Tool wear development in gear skiving process of quenched and tempered internal gears

Gear skiving is a highly productive machining process, especially for manufacturing of high strength internal gears as required for high performance electric drive trains. However, the complex process kinematics cause intense variations of the effective cutting parameters during tool engagement. Thus, particularly the tool must meet high requirements to achieve long tool life at required workpiece quality. These requirements are ampliﬁed even more when machining quenched and tempered materials from the massive blank. In the presented study, the inﬂuence of various key factors on the tool wear development in gear skiving process are quantiﬁed. In several tests, the cutting speed, workpiece tensile strength, cooling lubricant strategy, as well as the cutting strategy are varied in order to optimize tool life. Therefore, single-tooth tests on quenched and tempered internal gears from 31CrMoV9 (AISI 4340) steel are conducted and wear ﬂank land width evolution of the tools is examined. In addition, the workpiece is evaluated with regard to surface quality. Results reveal that different factor level combinations can have various effects on tool wear characteristics and therefore on tool life. The correlations presented provide recommendations for practical application and contribute to deeper process understanding.


Introduction
The highly productive gear skiving process is suitable for manufacturing high-quality internal gears required for planetary gearboxes in electric vehicles [1]. Although the process was patented over 100 years ago, setting economical tool life is still a major challenge in some applications. Intense variations of the effective cutting parameters during tool engagement are caused by the complex process kinematics. Negative rake angles and small clearance angles are typical for the process and often lead to small stable process windows [2]. Therefore, in contrast to other machining processes such as milling, special attention must be paid to those angles. Jansen used uncoated high speed steel tools and cooling lubricant in a gear skiving process to machine internal gears with a tensile strength up to Rm = 980 MPa [3]. Tool life increases by a factor of 3 to 5 by reducing cutting speed by 50%. The tool life of tungsten carbide can exceed that of high speed steel by a factor of 6 [4]. Compared to conventional AlTiN based coatings, an AlCrN coating performs with better adhesion and tool life [5]. Reducing the tensile strength of the workpieces by 15% increases tool life by a factor of 2 to 3. In general, these tendencies are also accepted for other processes with intermittent cut, e.g. gear hobbing [6]. Process strategies with multiple radial infeeds are also beneficial for tool life [2]. In a theoretical study, Guo et al. demonstrate, that the load distribution on the cutting edge and therefore the wear distribution is additionally depending on the cutting strategy [7]. For example, a combination of radial infeed and rotational offset can lead to high local loads being equalized along the cutting edge. According to Stadtfeld, tool life of coated carbide tools can be extended by omitting cooling lubricant in gear skiving [8]. He assumes, that this is caused by the increased process heat, which decreases the material resistance against deformation in the shear zone.
However, a systematic investigation on tool life of coated carbide tools in dry gear skiving process of high strength materials is absent. This study aims to show the potential of dry gear skiving with carbide tools in comparison to gear skiving with oil lubrication. Therefore, cutting speed and tensile strength of the workpieces are varied. Tool life and surface quality of the manufactured workpieces are targeted. In addition, two alternative process strategies are tried, which are developed based on experimental and theoretical process analysis.

Materials and methods
The experimental procedure and parameters including workpiece, tool and process correspond directly to the experiments of a previous study at wbk Institute of Production Science, where internal gears made of quenched and tempered steel 31CrMoV9 (AISI 4340) were machined from the massive blank with the use of oil lubricant [5]. This methodology was chosen in order to be able to compare the results directly. The tests were conducted on a skiving machine based on the customized vertical lathe type INDEX V300Sonder [9]. Similar to the previous study [5], the established analogous tool setup with a singletoothed cutting insert was used for the experiments, which allows to map the tool wear evolution at highly reduced workpiece quantity and tool costs [4]. The experimental setup is presented in Fig. 1. As the longest tool life was achieved with carbide tools K30 with AlCrN coating in previous experiments [5], this combination was used in this study. Workpiece, tool and process data are listed in Table 1. Experiments marked with "dry machining" have been conducted without the use of fluid cooling lubricant but with pressurized air to ensure proper chip removal.
