One of the main limits of productivity during cutting processes is the occurrence of regenerative chatter. Due to these self-excited vibrations, the load capacity of the machine components, the tool as well as the machine performance cannot be fully utilized. There are several methods to stabilize the milling process. One is the use of increased process damping, which results from the contact of the tool’s flank face and the workpiece. The flank wear land naturally increases the contact between tool and workpiece. However, this effect has not been used to increase productivity in milling processes. This paper investigates with experiments and numerical simulations how tool wear affects process stability in milling of aluminum and steel. Therefore slot milling and side milling tests were carried out with tools of various states of flank wear. It could be shown that increasing flank wear allows to raise the depth of cut ap up to 300% in machining aluminum and perform the machining process with a higher productivity.
Hinweise
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1 Introduction
There is a trend in the machine tool industry to increase spindle power and torque to meet the demand of higher metal removal rates and maximize the productivity of milling processes [1]. In most cases an increase of the process parameters (depth of cut ap, width of cut ae) is not limited by the performance of the machine tool, but by self-excited vibrations (chatter) above a limiting depth of cut ap,lim [2]. Decisive for these vibrations is the regenerative effect. This effect describes the occurrence of chatter due to the dynamic compliance of the milling system. The additional high loads caused by these vibrations result in significant lifetime reductions for different components of the machine tool including the cutting tool itself and also damage the workpiece surface [3]. As a result, machines are operated below their theoretical capacity limit in order to avoid chatter vibrations. Various techniques to suppress chatter in metal cutting have been investigated over the last 60 years [1]. The easiest way to avoid chatter is the selection of suitable spindle speeds and depth of cuts, which lead to a stable zone in the stability lobe diagram. Besides active damping systems and damping tool holders, other techniques for stabilizing the milling processes are for example using special tool geometries that perturb the regenerative effect [4] or using specific cutting edge geometries [5]. Tunc and Budak investigated the influence of tool geometries and cutting conditions on process stability mainly by simulations. They stated that slow cutting speeds and larger cutting edge roundings result in higher process damping and thus higher process stability [6].
The process damping effect is based on the workpiece volume indented by the tool’s flank face [7]. The damping force is caused by the indented workpiece volume from the tool’s flank face and acts in opposite direction of the vibration and therefore reduces the amplitude of the vibration [1]. Previous investigations showed that a chamfer on the flank face, manufactured by grinding, increases process damping, which reduces the vibrations significantly [1, 8]. Hence, the maximum depth of cut ap,lim could be increased significantly by a chamfer compared to conventional tools [8]. An ideal sharp cutting edge exhibits no contact between the flank face and the surface of the workpiece (Fig. 1a). With larger cutting edge roundings or a worn cutting edge, the contact surface and therefore the indented volume leads to an increase in damping force (Fig. 1b, c). This effect is used for rough milling tools by applying a chamfer to the tool to increase the possible indented volume V and optimize the process stability (Fig. 1d). However, the disadvantage is a reduced surface quality compared to unchamfered tools. Additionally, the production of the chamfer results in an increased effort during tool production especially in the quality assurance of small chamfers. The wear rate of flank wear is higher due to the smaller clearance angle of the chamfer although the cutting edge in total is more stable [9].
Fig. 1
Effect of different cutting edge geometries and worn cutting edge on intended volume and therefore on the process damping as in [6]
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Several investigations showed that a similar effect to chamfering is caused by flank wear. Munoa et al. stated that worn tools can be used to avoid chatter as the process damping increases with flank wear [1]. Ahmadi and Ismail investigated simulations of stability lobe diagrams and compared the necessary resolution of discretization when using the semi-discretization method. For simulations with worn cutting edges a higher resolution is necessary to receive accurate results [10]. Altintas et al. showed the increase of process damping with tool wear [11]. Turning experiments with stainless steel SS304 were carried out with a new tool and one with VBB = 0.08 mm flank wear. Several of the unstable cutting tests with the new tool were observed to become stable when tested with the worn tool. The stability investigations were carried out with one state of tool wear. Tyler and Schmitz explained the higher stability of worn tools with a higher process damping coefficient. In upmilling experiments and simulations they investigated an increase of this coefficient up to 31% for a cutting edge with flank wear of VB = 200 µm [12].
