# Corrosion and Wear Properties of Composite Coatings Reinforced withTiB2 Particles Produced by PTA on Steel Substrate in Different Atmospheres

Authors: M. Darabara; L. Bourithis; S. Diplas; G. D. Papadimitriou
Journal: ISRN Corrosion
 (2012)

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## Abstract

Titanium diboride (TiB2) and titanium carbonitride (Ti(C,N)) coatings are widely used as reinforcing materials in applications demanding high corrosion and wear resistance. In this paper, plain carbon steel has been surface alloyed with TiB2 by plasma transferred arc (PTA) technique using two different gas atmospheres. The first metal matrix composite (MMC) is produced with TiB2 particles and argon as shielding and plasma gas. In addition, a mixture of Ar and 5% N2 was used as shielding and plasma gas for producing of second MMC coating. The microstructure of both alloyed layers consists of primary titanium boride particles surrounded by a eutectic matrix, containing ferrite, eutectic boride, and titanium carbonitrides. The presence of these carbonitrides is more intense in the case of the N-enriched alloyed layer, as it was also proved via X-ray Diffraction. The alloyed layers are susceptible to pitting corrosion in 3.5% NaCl or 1 N H2SO4. The alloyed layer produced with nitrogen mixture gas is slightly more noble than the one produced with pure Ar.  The metallic-ferritic matrix corrodes in 6%
FeCl3∗6H2O leaving TiB2 particles protruding from the matrix. The wear performance of both TiB2 MMC depends on the counterbody (tool steel or alumina ball).


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## Body

## 1. Introduction

Titanium diboride (TiB2) and titanium carbonitride (Ti(C,N)) hard coatings are widely used in applications demanding high corrosion and wear resistance. As titanium has a strong affinity for boron nitrogen and carbon, it combines with these elements in order to form stable titanium borides, nitrides, and carbonitrides, which can be successfully used as reinforcing materials in metal matrix composites (MMCs). In previous studies, TiN and Ti(C,N) coatings are incorporated on various substrates by cathodic arc ion plating process [1, 2], physical vapour deposition [3], and plasma-assisted chemical vapour deposition [4]. In addition, TiB2 particles reinforce different substrates by electron beam [5, 6], laser [7–11], or pulsed electrode surfacing [10–12] techniques.In this study, two different metal matrix composites reinforced with TiB2 are produced on a plain carbon steel substrate by plasma transferred arc (PTA) technique. The first metal matrix composite (MMC) is reinforced with TiB2 particles, while the second one is a nitrogen-enriched TiB2 MMC. The reinforcement with TiB2 particles is achieved by particles of the initial TiB2 powder, whereas the nitrogen is incorporated into the steel surface from the plasma and shielded gas, which is a mixture of Ar and 5% N2. Following their production, the alloyed layers are characterized in respect to their microstructure and their corrosion and wear properties. In a final step, a comparison between the corrosion and wear properties of the produced alloyed layers is achieved.


## 2. Experimental

A plain carbon steel with chemical composition 0.2% wt C, 1.4%wt Mn, and 0.3%wt Si (AISI 1118) was used as the substrate material. Samples of50×50×14 mm were cut and polished with abrasive paper down to 1000 grit. Then they were covered with powder of pure TiB2 (grain size: 10 μm) by mixing the powder with alcohol and applying 0.13 g per cm2 on the surface of the samples. The covered samples were thereafter heated up to 60°C for 0.5 h for drying and then placed on a copper plate and scanned with plasma transferred arc. The samples were divided in two categories according to the chemistry of plasma and shielding gases used for the treatment. Under the name of “TiB2,” the specimens were scanned with pure argon as plasma and shielded gas and under the name of  “TiB2 + N,” with a mixture of argon and 5% nitrogen as plasma and shielded gas so as to achieve nitrogen absorption into the alloyed layer. The parameters of the process were carefully selected from a series of preliminary experiments [13] and are given in Table 1. More details regarding the equipment and process used are provided in a previous publication [14, 15].Table 1
P.T.A. operation parameters.
TiB2TiB2+ N (Nitrogen-enriched TiB2)Current I80 A80 AScanning speed2 mm/s2 mm/sElectrode set back0 mm0 mmWorking distance2.34 mm2.34 mmPlasma gas0.7 L/min Ar0.7 L/min Ar + 5% N2Shielding gas7.1 L/min Ar7.1 L/min Ar + 5% N2Electrode diameter (W-2% Ce2O)2.4 mm2.4 mmTip diameter2.36 mm2.36 mmLateral step2.34 mm2.34 mmAfter the treatment, some of the alloyed samples were cut and prepared for examination via optical and electron microscopy associated with EDS microanalysis in the SEM. X-ray diffraction was performed for the alloyed layers at room temperature using a Siemens 5000 diffractometer employing a monochromated Cu Kα radiation and 2θ range from 30° to 90° with 0.03 degrees steps and 1 s acquisition time for each step. Microhardness measurements were also provided for the alloyed layer by a microhardness Vickers tester with a load of 200 g for 15 s.Samples were also prepared for electrochemical corrosion tests in a cell filled with aqueous solutions of either 3.5% NaCl or 1 N H2SO4. The corrosion parameters (Ecorr and Icorr) of the alloyed layer were electrochemically determined by cyclic potentiodynamic polarization. Specimens with an exposed area of 1 cm2 were placed in the polarization cell for 1 h before initiating polarization so as their potential to be stabilized. The cell consisted of a reference platinum electrode and an AgCl counter electrode, as this is described in ASTM G5-94 standard. A polarization curve for each material was obtained in direct and reverse scans with a potential scan rate of 5 mV/min.Moreover, samples were also immersed in 6% FeCl3*6H2O aqueous solution in 50°C for 72 h as this is described in ASTM G48-99 standard for the pitting and crevice corrosion resistance of stainless steels and related alloys. The temperature was held stable for the desirable period by immersing the glasses with the samples into a water bath held at 50°C. After the period of 72 h, the samples were cleaned and were examined for pittings in stereoscope and scanning electron microscope.Furthermore, different samples were also prepared for wear testing using a pin-on-disc tribometer. The tests were conducted at room temperature according to ASTM G99-95A standard under loads of 4.9 N and 9.8 N and sliding velocities ranges from 0.15 to 0.60 m/s for a total covered distance for each test of 450 m. The specimens were placed on a rotating disc, whereas a ball of tool steel with 6 mm diameter and 900 HV hardness or alternatively a 6 mm ball of alumina with 1900 HV hardness was the stationary counterbody (pin). The friction coefficient was measured continuously through a load cell measuring the tangential force. For every set of conditions, three tests were done for reproducibility of the results. Each sample was examined with optical microscopy and profilometry so as to determine the wear rate and to assess the wear mechanisms.