To estimate the tensile strength Rm of the quenched and tempered workpieces, the Vickers hardness was measured on the surface and converted according to DIN EN ISO 18265 [10], see Table 2. Tool wear was measured optically with a light microscope of type Zeiss Stemi SV11 in combination with the software Zeiss Axiovision. For this purpose, pictures were taken from six specified positions of the dismounted cutting inserts representing its actual condition, see Fig. 2. In accordance to previous experiments, a maximum wear flank land width of VBmax = 60 µm was chosen as wear criteria, as the carbide inserts presented rapidly progressing breakage beyond this point [5]. The rake faces of the inserts were also examined using a Nanofocus confocal microscope and µsoft software analysis. The flank roughness of the manufactured workpieces was quantified by of Mahr MarSurf XCR 20. Parts machined by worn tools were measured before the wear criterion was exceeded.
The local process parameters are assessed with the help of geometric penetration calculation implemented in a cross-process simulation environment at wbk Institute for Production Science. Therefore, the process-specific kinematics are prepared in a pre-processing stage and transferred to a universal calculation core, where the local effective process parameters are determined. A detailed description of the methodology of the calculation core can be found in [11]. With the help of the simulation environment, two alternative process strategies were developed in order to analyze the influence of changes in local cutting parameters on the appearing wear phenomena, see Fig. 3 and Table 3. Strategy A was applied in the previous experiments [5], which is why it is used as reference. In process design, the maximum cutting thickness at the tool tip were kept in a range of 0.09 mm < hmax < 0.12 mm for all tool passes, which is why the axial feed sax increases with the tool pass, see Table 3. Strategies B and C are alternatives evaluated only in single experiments. Their theoretical background is descripted in Sect. 3. In contrast to strategy B, strategy C is tested at higher tensile strength due to limited workpieces of each batch.  Crater wear is typical for high speed steel tools and seldom described for carbides. However, crater wear has been observed in dry gear hobbing with AlCrN-coated carbide tools [6]. But the crater wear and fractures occurred at significantly increased cutting speeds (vc > 600 m/min), while abrasive wear was the dominating mechanism for more conservative process parameters. The fact that crater wear occurs at medium cutting speeds in gear skiving raises the question which conditions lead to the heavily increased tool loads in this process. A possible explanation for the differences in the dominant tool wear mechanism comparing dry and wet processes is the strong heating of the cutting edge during tool engagement. According to Stadtfeld, the increased process heat decreases the resistance against deformation of the chip in the shear zone [8]. As known from milling, this temperature dependent softening effect reduces cutting forces and thus tool load [12]. Besides the higher temperatures in the shear zone, the tool as a whole also reaches higher temperatures. Simultaneously, the tool is not cooled down by the cooling lubricant at high rates between tool engagements. This leads to smaller temperature gradients and therefore to lower thermomechanical stress in the tool. This helps to avoid cracks or at least slows down propagation. The softening effect and the effect of lower thermomechanical stresses probably appear in combination. However, there is currently no indication which of them is the dominant one. Analysis of the motor spindle power seem to support decreasing forces but still remain inconclusive. In effect, further investigations will have to be undertaken to definitively explain the dominant mechanisms.
Longest tool life is achieved when workpieces of lower strength are machined dry at a cutting speed of vc = 140 m/min, see Fig. 4. Here, tool life is limited by the wear on the trailing flank (TF). For this reason, strategy B is designed to relieve the TF by combining radial infeed with rotational offset, as proposed by Guo et al. [7]. Thus, the leading flank (LF) is mainly cutting in case of strategy B, see Fig. 6b. While the maximum chip thickness hmax at the tool tip T is kept constant, it slightly increases on the LF, see Fig. 6a. The minimum rake angle γmin decreases a bit in this area, see Fig. 6b. The minimum clearance angles αmin are almost not affected and locally drop below zero at the transition area between flank and tip (positions TT and LT, see Fig. 6c). As negative clearance angles indicate collision and are therefore critical for tool wear, strategy C is designed to ensure positive clearance angles. Unfortunately, due to the given tool geometry, this can only be achieved in conjunction with strongly decreased minimal rake angles at the tool tip T and on the LF.
