Roller cone bits, second only to polycrystalline diamond compact (PCD) bits, are currently the primary tool used in the drilling industry. They are made of three interconnected segments, named lugs or arms, which constitute the bit body. At the end of each of them is a rotating cone on a bearing journal. Due to the types of bearings, roller cone bits are divided into those with roller or friction bearings, sealed or unsealed. Each cone has a few rows of cutting elements (milled teeth or TC inserts, see Figure 1) designed to drill the rock. The degrees of hardness of cutting structures on bits are designed according to the International Association of Drilling Contractors (IADC) code for different formations. Bits with teeth work together to drill the rock formations and, at the same time, clean each other of the spoil. Inside the segments, channels end with nozzles, supplying the drilling fluid. The central nozzle is designed to bring the drilling fluid to the bottom of the hole, and the nozzles around the perimeter ensure the cleaning and cooling of the bearings. Due to the flushing system, the following types can be identified: center (1 nozzle), 3-jet (3 nozzles), and multi-jet flushing system (4 nozzles) [1, 2]. In this article, the authors focus on the material aspects of roller cone bites with milled teeth.
Types of roller cone bits: (a) milled-tooth bits, (b) insert-tooth bits – Glinik Drilling Tools product catalog [2]
The roller cone bits excavate the rock formation in two ways. Strong bit loading forces press the teethes or inserts into the rock and crush it. Rotation speed and torque drive the bit around the vertical axis, which drives the cones to rotate around their axis (slightly angled to the axis of bit rotation). This causes the cutting elements to exert a lateral force on the rock and shear its fragments [1, 3, 4].
The effective life of a roller cone bit is affected by the following factors: the construction parameters of bits (e.g., the shape and size of the teeth and their arrangement), type of drilling rocks (geomechanical properties), drilling parameters (e.g., weight on bit (WOB), rotary per minute (RPM), total bit revolutions (kRev), flow rate of mud), and properties of the materials from which its elements are made [5–7]. Bearing and teeth failures are the most common causes of shortened drill bit life [8, 9]. Many authors have examined the wear of roller cone bit teeth [3, 5–10]. Larsen-Basse [10] concluded that the main mechanisms are impact fracturing, mechanical fatigue due to overloads, abrasion wear, and thermal fatigue. Further research shows that the primary type of abrasion wear in a soft rock formation is caused by ploughing and, in hard formation, by micro-ploughing and microcutting [5]. During drilling, the bit material heats up in contact with the rock and then cools down with the drilling fluid contact. As a result of the differences in thermal properties (coefficients of expansion) of the carbide coating and the tooth core, microcracks can be formed, which results in the penetration of the dispersed medium, which contains erosive particles, and further degradation of the material. However, this wear mechanism and mechanical fatigue due to overloads can be minimized by adequately selecting the drilling regime and drilling fluid flow [3, 7].
As mentioned above, the material’s properties are one factor that influences the effective life of a roller cone. The companies manufacturing them do not make the materials used to produce the bits and their chemical compositions public. On the basis of the study of damaged drills, however, it can be concluded that the teeth of the bits consist of three layers: an outer hard-facing layer containing tungsten carbides in a steel or nickel matrix, a second layer of high-carbon martensitic steel, and a third layer (tooth core) of low-carbon martensitic steel [5, 7, 11]. Due to the specificity of the drill work, it is essential that the bit material is characterized by both wear resistance and chipping resistance. During the production of the material, it is crucial to find the trade-off between these two parameters. Many metal matrix composites (MMC) were tested. The typical composite material consists of hard tungsten carbides providing wear resistance and a soft matrix (usually Fe-, Ni-, and Co-based alloy) that improves ductility and impact strength. It is characterized by excellent chemical and mechanical properties such as hardness, resistance to cracking, and abrasive wear. The low price and high performance of Fe-based, self-fluxing alloy result in their being widely used [12]. Currently in the research spotlight are WC-Ni systems, which seem to exhibit the best performance in cutting tool production. A typical hardfacing nickel matrix contains silicon, boron, and sometimes chromium. The alloying elements are added to lower the melting point and reduce the dissolution of the strengthening phase but also to reinforce the matrix. The creation of nickel borides and nickel silicides improves wear resistance. The currently most commonly used strengthening phase is cemented carbide composed of tungsten carbide and cobalt (WC-Co). Cobalt increases the wettability of the tungsten carbide particles, which improves their binding. Among all hard phases in carbides, the most significant is hexagonal tungsten monocarbid (WC), but tungsten dicarbid (W2C) is also used. Several types of tungsten carbides, depending on the manufacturing technique, the type of carbide, the WC/W2C ratio, and resulting properties can be indicated, e.g., fused and crushed tungsten ratio (FTC), spherical tungsten carbides (SCC), macrocrystalline tungsten carbide (MTC) [13–19].