## 3. Results and Discussion

### 3.1. Microstructure

Figure1(a) shows a representative overview of a cross section of the alloyed layers. As it can be seen, the alloyed layers are uniform without cracks or porosities. The isolated dark grey areas observed in this figure correspond to areas dense in TiB2 grains and are present at the extremities of individual PTA passes. The thickness of the melting zone of the TiB2sample varies between 0.75 and 1 mm, while the TiB2 + N sample has a thickness, which varies between 0.85 and 1.05 mm.SEI micrographs of (a) an overview of a cross section of the microstructure of the alloyed layer, (b) and (c) the interface between the alloyed layer TiB2 and TiB2 + N with the substrate, respectively. (The arrows point the end of melting zone and start of heat-affected zone).
(a)(b)(c)Both alloyed layers, TiB2 and TiB2 + N, are well bonded to the substrate without cracks or porosities observed in the interface between melting zone and heat-affected zone, as revealed by metallography (Figures 1(b) and 1(c). The heat affected zone exhibits a typical bainitic microstructure and has a thickness of about 1 mm.Figure2(a) shows the microstructure of the alloyed layer TiB2, which consists of primary titanium boride particles surrounded by an eutectic matrix, containing ferrite and eutectic boride. The diameter of the primary crystals is about 8±2 μm and that of the eutectic particles smaller than about 1 μm, as measured with an image analysis program. Primary and eutectic TiB2 particles have polygonal and almost hexagonal shape, characteristic of the hexagonal titanium diboride symmetry. As it can also be seen from Figure 2(a), some zones of the matrix, appearing as dark grey, are almost devoid of eutectic particles and usually come in direct contact with the primary titanium borides.(a) SEI micrograph of the microstructure of the alloyed layer TiB2, (b) higher magnification of the microstructure of layer TiB2, (c–f) elemental mappings of Ti, B, C, and N, respectively, of the region observed in Figure 2(b).
(a)(b)(c)(d)(e)(f)Higher magnification of the microstructure of the TiB2 alloyed layer, Figure 2(b), reveals that primary diboride particles are not homogeneous. In fact, there are some areas inside the primary TiB2 particles that have a light grey colour. The same areas are observed in the rest microstructure. This observation implies that there are compositional differences throughout the TiB2 grains and also the microstructure of the whole alloyed layer. Elemental mappings (Figure 2(c) to 2(f)) of the microstructure observed in Figure 2(b) show that some light grey areas, situated either inside the TiB2 particles or in the rest of the microstructure, are enriched in nitrogen and carbon (Figures 2(e) and 2(f), resp.). Especially inside the TiB2 particle, in regions rich in nitrogen and carbon, there is not boron, indicating the formation of a Ti(C,N) compound. The presence of these carbonitrides should be attributed to contamination from carbon coming mainly from the steel substrate and nitrogen coming from titanium diboride powder used as raw material in the process. Nitrogen, carbon, and other contaminants are usually absorbed on the surface of commercial titanium diboride, due to its high specific surface, associated to the fineness of the powder (in our case 10 μm) [16, 17].Figure3(a) shows the microstructure of the TiB2 + N alloyed layer. As in the case of TiB2 alloyed layer, this layer also consists of primary titanium boride particles surrounded by a eutectic matrix, containing ferrite and eutectic boride. Titanium diboride particles, primary and eutectic, appear as dark contrast particles, and they exhibit prismatic or near hexagonal sections. The diameter of the primary crystals is about 7±4 μm and that of the eutectic particles smaller than about 1 μm, as measured with an image analysis program.(a) SEI micrograph of the microstructure of the alloyed layer TiB2 + N, (b) high magnification of a region of the layer TiB2 + N depicting a TiB2 particle with light grey areas on it enriched in N and C.
(a)(b)In general, primary diboride particles are not homogeneous; as in Figure3(b), compositional differences can be observed into them. In fact, titanium diboride particles include some light grey areas that are enriched with nitrogen and carbon, as this is clarified by both EDS microanalyses on the SEM and elemental mappings. As a matter of fact, high Ti and B contents were found on the dark grey area of the primary TiB2 particle, whereas high N and C contents were found inside the light grey areas of the same grain (Figure 3(b)). This fact implies again the presence of Ti(C,N), as in the case of TiB2 layer. In this coating, the presence of carbonitrides should be attributed to the higher nitrogen contents absorbed by the coating due to the high N contents in the used plasma and shielded gas. Carbon should also come from the steel substrate.X-ray diffraction was used so as to clarify further the two different microstructures, Figure4. X-ray diffraction for the TiB2 alloyed layer reveals the presence of α-Fe (or possibly martensite), hexagonal TiB2, and a small amount of titanium carbonitrides, Ti(C,N), with cubic symmetry (a=4.26 Å). On the other hand, the XRD pattern of the TiB2+N alloyed layer shows peaks of α-Fe (or possibly martensite) and peaks of Ti(C,N), which are relatively high. It is worth noting that in the second layer, the Ti(C,N) peak overtops the ferrite peak. This fact means that a great amount of nitrogen is absorbed by the alloyed layer in order for the titanium to combine with it and to form carbonitrides. These titanium carbonitrides detected by X-ray diffraction presumably coincide with the light grey areas in the SEI images of Figures 2(b) and 3(b). As it can be clearly seen from the XRD patterns, only stable phases such as TiB2 and Ti(C,N) are produced with PTA technique, in contrast to laser alloying techniques, leading also to metastable phases with unknown properties [8–11].Figure 4
X-ray diffraction pattern of the alloyed layers.


