Note that from the first issue of 2016, this journal uses article numbers instead of page numbers. See further details here.

Article Metrics

Back to TopTop