The protective layer is applied not only to protect the cutting structure but also to protect the diameter of the bit. For that, the teeth in the last row and the back of the arm are additionally strengthened. In addition to the surfacing, carbide inserts are also used as reinforcement. Both types of reinforcement are shown in Figure 2. Although there is much data in the literature on manufacturing layers using modern methods such as laser deposition commercially, gas deposition is still predominantly used. Recently, plasma deposition has been gaining attention, mainly due to the reproducibility of the process and the possibility of automation. However, there are still problems with the selection of parameters in the case of small tool diameters and complex tool geometries. The impact of the production processes on the microstructure of the layer and the resulting properties is significant because it directly affects the quality of the bit and its service life.
Different types of teeth and arms reinforcements [2]. The arrows mark the locations of the overlays
The motivation to undertake this research was the lack of studies on the properties of overlays on commercial products applied to cones by various methods. A wide range of materials for drilling tools was tested under optimal laboratory conditions [16, 18–21]. There is little updated research on the material aspects of roller cone bits, which has mainly focused on failure analysis or causes of wear [5, 7, 11, 22]. The research aim was to compare the microstructure and mechanical properties of overlays made by gas weld surfacing and plasma transferred arc (PTA) welding to evaluate their application on roller cone bits. The assessment criteria were hardness, impact strength, and abrasion resistance.
The tests were carried out on samples provided by Glinik Drilling Tools. The rectangular samples (Figure 3) were prepared using commercial materials by gas welding and plasma transferred arc (PTA) welding methods. Depending on the characteristics of the method, rod and powder were used to produce the overlay, respectively. The exact chemical composition and manufacturing parameters are company “know-how” and therefore proprietary. All samples were heat treated after welding, which included carburizing, hardening, and tempering. The exact heat treatment parameters are proprietary information. On the delivered samples, metallographic sections were made and subjected to microstructural analysis. Mechanical properties were evaluated.
The samples submitted for testing by Glinik Drilling Tool: (a) gas welding; (b) plasma transferred arc welding
Microscopic observations of the samples were carried out using Nikon Epiphot and Kayence VHX200 light microscopes. The samples were observed without and with etching with Murakami’s reagent. The study aimed to observe the obtained layer and analyze the material’s structure and defects.
Photos of the analyzed layers were taken using a Keyence VHX600 microscope, which was then binarized using the Met-Ilo program to determine the volume fraction of WC. The images obtained were analyzed in the Micrometer program, which allows for determining the volume fraction and particle size distribution.
Microscopic observations were made using the scanning electron microscope SU 8000 by Hitachi. Observations were made in the magnification range from 30 to 50000. The accelerating voltage of the electrons was set at 5–30 kV. The observations were made using the secondary electron (SE) and back-scattered electron (BSE) detector. Microanalysis of the chemical composition of the samples, including qualitative and quantitative analysis, was determined using an energy-dispersive spectrometer (EDS) by ThermoFisher.
The phase composition was determined using a Bruker D8 Discover x-ray diffractometer working in a point beam geometry with a 1.5-mm collimator, using non-monochromatic CoK
Microhardness tests using the Vickers method were performed on the Falkon500 device, according to the PN-EN ISO 6507-1 standard “Microhardness tests.” Measurements were made in the overlay area and the base material.
The impact test was carried out on a Charpy SUNPOC JB300B impact hammer with an initial energy of 300 J, following the requirements of PN-EN ISO 148-1:2010. The tests were performed at room temperature on five specimens from each series. Samples with a U-shaped notch on the opposite side of the surfacing were used. Because the specimens were not identical, and the surfacing was only a tiny part of the specimen cross-section, these results cannot be considered conclusive. Still, they can be used for comparison purposes between the two series.
Following ASTM G 6-00, Procedure A, Abrasion tests were conducted under laboratory conditions. For each combination, tests were carried out in five repetitions. In addition, tests were performed on three samples of Hardox 450 steel, which was the reference material. Each sample was ground to obtain flatness and straightness of the surface. The abrasive wheel made 6,000 revolutions during the test, and the abrasive flow rate (A. F. S. testing Stand 50-70 sand) was 335 g/min. To determine weight loss, samples were weighed to the accuracy of 0.0001 g before and after the tests. The average density of the overlays was determined using a WAX 60/220 RADWAG laboratory balance based on measurements of samples weighed in air and demineralized water. Volumetric weight loss (mm3) was calculated as the weight loss ratio to density. The results were compared to the abrasive wear resistance of Hardrox 450 steel by determining the relative abrasive wear resistance of the metal-mineral type of surfaced layers.