### 3.2. Hardness Measurements

Microhardness tests performed in the melting zone of a cross section of the TiB2 alloyed layer give microhardness, which varies between 550 HV and 650 HV. In contrast, in the regions with dense TiB2 grains, the hardness increases and varies between 1200 HV and 1400 HV. On the other hand, the microhardness of the melting zone of TiB2 + N layer with uniform microstructure varies between 600 HV and 700 HV, while the microhardness in regions with dense TiB2 grains between 1200 HV and 1400 HV.The fluctuations in the microhardness within the same area of the alloyed layers must be attributed to the different hardness of the microstructural constituents combined in the composites. As titanium diboride is a ceramic material with high hardness, above 2500 HV [18], it results in the reinforcement of the coated material. Especially in the second layer, the high amount of titanium carbonitrides reinforces even more the ferritic matrix of the coating and increases its hardness. As a matter of fact, the macrohardness of the first alloyed layer is about 600 HV and of the second layer is about 700 HV. In areas with dense TiB2 particles, the macrohardness in both layers can reach 1000 HV.


### 3.3. Corrosion

Figures5(a) and 5(b) represent the cyclic potentiodynamic curves for the plain carbon steel and the alloyed layers in aqueous solutions of 3.5% NaCl and 1 N H2SO4, respectively. All curves exhibit positive hysteresis, given that in the reverse anodic scan the current density is higher than that for the forward scan. This fact confirms that both steel and the alloyed layers are susceptible to pitting corrosion.Cyclic polarization curves of the plain carbon steel and the alloyed layers in 3.5% NaCl and 1 N H2SO4solutions.
(a)(b)According to Figure5(a) and Table 2, the alloyed layers TiB2 and TiB2 + N in 3.5% NaCl are more noble than carbon steel, as they both have higher corrosion potential (Ecorr). Moreover, they exhibit lower current densities (Icorr), and thus they do not corrode as fast as plain carbon steel does. They do not also have a passive region observed in the polarization curve, as the potential continuously increases as the current increases too.Table 2
Potentiodynamic parameter values (Ecorr, Icorr) obtained for the alloyed layers.
3.5% NaCl1 N H2SO4Ecorr (mV)Icorr (A/cm2)Ecorr (mV)Icorr (A/cm2)Plain carbon steel−5243*10−6−3474*10−6TiB2−4209*10−7−1793*10−4TiB2+ N−3749*10−7−1643*10−4Similarly, the alloyed layers are nobler than steel in 1 N H2SO4 solution, as they have higher Ecorr than that of steel. The main difference between the two materials lies on their current density values that in the case of the alloyed layers seems to be a little higher than the plain steel. This fact implies that although the layers are nobler than steel, when they will begin to corrode, they will exhibit higher corrosion rates. In addition, all the tested materials do not passivate in 1 N H2SO4. A similar result was also found in the work of Munro [18] who attributed the absence of TiB2 passivation to the presence of the white film of tetravalent oxide titanium (TiO2*H2O) coming from the dissolution of TiB2.The alloyed layer TiB2 + N has slightly better corrosion behaviour than the alloyed layer TiB2, as it has higher corrosion potential values in the two tested solutions. As a matter of fact, following the corrosion experiments of both layers in 6% wt FeCl3*6H2O, the alloyed layer TiB2 + N was found again more resistant. Figures 6(a) and 6(b) present the surface of the coating TiB2, while Figures 6(c) and 6(d) present the corroded surface of the layer TiB2 + N. As it can be seen from the first two figures, layer TiB2 is totally detached from the substrate, leaving the steel substrate susceptible to corroded solutions. On the contrary, layer TiB2 + N is not totally detached from the substrate but presents cracks and corrosion signs. In fact, TiB2 particles are protruding from the matrix, which has been highly corroded (Figure 6(d)).SEI micrographs of the exposed surfaces of the alloyed layers to FeCl3 solution after corrosion experiments: (a, b) alloyed layer TiB2 and (c,d) alloyed layer TiB2 + N.
(a)(b)(c)(d)Generally speaking, the corrosion resistance of the alloyed layers is not highly improved by the TiB2 particles, because of the metallic ferritic matrix, which is considerably susceptible to pitting corrosion. This is also confirmed from the observation of the alloyed layer after corrosion experiments in the scanning electron microscope (Figure 6), where TiB2 particles are protruding from the ferritic matrix that has been consumed due to the corrosive environments. The presence of the metallic binder in the alloyed layers decreases the corrosion resistance, as it has also been studied elsewhere [19, 20].