These investigations have in common that only one state of wear was used for the investigations and the stabilizing mechanisms of wear are simplified with an adjusted process damping coefficient. The positive effect of tool wear with regard to increased process stability has not yet been systematically investigated with continuously increasing and different states of tool wear. This paper examines for the first time systematically the effect of various states of tool wear on the process stability in milling processes. Furthermore, a comparison is made between experimental stability diagrams and stability diagrams simulated with the semi-discretization method. A simulation which is in good agreement with the related experiment offers good possibilities to vary parameters and characterize the changes for stability without the need of more extensive experiments.
2 Experimental
2.1 Stability investigations
In order to investigate the potential of tool wear for increasing productivity, stability experiments in milling were conducted as well as a stability simulations based on the semi-discretization method. The experiments were carried out on a Heller MC16 4-axis machining center. A three-component dynamometer Kistler 9257B was used to measure the process forces. Two different processes were analyzed in terms of stability. One process was the milling of Al7075 with a tensile strength of Rm = 525 N/mm2. The other process was milling of quenched/tempered low-alloy steel AISI 4140+QT with a tensile strength of Rm = 886 − 935 N/mm2.
2.1.1 Milling of Al7075 with solid carbide end mills
Figure 2 shows the experimental setup. Because of the low wear rate while machining Al7075 the depth of cut could be increased step by step every 100 mm and the tool wear between the steps could be neglected.
Fig. 2
Experimental setup for stability investigations of milling Al7075
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The modal input parameters mass, stiffness and damping, which are necessary for the stability calculations, were determined by the impulse hammer method. The resulting frequency response functions (FRF) are shown in Fig. 3. The main compliance of the workpiece in milling Al7075 is at 500 Hz for both x- and y-direction. The compliance of the tool has two peaks, one at 1,625 Hz and one at 3,415 Hz.
Fig. 3
FRF of workpiece and tool from milling process Al7075
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By comparing the amplitudes of the FRF’s it can be seen that the workpiece is slightly more rigid with a compliance of 0.25 µm/N in x-direction and 0.4 µm/N in y-direction. The tool has a compliance of 0.6 µm/N in x-direction and 0.4 µm/N in y-direction (Fig. 3).
Aluminum was machined without coolant with uncoated, polished solid carbide end mills (Table 1).
Table 1
Tool geometry of solid carbide end mill
Diameter D
16 mm
Number of teeth Nt
3
Corner radius rε
1 mm
Rake angle γ
10
Clearance angle α
10
Helix angle δ
39; 40; 41°
Feed per tooth fz
0.1 mm
To investigate the stability in milling Al7075, slot milling was carried out with a constant depth of cut at each specimen. The depth of cut was increased in discrete steps until chatter was noticed in the force measurements of feed force, feed normal force and the machined surface quality (Fig. 4). The spindle speed was varied between n = 10,000–22,000 min−1 in steps of 2000 min−1. The max. cutting speed is with vc = 1.100 m/min still below the limit of high speed cutting. The depth of cut was varied between ap = 2–7 mm in steps of 1 mm. To show differences between various wear conditions, new tools (VB = 0 µm) as well as tools with defined width of flank wear (VB = 15 µm, VB = 30 µm, VB = 90 µm) were used. The flank wear was defined by using an optical topography measurement system based on focus variation Alicona Infinite Focus G5. Based on the force measurements and the machined surface quality, chatter vibrations and the maximum depth of cut can be determined. Figure 4 shows one example from the experiments with Al7075.