Tool life before exceeding the wear criteria is compared for different cooling strategies, workpiece strength, cutting speeds and process strategies, see Fig. 7. As expected, tool life is generally exceeded when dry machining workpieces with lower tensile strength. Reducing the strength by 15% K Fig. 4 Tool wear evolution for machining with a cutting speed of vc = 140 m/min in wet and dry condition with process strategy A. Data regarding oil lubrication is taken from [5] resulted in an increase of the tool life by a factor of 3 to 6. This means that the benefit is even greater than in the wet process, where a factor of 2 to 3 was obtained [5]. In accordance with the literature, for machining with oil lubrication, tool life increases steadily with decreasing cutting speeds [3]. However, this is not the case for dry machining in the interval of 120 m/min < vc < 140 m/min. Here, tool life increases with increasing cutting speed, see Fig. 7. The tendency is clear only for the lower strength. Again the softening effect would be an acceptable explanation, as rising cutting speeds lead to rising temperatures and therefore, to decreasing cutting forces [12]. In this way, local tool life optima in dry gear hobbing have been explained [13].  can be confirmed [7]. However, increasing the maximum chip thickness and decreasing the minimal rake angle on the LF did not only add strain here. In particular, the slope of wear development at the tool tip T rises considerably, although the main local process parameters did not change much at this point, see Fig. 6.
As the profiles of the main process parameters shown in Fig. 6 are composed of extreme values, changes in the characteristics of single tool passes cannot be determined from them. Detailed analysis reveals, that the maximum chip thickness variation Δhmax between single tool passes is increased in the area of the tool tip T in case of strategy B, see Fig. 9. This may influence the wear evolution at this point.
In case of strategy C, the wear pattern observed differs considerably from that obtained from strategy A. A breakout on the LF ends the tool life, see Fig. 10a. However, even after the end of tool life, no crater wear can be detected on the rake face, but is already found for strategy A at a similar stage and half its tool life, see Fig. 10b,c. Thus, it is suggested that crater wear of carbide tools is directly related to higher but still negative minimal local rake angle in combination with negative local clearance angles, which cause collision and therefore compression of the tool.
The use of the analogous tool setup resulted in an overall good surface quality, see Fig. 11. This is caused by the ideal cutting conditions, as the analogous tool setup does not exhibit typical tool deviations like pitch errors. There is no evident advantage of wet or dry machining in terms of flank roughness when manufacturing workpieces with new tools. Also, there is almost no difference between TF and LF. Taking into account the standard deviations, the rough ness generally increases with tool wear. However, there are major differences for workpieces of lower strength manufactured with worn tools. While in general the flank roughness worsens only slightly in the wet process, the flank roughness increases by a factor of about 3 on the LF in the dry process. For the TF, the factor is a little lower. The also highly increasing standard deviations indicate more variation in machining conditions. In case of dry machining, the much longer tool life is to be taken into account when assessing the decrease in surface quality. The slight change of roughness for high strength workpieces can be explained by the short observation time. Since the tools fail abruptly with only slight formation of abrasive wear, the effect of tool wear on the surface quality of the last workpiece manufactured before tool failure is low. All workpieces were machined using strategy A. Data regarding oil lubrication is taken from [6]

Conclusions
In the present study, tool wear and surface quality of the manufactured workpieces has been investigated in dry gear skiving process. The following conclusions can be drawn: Tool life and surface quality should always be considered in combination. While there is no evident advantage of wet or dry machining when starting with new tools, a significant increase in roughness is to be expected in case of dry machining till the end of tool life. The use of lubricant only in the finishing tool pass should be tested in the future. Geometric penetration calculation is an effective method to assess and specifically manipulate local process parameter. The potential to influence the appearing wear phenomena by adapting the infeed strategy and thus rake and clearance angles was demonstrated. However, optimization of tool life and productivity requires a deep analysis of local cutting conditions in each tool pass and a balancing of the interacting relevant parameters. Significantly different wear phenomena raise the question, to what extend findings regarding tool substrate and coating can be transferred from the wet to the dry gear skiving process. Moreover, the wear mechanisms under the specific and challenging conditions of gear skiving and how they are influenced is not yet understood in detail. Thus, further research should be conducted in this area.
Funding Open Access funding enabled and organized by Projekt DEAL.
Conflict of interest T. Arndt, J. Klose, M. Gerstenmeyer and V. Schulze declare that they have no competing interests.
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