### 3.4. Pin on Disk Wear Testing

Figure7(a) presents the wear rate of the alloyed layer TiB2 against the tool steel ball that is of the order 10−5mm3 volume loss per m of sliding distance. Increasing the sliding speed, the wear rate decreases slightly for the two applied loads, as it has also been found in another investigation [21]. At the same time, for higher applied loads, the wear rate increases. In addition, the wear rate for the tests with the Al2O3 ball, presented in Figure 7(b), is of the order of 10−4mm3 volume loss per m of sliding distance. In this case, the wear rate increases with increasing applied load, but it is not been affected by sliding speed.(a) Wear rates of the pair-alloyed layer TiB2-tool steel ball, (b) wear rates of the pair-alloyed layer TiB2-Al2O3 ball, (c) wear track for the pair-alloyed layer TiB2-tool steel ball, (d) SEM micrograph of the wear track for the pair-alloyed layer-alumina ball showing the plastic deformation of the alloyed layer and the presence of TiB2 particles protruding from the matrix.
(a)(b)(c)(d)The wear tracks after the tests with the tool steel ball are covered by a gray layer of oxide powder, Figure7(c), consisting oxygen, titanium, and iron, as this was confirmed by EDS microanalyses on the SEM. Examination of the worn surface of the tool steel ball reveals no sign of oxides or material transfer to the ball from the wear track. On the contrary, it is very clean and presents abrasion scars to the direction of movement. Moreover, for the pair, alloyed layer-Al2O3 ball, there is no sign of an oxide layer formed or material stack on the surface of the track. The matrix present deep scars and abrasive marks, while TiB2 particles are protruding from the matrix, Figure 7(d). The worn surface of the Al2O3 ball is partially covered with a black powder, apparently steel debris stack on the ball, and it has hills on its surface that act as cutting points for the alloyed layer. The high hardness of the alumina compared to the relative softer matrix of the alloyed layer favors the cutting action.The friction coefficient for the pair, alloyed layer TiB2-steel, was measured throughout the experiments and very stably attained the value of 0.12±0.01. This is a very low friction coefficient compared with that found elsewhere [11]. The oxide layer found on the surface of the wear tracks in combination with the decrease of the wear rate with increasing sliding speed and the low friction coefficient dominating the coating may be attributed leads to an active oxidation mechanism [22, 23]. On the contrary, the friction coefficient for the pair, alloyed layer TiB2-alumina ball, is 0.59±0.05 and is considerably higher than the one measured for the couple alloyed layer-tool steel. A similar friction coefficient was found in another work [24].The wear rate of the pair, alloyed layer TiB2 + N-tool steel ball, is presented in Figure 8(a). As it can be seen, the wear rate is of the order of 10−4mm3 volume loss per m of sliding distance, while it increases for higher applied loads and sliding speed values. The wear tracks after the tests exhibit plastic deformation and the presence of an oxide layer, while some areas have been removed from the alloyed layer. This removed material has been stuck on the steel ball, as according to EDS microanalyses on the SEM, oxygen, titanium, and iron found on the balls. Similarly, the wear rate of the pair, alloyed layer TiB2 + N—Al2O3 ball, presented in Figure 8(b), are again of the order of 10−4mm3 volume loss per m of sliding distance. As it can be seen, increasing applied load and increasing sliding speed result in increasing wear rate. The wear tracks after the tests present signs of oxide, Figure 8(c), and severe plastic deformation, Figure 8(d). The wear spot of the Al2O3 ball is partially covered with steel debris.(a) Wear track for the pair alloyed layer TiB2 + N-tool steel ball, (b) wear track for the pair alloyed layer TiB2 + N-alumina ball, (c) wear track for the pair alloyed layer TiB2-tool steel ball, (d) SEM micrograph of the wear track for the pair alloyed layer-alumina ball showing the plastic deformation of the alloyed layer and the presence of TiB2 particles protruding from the matrix.
(a)(b)(c)(d)The friction coefficient measured throughout almost all the experiments with tool steel ball was not stable. The plastic deformation in combination with material transfer from the alloyed layer to the ball leads to a relatively high friction coefficient (between 0.45 and 0.6). Similarly, for the pair layer-alumina, the friction coefficient did not remain stable and was fluctuated between the values measured for the couple alloyed layer-tool steel.Comparing the two different tribosystems for the alloyer layer TiB2, it can be postulated that the wear performance of the TiB2 MMC depends on the counterbody, since both wear mechanism and friction coefficient are quite different. The alumina ball, as it is harder than the steel ball, causes more damage to the alloyed layer but also alters the wear mechanism involved leading to higher friction coefficient. On the contrary, comparing the two different tribosystems for the alloyed layer TiB2 + N, it gets the conclusion that the wear performance of the nitrogen-rich TiB2 MMC is characterized by plastic deformation and formation of oxides for both tribosystems. Especially for the alloyed layer—tool steel system, the alloyed layer in every test condition underwent plastic deformation with detachment of material transferred and stuck to the ball surface.