Fig. 4
Determination of chatter when machining Al7075
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At the top of Fig. 4 the surface quality of the machined specimen is shown. For the unstable process chatter marks can be clearly detected. Additionally the force measurements in time and frequency domain are shown. When the process becomes unstable, the force amplitude increases significantly and chatter vibrations can be detected. The force measurements in frequency domain are described in a spectrogram, where the force frequency is plotted over time and the force amplitude is displayed by color. In this spectrogram the tooth engagement frequency and the natural frequencies of the tool can be differentiated from the chatter frequencies.
2.1.2 Milling of AISI 4140+QT with a long cantilevered indexable insert mill
Figure 5 shows the experimental setup. Because of the higher wear rate while machining AISI 4140+QT a different setup was used where special workpieces with ap-ramps were machined. With these workpieces it was possible to investigate various depths of cut in one milling path and determine the maximum depth of cut.
Fig. 5
Experimental setup for stability investigations of milling AISI 4140+QT
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The resulting frequency response functions (FRF) of the modal analysis for milling steel are shown in Fig. 6. The compliances in milling AISI 4140+QT are characterized by one main peak at 1000 Hz for the tool and the workpiece in x- and y-direction (Fig. 6). For this setup the workpiece is more rigid with a compliance of 0.06 µm/N compared to the tool with a compliance of 4 µm/N. This shows that the tool has the highest impact for the stability of the steel milling process. On the one hand it is because of the length of the tool. On the other hand the tool-body consisting of steel in contrast to cemented carbide for the monolithic tool also has an effect on rigidity.
Fig. 6
FRF of workpiece and tool from milling process AISI 4140+QT
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Steel was machined without coolant with a long (188 mm) cantilevered indexable insert milling cutter with coated (Al2O3) solid carbide inserts (Table 2). The long milling cutter was used to investigate the potential of tool wear in compliant milling processes.
Table 2
Tool geometry of indexable insert milling cutter
Diameter D
20 mm
Number of teeth Nt
2
Corner radius rε
0.8 mm
Rake angle γ
11
Clearance angle α
9
Helix angle δ
12
Feed per tooth fz
0.08 mm
To investigate the stability in the milling AISI 4140+QT process, side milling was carried out due to the low stiffness of the long cantilevered end mill. The spindle speed was varied between n = 1,300–5,500 min−1 in steps of 700 min−1. Because of the low stiffness of the end mill a low width of cut ae = 2 mm was chosen. Due to the faster wear during dry steel machining, the depth of cut was continuously varied by machining ap-ramps with a gradient of 3 mm on 100 mm workpiece length. Special workpieces were prepared, with which the cutting depth varied from ap = 0–6 mm. The depth of cut, where chattering occurs was determined by force measurements and analysis of the machined surface (Fig. 7) analogous to Fig. 4. For this process, new inserts and inserts with defined flank wear width (VB = 10 µm, VB = 30 µm, VB = 50 µm) were used. The tests were repeated once.
Fig. 7
Determination of chatter when machining AISI 4140+QT
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2.2 Tool wear
Before the stability experiments with defined worn tools could be performed, it was necessary to analyze the wear behavior of the tools and its change over time. For this purpose, wear tests were carried out for the two different milling processes.
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2.2.1 Milling of Al7075 with solid carbide end mills
Due to the low wear when machining Al7075, EN AC-43,000 was machined to achieve wear on the cutting edge. Because of the high proportion of silicon, the material is highly abrasive and wear occurs more quickly. Tests before showed a similar tool wear compared to milling Al7075 in the investigated range of cutting speed (Fig. 8).
Fig. 8
Flank wear when machining Al7075 and AlSi10Mg with solid carbide end mill (n = 10,000 min−1, fz = 0.17 mm, ap = 5 mm, ae = 6.4 mm, down milling)
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Figure 9 shows the wear diagram of the aluminum milling process.