The cross-section of the overlay made by gas welding is shown in Figure 4. The overlay thickness was from 22 to 25 mm. The consistent and uniform microstructure of the layer proves the good weldability of the material. Microscopic observations did not reveal the presence of discontinuities such as pores or cracks throughout the overlay. However, the dissolution of tungsten carbide particles is observed in the bottom part of the overlay, which is clearly visible during mapping analyses (Figure 5). The basic material used by the Glinik Drilling Tools company is a gas surfacing rod, which, as the manufacturer declares, consists of a steel tube filled with a mixture of WC and Si-Mn alloy. This information is consistent with the chemical composition analyses performed.
Cross-section of the coating made by the gas weld surfacing
Mapping of key elements of the gas weld surfacing layer
Spherical and polyhedral particles are visible inside, with a 50.7% and 4.7% volume fraction, respectively. The diameter of the spherical particles was in the range of 400 to 600 μm. The different microstructures of particles are demonstrated in Figure 6. The spherical particles are characterized by typical features of cermet with well-bonded prismatic WC grains and Co matrix [18, 19].
Spherical and polyhedral particles in the gas weld surfacing
EDS analysis (Figure 7, Table 1) was used to characterize the particles observed. It showed that both contain predominant amounts of tungsten, iron, and carbon. Polyhedral and spherical particles differ in that the first also contains nickel and is richer in iron (spots 1 and 3), and in the second (spots 2 and 4), cobalt is also detected.
SEM micrographs of overlay made by gas welding surface with EDS spot analysis
EDS spot analysis of the areas in Figure 7 (weight %)
C-K | Fe-K | Ni-K | Co-L | W-M | |
---|---|---|---|---|---|
2.2 | 2.6 | 0.8 | 94.4 | ||
3.5 | 1.6 | 0.2 | 94.7 | ||
1.8 | 3.5 | 0.3 | 94.4 | ||
2.9 | 2.2 | 0.6 | 94.3 |
The cross-section of the overlay made by PTA is shown in Figure 8. The PTA overlay’s thickness was lower than that made by gas welding and amounted to 15–17 mm. Similarly, the coating was well bonded with the steel base and uniform without defects like microcracks or pores. The main particles had spherical shapes; however, their concentration was lower in some parts of the overlay. Comparably to the previous overlay, the volume fraction of the strengthening phase was 55%. The particles were finer, however, and their diameter was about 120 μm. The distribution of primary elements in the whole was similar to the gas-welded overlay (Figure 9). According to the company, the powder used to make overlay by PTA methods contains WC and nickel alloy as a matrix, which is in line with mapping and EDS results (Figure 9). The enrichment of iron observed in the fusion zone may be caused by the diffusion of the element during the surfacing process; similar results were observed by Li et al. [23].
Cross-section of the coating made by the PTA weld surfacing
Mapping of key elements of the PTA weld surfacing layer
Microstructure analysis using a scanning electron microscope revealed two morphological zones in the padding weld, differing microstructure elements caused by the coating application process, and the parameters used (Figure 10). The first zone is the fusion zone of the surfacing with the base material. The surfacing adheres tightly to the base material. Visible deformations can be caused by the impact of hard particles on the substrate material during the process. In the matrix, the eutectics are clearly visible. In zone two, carbides are seen in the dendrites’ nickel matrix. In each zone, secondary carbides are visible, mainly formed around the primary ones. Other authors observed similar microstructures in a study of materials strengthened with WC particles [24–26]. The dendritic structures with motile, floral, star-shaped, and blockshaped carbides were formed by the melting of tungsten carbide particles during the surfacing process. The formation or not of dendritic structures in the matrix depended on the parameters of the layering process [23]. A detailed study on the microstructure analysis of Ni-WC surfaced layers using transmission electron microscopy (TEM) was carried out by Liyanage and coauthors [26]. A Ni-base matrix composed of a eutectic mixture of dendrites and interdendritic, identified as
The microstructure of the coating is made by PTA weld surfacing with the distinction of three zones occurring in the layer
EDS analyses of blocky-shaped structures (Figure 11, Table 2) also confirmed the partial dissolution of the tungsten carbides and formation of transition phases between the matrix and the reinforcing particle, in agreement with the literature [16, 18, 20, 26]. Inside the spherical particles, only tungsten and carbide were detected. The
SEM micrographs of overlay made by PTA surface with EDS spot analysis
Results of XRD analyses on sample cross-section made by gas weld surfacing
Results of XRD analyses on sample cross-section made by PTA
