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Transcript of Furação e rosqueamento hsm
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Rapid machining of hardened AISI H13 and D2 moulds,dies and press tools
Helen Coldwell, Richard Woods, Martin Paul,Philip Koshy, Richard Dewes*, David Aspinwall
School of Engineering Mechanical and Manufacturing Engineering/IRC in Materials Processing,
The University of Birmingham, Edgbaston, Birmingham B15 2TT, UK
Abstract
Tools and dies for the forging, die casting and plastics moulding industries are commonly made from AISI H13, heat treated to 4852 HRC,while the press tool sector predominantly uses AISI D2 at a significantly higher hardness of 6062 HRC. Over the last 10 years, the
introduction of high speed end milling has enabled the direct manufacture of prismatic components in the hardened state. The paper briefly
outlines such techniques and details published machinability data. Following on from this, experimental work is presented on the drilling of
hardened AISI H13 using carbide tooling, together with research on ancillary drilling and tapping operations on hardened AISI D2. When
through drilling AISI H13, it was possible to produce up to 210 holes (16 mm deep), with a cutting speed of 30 m/min and a feed rate of
0.1 mm/rev. Drilling data arealso presented on the use of water-based electrical dischargemachining (EDM) dielectric fluids as a replacement
for a conventional soluble oil cutting fluid to allow hybrid HSM/EDM on one machine tool. When drilling and tapping D2, tool life was low
with six and nine holes, respectively. Finally, case study work is detailed, relating to the production of AISI D2 automotive press tool parts, in
which traditional manufacture is compared with high speed machining (HSM) techniques, using both indexable and solid coated carbide
cutting tools. When producing accurate radii on one component, the manufacturing time was cut by 75% using the HSM approach, despite the
relatively poor tool life performance detailed above.
# 2002 Elsevier Science B.V. All rights reserved.
Keywords: Rapid machining; Moulds; Press tools; High speed milling; Drilling; Tapping; EDM/HSM
1. Introduction
High speed machining (HSM) or high speed cutting
(HSC) is usually associated with end milling at high rota-
tional speeds between 10,000 and 100,000 rpm. It has been
applied to a range of applications in the aerospace industry,
originally for the machining of aluminium alloys and more
recently titanium alloys and nickel-based superalloys [1,2].
HSM has also been employed in the machining of the
copper/graphite electrodes used in electrical discharge
machining (EDM). Over the last decade, HSM has increas-
ingly been used to manufacture moulds/dies made from
hardened tool steels such as AISI H13, P20 and D2, for
the production of a wide range of automotive and electronic
components. HSM compares extremely favourably with the
traditional mould/die-manufacturing route which entails
milling the workpiece in the annealed state, heat treatment
to in-service hardness, EDM, grinding and hand finishing
[3]. In order to fully realise the potential of HSM, however,
other machining operations such as drilling, tapping and
reaming need to be addressed.
The UK mould, die and press tool industry is characterised
by large numbers of small companies employing highly
skilled designersand toolmakers. In the past,it has maintained
its market share by producing products of high quality,
however, with increasing imports from countries such as
Japan (81% of UK press tool imports in 1999 [4]), theindustry
is under pressure to compete on price and lead time. One way
in which it is addressing these issues is by adopting HSM.
Benefits with this approach include significant cost/lead time
reduction (a product manufactured using the traditional route
can take over 20 weeks [5]), through the elimination of
multipleprocesses includinghand finishing.Quality improve-
ments stemming from better component dimensional accu-
racy/surface roughness/surface integrity and the elimination
of distortion due to heat treatment are additional factors.
A wide range of tool steels are employed to produce
machined moulds and dies [69]. In forging and die casting,
Journal of Materials Processing Technology 135 (2003) 301311
* Corresponding author. Tel.: 44-121-414-3541;fax: 44-121-414-3958.E-mail address: [email protected] (R. Dewes).
0924-0136/02/$ see front matter # 2002 Elsevier Science B.V. All rights reserved.
PII: S 0 9 2 4 - 0 1 3 6 ( 0 2 ) 0 0 8 6 1 - 0
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the choice is generally hot work tool steels (AISI Group H
series) which can withstand the relatively high working
temperatures involved, typically 315650 8C. These include
chromium-based (e.g. AISI H13) and tungsten-based (e.g.
AISI H21) compositions. Some alloy steels are also utilised.