Fig. 9
Wear diagram for machining EN AC-43000 (n = 10,000 min−1, fz = 0.17 mm, ap = 5 mm, ae = 6.4 mm, down milling)
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The process parameters for achieving defined worn tools were chosen in a range where even wear on the flank face occurred. This was mandatory for the stability investigations, because process damping is only caused by the contact of the flank face. For the same reason, crater wear or breakouts were not desired.
Based on the wear diagrams, three states of wear were selected for the stability investigations. The corresponding cutting edges of the tools are shown in Fig. 10. The wear that occurred on the tools was analyzed with a scanning electron microscope (SEM) Zeiss EVO 60 VP (Fig. 10, left) and an optical topography measurement system based on focus variation Alicona Infinite Focus G5 (Fig. 10, right).
Fig. 10
Wear of solid carbide end mills when milling EN AC-43000 (n = 10,000 min−1, fz = 0.17 mm, ap = 5 mm, ae = 6.4 mm)
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Figure 10 shows the three states of tool wear, which were later used for the stability investigations with Al7075. The cutting edge profile sections of the worn edges show changes of the tool’s microgeometry. With increasing tool wear the clearance angle in the area of wear decreases and becomes negative near the cutting edge. The negative clearance angle of the flank face in the area of wear leads to a larger contact area of the tool and the workpiece and therefore to a higher indented volume of the flank face and workpiece. This results in a higher process damping. Because of bigger cutting edge radii also the ploughing increases which results in higher ploughing forces and puts additional loads to the cutting edge. The profile sections also show that with increasing wear the diameter of the tools decreases. Therefore, an increasing productivity caused by tool wear is only useful for rough machining, where small differences of tool diameters are acceptable.
2.2.2 Milling of AISI 4140+QT with a long cantilevered indexable insert mill
Analogous to the wear investigations of aluminum, the tool wear was also analyzed for milling of AISI 4140+QT. The results are shown in Fig. 11.
Fig. 11
Wear diagram for machining AISI 4140+QT with short, stiff tool (n = 2,000 min−1, fz = 0,08 mm, ap = 2 mm, ae = 12 mm, down milling)
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By using a short tool it was ensured that no chatter occurs and the uniform wear arises. The wear diagrams show the typical course with degressive wear in the beginning, constant wear in the middle and progressive wear at the end of the tool life.
Figure 12 shows the three states of tool wear, which were later used for the stability investigations with AISI 4140+QT. The width of flank wear is evenly distributed along the cutting edge. Crater wear occurred only on the rake face of the insert with the biggest width of flank wear with VB = 50 µm caused by the longer machining time. In this state of tool wear the coating was broken off the cemented carbide.
Fig. 12
Wear of indexable inserts when milling AISI 4140+QT (n = 2,000 min−1, fz = 0.08 mm, ap = 2 mm, ae = 12 mm, cutting time tc = 3/47/102 min)
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3 Results of stability investigations
3.1 Milling of Al7075 with solid carbide end mills
In order to quantify the effect of tool wear on process stability, stability diagrams for various states of tool wear (VB = 0–90 µm) were created experimentally. Figure 13 shows the results for machining Al7075.
Fig. 13
Experimental stability diagrams of machining Al7075 with various tool wear states (fz = 0.1 mm, ae = 16 mm)
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For the new tool, a stability limit between 2 and 4 mm was detected. The absolute stability limit is 2 mm. It describes the value of cutting depth ap that leads to stable milling processes across all spindle speeds. The tool with the smallest investigated width of flank wear VB = 15 µm results in higher process stability for spindle speeds n = 12,000 min−1 and n = 16,000 min−1. For these spindle speeds the maximum depth of cut increased by 1 mm. The stability of the tool with flank wear VB = 30 µm changes for spindle speeds n = 14,000 min−1 and n = 18,000 min−1 where the absolute stability limit for all spindle speeds increases by 1 mm. With the largest width of flank wear VB = 90 µm the largest increase in stability can be achieved. Also the stability of the cutting edge increases due to increasing cutting edge radii. Bigger cutting edge roundings reduce the stress concentration in the tool tip and the cutting edge becomes more stable [5]. The higher process stability is particularly noticeable for n = 12,000 min−1 and n = 20,000 min−1. Here, the cutting depth can be increased to ap = 6 mm (from ap = 2 mm and ap = 3 mm). This increase in stability is expected to result from the increased process damping, caused by greater contact of the flank face. With flank wear VB = 30 µm the absolute stability limit increases from ap,lim = 2 mm to ap,lim = 3 mm.