## 3.1. Microstructure

Figure1(a) shows a representative overview of a cross section of the alloyed layers. As it can be seen, the alloyed layers are uniform without cracks or porosities. The isolated dark grey areas observed in this figure correspond to areas dense in TiB2 grains and are present at the extremities of individual PTA passes. The thickness of the melting zone of the TiB2sample varies between 0.75 and 1 mm, while the TiB2 + N sample has a thickness, which varies between 0.85 and 1.05 mm.SEI micrographs of (a) an overview of a cross section of the microstructure of the alloyed layer, (b) and (c) the interface between the alloyed layer TiB2 and TiB2 + N with the substrate, respectively. (The arrows point the end of melting zone and start of heat-affected zone).
(a)(b)(c)Both alloyed layers, TiB2 and TiB2 + N, are well bonded to the substrate without cracks or porosities observed in the interface between melting zone and heat-affected zone, as revealed by metallography (Figures 1(b) and 1(c). The heat affected zone exhibits a typical bainitic microstructure and has a thickness of about 1 mm.Figure2(a) shows the microstructure of the alloyed layer TiB2, which consists of primary titanium boride particles surrounded by an eutectic matrix, containing ferrite and eutectic boride. The diameter of the primary crystals is about 8±2 μm and that of the eutectic particles smaller than about 1 μm, as measured with an image analysis program. Primary and eutectic TiB2 particles have polygonal and almost hexagonal shape, characteristic of the hexagonal titanium diboride symmetry. As it can also be seen from Figure 2(a), some zones of the matrix, appearing as dark grey, are almost devoid of eutectic particles and usually come in direct contact with the primary titanium borides.(a) SEI micrograph of the microstructure of the alloyed layer TiB2, (b) higher magnification of the microstructure of layer TiB2, (c–f) elemental mappings of Ti, B, C, and N, respectively, of the region observed in Figure 2(b).
(a)(b)(c)(d)(e)(f)Higher magnification of the microstructure of the TiB2 alloyed layer, Figure 2(b), reveals that primary diboride particles are not homogeneous. In fact, there are some areas inside the primary TiB2 particles that have a light grey colour. The same areas are observed in the rest microstructure. This observation implies that there are compositional differences throughout the TiB2 grains and also the microstructure of the whole alloyed layer. Elemental mappings (Figure 2(c) to 2(f)) of the microstructure observed in Figure 2(b) show that some light grey areas, situated either inside the TiB2 particles or in the rest of the microstructure, are enriched in nitrogen and carbon (Figures 2(e) and 2(f), resp.). Especially inside the TiB2 particle, in regions rich in nitrogen and carbon, there is not boron, indicating the formation of a Ti(C,N) compound. The presence of these carbonitrides should be attributed to contamination from carbon coming mainly from the steel substrate and nitrogen coming from titanium diboride powder used as raw material in the process. Nitrogen, carbon, and other contaminants are usually absorbed on the surface of commercial titanium diboride, due to its high specific surface, associated to the fineness of the powder (in our case 10 μm) [16, 17].Figure3(a) shows the microstructure of the TiB2 + N alloyed layer. As in the case of TiB2 alloyed layer, this layer also consists of primary titanium boride particles surrounded by a eutectic matrix, containing ferrite and eutectic boride. Titanium diboride particles, primary and eutectic, appear as dark contrast particles, and they exhibit prismatic or near hexagonal sections. The diameter of the primary crystals is about 7±4 μm and that of the eutectic particles smaller than about 1 μm, as measured with an image analysis program.(a) SEI micrograph of the microstructure of the alloyed layer TiB2 + N, (b) high magnification of a region of the layer TiB2 + N depicting a TiB2 particle with light grey areas on it enriched in N and C.
(a)(b)In general, primary diboride particles are not homogeneous; as in Figure3(b), compositional differences can be observed into them. In fact, titanium diboride particles include some light grey areas that are enriched with nitrogen and carbon, as this is clarified by both EDS microanalyses on the SEM and elemental mappings. As a matter of fact, high Ti and B contents were found on the dark grey area of the primary TiB2 particle, whereas high N and C contents were found inside the light grey areas of the same grain (Figure 3(b)). This fact implies again the presence of Ti(C,N), as in the case of TiB2 layer. In this coating, the presence of carbonitrides should be attributed to the higher nitrogen contents absorbed by the coating due to the high N contents in the used plasma and shielded gas. Carbon should also come from the steel substrate.X-ray diffraction was used so as to clarify further the two different microstructures, Figure4. X-ray diffraction for the TiB2 alloyed layer reveals the presence of α-Fe (or possibly martensite), hexagonal TiB2, and a small amount of titanium carbonitrides, Ti(C,N), with cubic symmetry (a=4.26 Å). On the other hand, the XRD pattern of the TiB2+N alloyed layer shows peaks of α-Fe (or possibly martensite) and peaks of Ti(C,N), which are relatively high. It is worth noting that in the second layer, the Ti(C,N) peak overtops the ferrite peak. This fact means that a great amount of nitrogen is absorbed by the alloyed layer in order for the titanium to combine with it and to form carbonitrides. These titanium carbonitrides detected by X-ray diffraction presumably coincide with the light grey areas in the SEI images of Figures 2(b) and 3(b). As it can be clearly seen from the XRD patterns, only stable phases such as TiB2 and Ti(C,N) are produced with PTA technique, in contrast to laser alloying techniques, leading also to metastable phases with unknown properties [8–11].Figure 4
X-ray diffraction pattern of the alloyed layers.


## 3.2. Hardness Measurements

Microhardness tests performed in the melting zone of a cross section of the TiB2 alloyed layer give microhardness, which varies between 550 HV and 650 HV. In contrast, in the regions with dense TiB2 grains, the hardness increases and varies between 1200 HV and 1400 HV. On the other hand, the microhardness of the melting zone of TiB2 + N layer with uniform microstructure varies between 600 HV and 700 HV, while the microhardness in regions with dense TiB2 grains between 1200 HV and 1400 HV.The fluctuations in the microhardness within the same area of the alloyed layers must be attributed to the different hardness of the microstructural constituents combined in the composites. As titanium diboride is a ceramic material with high hardness, above 2500 HV [18], it results in the reinforcement of the coated material. Especially in the second layer, the high amount of titanium carbonitrides reinforces even more the ferritic matrix of the coating and increases its hardness. As a matter of fact, the macrohardness of the first alloyed layer is about 600 HV and of the second layer is about 700 HV. In areas with dense TiB2 particles, the macrohardness in both layers can reach 1000 HV.