EDS spot analysis of the areas in Figure 11(weight %)
C-K | Cr-K | Fe-K | Ni-K | W-L | |
---|---|---|---|---|---|
6.6 | 0.3 | 1.5 | 18.4 | 73.2 | |
3.6 | 0.2 | 0.9 | 13.8 | 81.6 | |
5.9 | 0.2 | 0.7 | 8.8 | 84.5 | |
4.3 | 0.2 | 0.9 | 12.6 | 81.9 | |
3.8 | 0.3 | 1.1 | 14.9 | 79.9 | |
3.7 | 0.2 | 0.9 | 16.0 | 79.2 | |
5.4 | 0.1 | 94.3 | |||
5.4 | 0.2 | 88.9 |
The results of the microhardness tests are shown in Table 3 and Figures 14 and 15. The impressions were made in both the base and the surfacing, taking 0 points as the joint. In the sample made by gas welding, both the base and matrix of the surfacing exhibited higher hardness compared to the sample made using the PTA method. An inverse correlation was observed for the strengthening phase. In both cases, the hardness of the coating matrix was about twice that of the steel base material. Changes in matrix microhardness are related to the dissolution of the tungsten carbides and the formation of secondary carbides during surfacing. Similar results were observed by Maroli and Dizdar [20] and Czupryński [21]. The microhardness tests showed that structures identified as secondary carbides show lower hardness than tungsten carbides, but higher hardness than the matrix. It confirms the data in the literature about the hardness of secondary eta carbides [18]. The tungsten carbides also showed a high range of variability. Garcia-Ayala et al. [19] pointed out that the hardness, and consequently the toughness of tungsten carbides, is a function of the average WC grain size and content of Co. The finer grains and lower Co content increase hardness. The highest hardness shows carbides with ultrafine grains amounted to 0.2–0.5 μm. On this basis, it can be concluded that the strengthening phase used in plasma surfacing has a finer structure and/or lower Co content. Yang et al. [32] pointed out that an increase in microhardness positively correlates with the material’s wear resistance and negatively with the resistance to brittle fracture.
HV 0.1 microhardness measurements
Basis (steel) | Matrix | Strengthening phase | |
---|---|---|---|
567.0 | 1028.2 | 1699.8 | |
23.6 | 60.6 | 245.4 | |
352.6 | 714.2 | 3707.6 | |
26.7 | 162.4 | 237.2 |
Microhardness distribution on sample cross-section made by gas weld surfacing (0mm-joint)
Microhardness distribution on sample cross-section made by PTA weld surfacing (0mm-joint)
The impact test results are shown in Figure 16. It is worth noting that these results can only be used to compare series (explanation in section 2.2.6.
Comparison of the impact test results of samples made by Gas welding and PTA
The comparison of relative abrasion resistance of the analysis series is shown in Figure 17. Overlay made by the PTA method characterized two times better abrasive wear resistance than series produced by gas welding. The abrasive wear of welding overlays depends on several structural factors, for example, the tungsten carbides’ amount, shape, and distribution. However, there is a maximum content for the reinforcement phase (depending on the welding methods and matrix phase), above which there are problems with aggregation and bonding with the matrix. There is also a significant influence on the degree of dissolution of the WC, which depends on the matrix’s chemical composition and the welding process parameters [12, 16, 20, 33, 34]. The higher wear resistance correlates with higher WC content and finer particles. As with impact strength, the presence of the eta phase contributes to the deterioration of wear resistance.
Comparison of the relative abrasion resistance of samples made by gas welding and PTA
In summary, the plasma-generated surfacing was characterized by a more homogeneous structure and higher fragmentation of the reinforcing phase compared to the gas-generated coating. In addition, two types of tungsten carbide, WC and W2C, were identified in the PTA-generated surfacing. Complete elimination of dissolution cannot be possible, but its minimization would significantly improve material properties. The occurrence of secondary carbides was observed in both of the coatings. The formation of secondary carbides may also be related to the elements’ heat treatment after surfacing to improve the base material, which should be further investigated. The microstructure of the surfacing affects its mechanical properties. In terms of usability, the PTA-generated surfacing was found to be better. It was characterized by a lower hardness of both the substrate and the overlay matrix, but a higher hardness of the reinforcing phase. The study showed that it exhibited higher impact strength and abrasion resistance than the surfacing produced by the gas method. Using the PTA method and modifying the material composition has brought many advantages, both in the process’s automation and the obtained properties. Nevertheless, the observed imperfections, such as the lack of homogeneity of the reinforcing phase distribution, the partial dissolution of primary carbides, and the formation of brittle secondary carbides, leave room for even more significant improvement in the materials produced.