3.2 Milling of AISI 4140+QT with a long cantilevered indexable insert mill
The stability diagrams of the long cantilevered indexable insert mill with VB = 0–50 µm in milling AISI 4140+QT are shown in Fig. 14. The discrete points for each maximum depth of cut were determined with the method shown in Fig. 7.
Fig. 14
Experimental stability diagrams of machining AISI 4140+QT with various tool wear states (fz = 0.08 mm, ae = 2 mm)
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The stability diagrams show a steady increase of the absolute stability limit with increasing tool wear. The absolute stability limit of a new tool is at ap,lim = 1,25 mm and increases continuously to ap,lim = 1,6 mm with a width of flank wear of VB = 50 µm. This results in an increase of process stability of 28%. The state of tool wear with VB = 50 µm shows also crater wear, which can be one reason for the less increased stability compared to the other states of tool wear. The effect of higher process stability with worn cutting edges is bigger at exceptionally low spindle speeds (n = 1,300 min−1) from 2.8 mm to 6 mm and very high spindle speeds (n = 5,500 min−1) from 2.6 mm to 4.22 mm. This can be attributed to the longer contact time between flank face and workpiece at low spindle speeds [3] and to high speed damping effects due to mode coupling as described in [13].
3.3 Calculated stability charts
Experimental stability investigations are very extensive and time consuming. Calculating the stability limits with simulations offers a possibility to predict the stability limit without the need of experiments on a machine tool. In order to calculate the process stability of the two machining processes, a simulation based on the semi-discretization derived in [8, 14] was used. The process damping force is calculated as described in [8, 15]:
$$F_{{{\text{r}},{\text{pd}}}} \left( t \right) = V\left( t \right)K_{{{\text{pd}}}}$$
(1)
$$F_{{{\text{t}},{\text{pd}}}} \left( t \right) = \mu V\left( t \right)K_{{{\text{pd}}}}$$
(2)
The process damping coefficient was set to the value Kpd = 50,000 N/mm3 and added to the damping of the modes analyzed with the modal analysis as stated in [13]. For the calculation of the stability charts, modal parameters and force coefficients were required beforehand. Stable milling tests with various feed rates were carried out to determine the force coefficients described in [15] and used in the simulation (Tables 3 and 4).
Table 3
Specific force coefficients of machining Al7075 with solid carbide end mills
Ktc
600.71 N/mm2
Krc
279.91 N/mm2
Kac
130.58 N/mm2
Kte
3.28 N/mm
Kre
17.89 N/mm
Kae
4.65 N/mm
Table 4
Specific force coefficients of machining AISI 4140+QT with indexable insert mill
Ktc
1310.2 N/mm2
Krc
893.4 N/mm2
Kac
148.76 N/mm2
Kte
12.37 N/mm
Kre
46.8 N/mm
Kae
2.4 N/mm
Additionally, the geometry of the tool was implemented in the simulation. The micro geometry of the tool wear was approximated according to the profile sections from Fig. 10 and Fig. 12.
3.3.1 Milling of Al7075 with solid carbide end mills
The experimental and simulated stability lobes in milling Al7075 are presented in Fig. 15. The black, continuous line represents the stability limit from the simulation. Above the line, all parameters are unstable, parameters below the line are stable. The colored squares represent the experimental data. The simulation is in good agreement with the experimental results.