## 3.3. Corrosion

Figures5(a) and 5(b) represent the cyclic potentiodynamic curves for the plain carbon steel and the alloyed layers in aqueous solutions of 3.5% NaCl and 1 N H2SO4, respectively. All curves exhibit positive hysteresis, given that in the reverse anodic scan the current density is higher than that for the forward scan. This fact confirms that both steel and the alloyed layers are susceptible to pitting corrosion.Cyclic polarization curves of the plain carbon steel and the alloyed layers in 3.5% NaCl and 1 N H2SO4solutions.
(a)(b)According to Figure5(a) and Table 2, the alloyed layers TiB2 and TiB2 + N in 3.5% NaCl are more noble than carbon steel, as they both have higher corrosion potential (Ecorr). Moreover, they exhibit lower current densities (Icorr), and thus they do not corrode as fast as plain carbon steel does. They do not also have a passive region observed in the polarization curve, as the potential continuously increases as the current increases too.Table 2
Potentiodynamic parameter values (Ecorr, Icorr) obtained for the alloyed layers.
3.5% NaCl1 N H2SO4Ecorr (mV)Icorr (A/cm2)Ecorr (mV)Icorr (A/cm2)Plain carbon steel−5243*10−6−3474*10−6TiB2−4209*10−7−1793*10−4TiB2+ N−3749*10−7−1643*10−4Similarly, the alloyed layers are nobler than steel in 1 N H2SO4 solution, as they have higher Ecorr than that of steel. The main difference between the two materials lies on their current density values that in the case of the alloyed layers seems to be a little higher than the plain steel. This fact implies that although the layers are nobler than steel, when they will begin to corrode, they will exhibit higher corrosion rates. In addition, all the tested materials do not passivate in 1 N H2SO4. A similar result was also found in the work of Munro [18] who attributed the absence of TiB2 passivation to the presence of the white film of tetravalent oxide titanium (TiO2*H2O) coming from the dissolution of TiB2.The alloyed layer TiB2 + N has slightly better corrosion behaviour than the alloyed layer TiB2, as it has higher corrosion potential values in the two tested solutions. As a matter of fact, following the corrosion experiments of both layers in 6% wt FeCl3*6H2O, the alloyed layer TiB2 + N was found again more resistant. Figures 6(a) and 6(b) present the surface of the coating TiB2, while Figures 6(c) and 6(d) present the corroded surface of the layer TiB2 + N. As it can be seen from the first two figures, layer TiB2 is totally detached from the substrate, leaving the steel substrate susceptible to corroded solutions. On the contrary, layer TiB2 + N is not totally detached from the substrate but presents cracks and corrosion signs. In fact, TiB2 particles are protruding from the matrix, which has been highly corroded (Figure 6(d)).SEI micrographs of the exposed surfaces of the alloyed layers to FeCl3 solution after corrosion experiments: (a, b) alloyed layer TiB2 and (c,d) alloyed layer TiB2 + N.
(a)(b)(c)(d)Generally speaking, the corrosion resistance of the alloyed layers is not highly improved by the TiB2 particles, because of the metallic ferritic matrix, which is considerably susceptible to pitting corrosion. This is also confirmed from the observation of the alloyed layer after corrosion experiments in the scanning electron microscope (Figure 6), where TiB2 particles are protruding from the ferritic matrix that has been consumed due to the corrosive environments. The presence of the metallic binder in the alloyed layers decreases the corrosion resistance, as it has also been studied elsewhere [19, 20].