Fig. 15
Experimental and simulated stability diagram of machining Al7075 with new solid carbide end mills
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Especially the peak at spindle speed n = 16,000 min−1 matches the simulation well. The peak is the result of the highest rigidity of the setup for the tooth engagement frequency of 800 Hz. The knowledge about this peak is important to choose machining parameters for the highest productivity without stability issues. The result for machining Al7075 with solid carbide end mills with a width of flank wear of VB = 90 µm is shown in Fig. 16. The experiments are in good agreement in a wide range of spindle speeds. Only one stability lobe at spindle speed n = 20,000 min−1 cannot be displayed in the simulation. As assumed in [14], where similar effects occurred, this can be attributed to plastic deformation and thermal effects. These effects cannot be considered in this simulation.
Fig. 16
Experimental and simulated stability diagram of machining Al7075 with worn solid carbide end mills (VB = 90 µm)
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3.3.2 Milling of AISI 4140+QT with a long cantilevered indexable insert mill
The experimental and simulated stability lobes for machining AISI4140+QT with the long cantilevered indexable insert mill without wear are presented in Fig. 17. Overall, there is an overestimation of the experimental stability of the milling process. This is due to the milling strategy of machining ap-ramps. When reaching the critical depth of cut ap,lim, the system needs a certain time to oscillate, so chatter vibrations can be detected. In this delay time the depth of cut increases and instability is detected at a higher depth of cut. To prove this effect a brief trial with constant ap was conducted (Fig. 17, green line).
Fig. 17
Experimental and simulated stability diagram of machining AISI 4140+QT with a long cantilevered indexable insert mill (new inserts)
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The experimental results in milling with constant ap are at the upper stability limit of the simulation and therefore in better agreement with the simulation. This shows that for a accurate determination of the process stability it is better to use a setup for milling with a constant ap. In this case it was decided to keep the setup with ap-ramps because of the fast wear occurrence in milling AISI 4140+QT. The comparison of experimental and simulated stability investigations for the tool with indexable inserts with a width of flank wear of VB = 50 µm is shown in Fig. 18.
Fig. 18
Experimental and simulated stability diagram of machining AISI 4140+QT with a long cantilevered indexable insert mill (VB = 50 µm)
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The results of the worn tool show the same effect of overestimating the stability when machining ap-ramps over a wide range of spindle speeds. The main deviations between experiment and simulation can be seen for low spindle speeds from n = 1,300 min−1 to n = 2,000 min−1 and for high spindle speeds above n = 4,000 min−1. For low spindle speeds the simulation calculates a higher stability compared to the experiment, which means the simulation overestimates the process damping effect of tool wear. For high spindle speeds the deviations between experiment and simulation become larger. This can be explained with the high speed damping effect which cannot be considered in the simulation. The high speed process damping effect results from mode interactions of low frequency modes with the high frequency modes [13]. Despite these deviations, a good estimation of the stability for a tool with defined wear can be made in that range of spindle speeds that is of industrial relevance.
3.4 Wear stability map
To evaluate the potential of higher process stability with increasing tool wear, a method is introduced, which shows the spindle speed, width of flank wear and the maximum depth of cut in one map. With this map, it is possible to quantify changes in terms of stability with tool wear and to select suitable process parameters for increasing productivity.
3.4.1 Milling of Al7075 with solid carbide end mills
For the machining process of Al7075 it can be seen that there is a potential in an early state of tool life at spindle speeds of n = 16,000 min−1 (Fig. 19a) because of small width of flank wear to increase productivity. At this spindle speed, the cutting depth can be increased by 25% with a flank wear of VB = 15 µm. In comparison, at n = 12,000 min−1 and n = 20,000 min−1 this potential only occurs upon a flank wear of VB = 60 µm. Accordingly, despite the lower spindle speed, higher productivity can be achieved earlier than at n = 20,000 min−1. Considering the slow increase in wear during aluminum machining, this knowledge is even more important.