## 3.4. Pin on Disk Wear Testing

Figure7(a) presents the wear rate of the alloyed layer TiB2 against the tool steel ball that is of the order 10−5mm3 volume loss per m of sliding distance. Increasing the sliding speed, the wear rate decreases slightly for the two applied loads, as it has also been found in another investigation [21]. At the same time, for higher applied loads, the wear rate increases. In addition, the wear rate for the tests with the Al2O3 ball, presented in Figure 7(b), is of the order of 10−4mm3 volume loss per m of sliding distance. In this case, the wear rate increases with increasing applied load, but it is not been affected by sliding speed.(a) Wear rates of the pair-alloyed layer TiB2-tool steel ball, (b) wear rates of the pair-alloyed layer TiB2-Al2O3 ball, (c) wear track for the pair-alloyed layer TiB2-tool steel ball, (d) SEM micrograph of the wear track for the pair-alloyed layer-alumina ball showing the plastic deformation of the alloyed layer and the presence of TiB2 particles protruding from the matrix.
(a)(b)(c)(d)The wear tracks after the tests with the tool steel ball are covered by a gray layer of oxide powder, Figure7(c), consisting oxygen, titanium, and iron, as this was confirmed by EDS microanalyses on the SEM. Examination of the worn surface of the tool steel ball reveals no sign of oxides or material transfer to the ball from the wear track. On the contrary, it is very clean and presents abrasion scars to the direction of movement. Moreover, for the pair, alloyed layer-Al2O3 ball, there is no sign of an oxide layer formed or material stack on the surface of the track. The matrix present deep scars and abrasive marks, while TiB2 particles are protruding from the matrix, Figure 7(d). The worn surface of the Al2O3 ball is partially covered with a black powder, apparently steel debris stack on the ball, and it has hills on its surface that act as cutting points for the alloyed layer. The high hardness of the alumina compared to the relative softer matrix of the alloyed layer favors the cutting action.The friction coefficient for the pair, alloyed layer TiB2-steel, was measured throughout the experiments and very stably attained the value of 0.12±0.01. This is a very low friction coefficient compared with that found elsewhere [11]. The oxide layer found on the surface of the wear tracks in combination with the decrease of the wear rate with increasing sliding speed and the low friction coefficient dominating the coating may be attributed leads to an active oxidation mechanism [22, 23]. On the contrary, the friction coefficient for the pair, alloyed layer TiB2-alumina ball, is 0.59±0.05 and is considerably higher than the one measured for the couple alloyed layer-tool steel. A similar friction coefficient was found in another work [24].The wear rate of the pair, alloyed layer TiB2 + N-tool steel ball, is presented in Figure 8(a). As it can be seen, the wear rate is of the order of 10−4mm3 volume loss per m of sliding distance, while it increases for higher applied loads and sliding speed values. The wear tracks after the tests exhibit plastic deformation and the presence of an oxide layer, while some areas have been removed from the alloyed layer. This removed material has been stuck on the steel ball, as according to EDS microanalyses on the SEM, oxygen, titanium, and iron found on the balls. Similarly, the wear rate of the pair, alloyed layer TiB2 + N—Al2O3 ball, presented in Figure 8(b), are again of the order of 10−4mm3 volume loss per m of sliding distance. As it can be seen, increasing applied load and increasing sliding speed result in increasing wear rate. The wear tracks after the tests present signs of oxide, Figure 8(c), and severe plastic deformation, Figure 8(d). The wear spot of the Al2O3 ball is partially covered with steel debris.(a) Wear track for the pair alloyed layer TiB2 + N-tool steel ball, (b) wear track for the pair alloyed layer TiB2 + N-alumina ball, (c) wear track for the pair alloyed layer TiB2-tool steel ball, (d) SEM micrograph of the wear track for the pair alloyed layer-alumina ball showing the plastic deformation of the alloyed layer and the presence of TiB2 particles protruding from the matrix.
(a)(b)(c)(d)The friction coefficient measured throughout almost all the experiments with tool steel ball was not stable. The plastic deformation in combination with material transfer from the alloyed layer to the ball leads to a relatively high friction coefficient (between 0.45 and 0.6). Similarly, for the pair layer-alumina, the friction coefficient did not remain stable and was fluctuated between the values measured for the couple alloyed layer-tool steel.Comparing the two different tribosystems for the alloyer layer TiB2, it can be postulated that the wear performance of the TiB2 MMC depends on the counterbody, since both wear mechanism and friction coefficient are quite different. The alumina ball, as it is harder than the steel ball, causes more damage to the alloyed layer but also alters the wear mechanism involved leading to higher friction coefficient. On the contrary, comparing the two different tribosystems for the alloyed layer TiB2 + N, it gets the conclusion that the wear performance of the nitrogen-rich TiB2 MMC is characterized by plastic deformation and formation of oxides for both tribosystems. Especially for the alloyed layer—tool steel system, the alloyed layer in every test condition underwent plastic deformation with detachment of material transferred and stuck to the ball surface.


## 4. Conclusions

(i)
Through a nitrogen-rich plasma and shielded gas of the Plasma Transferred Arc technique, alloyed layers enriched in nitrogen can be produced. Moreover, the PTA alloying technique can produce metal matrix composites with TiB2 as reinforcing material.(ii)
Both alloyed layers produced, TiB2 and TiB2 + N, are uniform, without cracks, and have a thickness of about 1 mm.(iii)
The microstructures obtained consist of primary titanium diboride particles in an eutectic mixture of iron and eutectic boride particles. Titanium carbonitrides are also present in both alloyed layers with Ar or Ar + 5% N2. In the first layer, carbon comes from the substrate, while carbon and nitrogen are impurities of the titanium diboride powder used in the process. In the second layer, carbon also originates from the substrate, and nitrogen mainly from the N2 of the plasma and shielded gases.(iv)
Both alloyed layers are susceptible to pitting corrosion in 3.5% NaCl and 1 N H2SO4. The alloyed layers produced with mixture of Ar + 5% N2 are slightly more noble than the one produced with pure Ar.(v)
The corrosion resistance of the alloyed layers in 6% wt FeCl3*6H2O is not highly improved by TiB2 particles, because of the metallic-ferritic matrix, which is considerably susceptible to corrosion.(vi)
The wear rate of the coupling alloyed layer TiB2-tool steel is of the order of 10−5mm3/m, while for the coupling alloyed layer-alumina is of the order of 10−4mm3/m. On the contrary, the wear rate of the coupling alloyed layer TiB2 + N-tool steel or alumina is of the order of 10−4mm3/m.(vii)
The wear mechanism observed for the alloyed layer TiB2 against tool steel or alumina ball is different, although they are tested under the same conditions. On the other hand, the wear mechanism of the alloyed layer TiB2 + N against a tool steel or an alumina ball is similar.(viii)
Under the wear conditions examined here alloyed layers undergo severe plastic deformation with, in some cases, detachment of material from the surface that transfers and stick on the ball surface. In addition, for the tribosystem TiB2 alloyed layer against tool steel, there is evidence of an active oxidation mechanism, which leads to decrease in wear rate and low-friction coefficient.



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*Source: 898650-2012-03-21.xml*