Fig. 19
Wear-stability map Al7075, tool: ratio mill alu RF 100 A, fz = 0.1 mm, d = 16 mm, z = 3, slot milling
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With increasing tool wear, two new areas with a high potential of increasing process stability are created (Fig. 19b). At spindle speeds of n = 12,000 min−1 and n = 20,000 min−1, the maximum depth of cut increases from ap,lim = 2 mm (n = 12,000 min−1) and from ap,lim = 3 mm (n = 20,000 min−1) to ap,lim = 6 mm which corresponds to an increase of stability of 300% and 200% respectively. The areas b in Fig. 19 are the result of the calculation method and will be verified in future investigations.
The presented wear-stability map in milling Al7075 leads to the conclusion that stability peaks becoming higher by initial tool wear and other areas of the map show an increase of stability only with greater tool wear. With tool wear above a limit of VB = 60 µm a higher process stability in other areas can be observed. The knowledge of a wear-stability map for a special milling process will help to fully exploit the potential of the machining setup.
3.4.2 Milling of AISI 4140+QT with a long cantilevered indexable insert mill
The wear-stability map for the machining process of AISI4140+QT is shown in Fig. 20. The highest depth of cut can be achieved with low spindle speeds of n = 1,300 min−1 and width of flank wear from VB = 30 µm (Fig. 20a). Another area with high potential of increasing stability is at spindle speeds of n = 5,500 min−1 and width of flank wear from VB = 30 µm (Fig. 20b).
Fig. 20
Wear-stability map AISI 4140+QT, tool inserts: XOEX10T308R-M06, MM4500, fz = 0.08 mm, d = 20 mm, z = 2, ae = 2 mm
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The results confirm the investigations made in [6, 13]. For high cutting speeds a high speed damping effect can be observed [13] and for low cutting speeds the effect of process damping is higher. The process damping here is also reinforced by the tool wear. With regard to an increased productivity the highest spindle speed of n = 5,500 min−1 will not be the optimum parameter due to the very high wear rate at these cutting speeds. The higher stability at low spindle speeds will lead to a longer tool life with also a high productivity. The presented wear-stability map is a useful method to determine the balance between tool life and high productivity.
4 Conclusion and outlook
In the contribution presented, the stability of milling processes with tools with defined width of flank wear was investigated. For this purpose, milling tests and simulations were carried out. Based on the results shown, the following conclusions can be drawn:
Higher process stability caused by process damping can be achieved with defined worn tools. The responsible mechanism is the larger contact area of the flank face and the workpiece, which leads to a damping force acting in the opposite direction of the tool oscillation.
Even initial flank wear leads to a higher stability in certain areas of spindle speeds. This knowledge can be used to increase productivity in an early state of tool lifetime
Stability peaks are reinforced by tool wear. With higher tool wear in milling aluminum new stability peaks emerge in different ranges of spindle speed.
Wear stability maps can be used to visualize processes with a high potential to increase productivity due to process damping effects, which are the result of increased flank wear.
A simulation based on the semi-discretization method was used to calculate the stability lobes of tools with defined wear in good agreement with experimental results.
The results for milling aluminum Al7075 show that the stability can be increased for certain spindle speeds up to 300% compared to new sharp tools.
Further improvements, e.g. an adapted process damping model, have to be realized, to increase the accuracy of the simulation. Another potential way of calculating stability charts is the use of time-domain milling simulations [16, 17].
Acknowledgements
The presented investigations were undertaken with support of the German Federation of Industrial Research Associations (AiF) within the project “Potential for increasing productivity through wear-related process damping” (IGF 20636 N/1). The authors would like to thank the AiF for the financial and organizational support of this project and the companies Seco Tools and Gühring KG for providing the milling tools.
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