Forging dies are mainly employed at a hardness of 4556
HRC, while plastics moulds for thermoplastics and thermo-sets are typically made from cold work tool steels including
AISI P20, AISI P6, AISI O1 (oil hardening) and AISI S7
(shock resisting). Tool steels conforming to AISI Group D
are widely used in the manufacture of blanking and cold-
forming dies and in-service hardness for such steels is in the
range 5862 HRC [10].
In previous studies comparing traditional manufacture
with HSM techniques [11,12] it has been reported that
mould, die and press tool components typically range in
overall size from 60 to 500 mm. Components comprise
critical features such as: internal radii down to 1 mm;
external radii down to 4 mm; and M6M12 tapped holes.
The studies also highlighted the use of processes including
drilling, tapping, reaming, grinding, milling (edge profiling,
cavity production and graphite electrode production), EDM
(die sinking, small hole drilling and wire), hand polishing
and vacuum hardening. Typical values for component sur-
face roughness and dimensional accuracy of 15 mm Ra and
550 mm, respectively, have also been reported [13].
2. Literature survey
An extensive body of literature exists on the HSM of
hardened steels, comprising aspects such as operatingparameters, tool life and workpiece surface roughness. This
has been reviewed comprehensively in [3,14], in which
much of the literature relates to AISI H13 hot work tool
steel. In contrast, there is only limited published infor-
mation available on the machinability of AISI D2 cold
work tool steel, despite its extensive use for cold forming
operations.
Polycrystalline cubic boron nitride (PCBN) has been
used successfully to face mill hot work tool steel AISI
H13 (4850 HRC) at cutting speeds between 100 and
200 m/min, with a feed of 0.1 mm/tooth and 1.0 mm depth
of cut [15]. In addition, it has been shown that at a cutting
speed of 180 m/min, a feed of 0.2 mm/tooth and 1.0 mm
depth of cut, PCBN can be used effectively to face mill coldwork tool steel (60 HRC) [16,17]. More recently, PCBN face
milling work on AISI H13 ($52 HRC) and D2 ($58 HRC)has been conducted [10,18]. In the work reported by Koshy
et al., direct comparisons between results are not possible due
to differences in the mode of operation and the radial depth of
cut employed, however, for AISI H13, the volume of material
removed was 120 cm3 compared with 40 cm3 for AISI D2.
The range of tool materials utilised for ball nose end
milling encompasses cermets (ceramic metal composites),
PCBN and limited use of conventional ceramics (silicon
nitride and whisker reinforced alumina), however, coated
cemented carbide tools predominate [1925]. The majority
of carbide cutters are solid, although indexable insert pro-
ducts are also employed [25]. The advantages of the former
include higher accuracy and tool life (in some cases,
>1000 m cut length when machining hardened AISI H13
[20]), however, the purchase price of such tools can be high
(an 8 mm diameter coated carbide ball nose end mill can cost
60120). In contrast, even complex indexable inserts can
be purchased at significantly lower cost (
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Drilling has been reported by Konig et al. [26] and Konig
and Hoff [27] where PCBN was used to drill 32 mm
diameter holes in AISI D2 with a hardness of 60 HRC. A
cutting speed of 100 m/min and feed rates of 0.012
0.025 mm/rev were employed. Further work published by
Konig et al. [28,29] identified the use of a similar drill to
machine a range of ferrous alloys hardened to$62 HRC at acutting speed of 200 m/min and a feed rate of 0.02 mm/rev.
Cutting lengths of 100 mm for AISI A2, 50 mm for AISI D3
and 20 mm for high speed steel AISI M2 were achieved.
Drills made from coated tungsten carbide have also been
used successfully to machine hardened steels. Arai et al. [30]
experimented with cutting fluid supply when drilling 6 mm
diameter holes 30 mm deep in JIS SKD 11 (AISI D2)
hardened to 46 HRC. Usingconventional low pressure cutting
fluid supply, the flank wear after 10 holes was approximately
0.06 mm, however, somewhat surprisingly a higher level of
wear (0.2 mm) was recorded when using high pressure
(7 MPa/$70 bar) fluid. The use of 10 mm diameter TiAlNcoated carbide drills for machining JIS SKD 61 (AISI H13)
hardened to 52 HRC has also been reported [31]. On average,
over 65 blind holes (20 mm deep) could be produced before
drill replacement was necessary. When drilling Ck 45 (AISI
1045) tempered steel at a cutting speed of 80 m/min anda feed
rate of 0.16 mm/rev, TiAlN coated carbide drills achieved
better results than cermet or uncoated carbide products [32].
With surface hardened steel workpieces, carbide tipped
drills (employing high speed steel shanks) were reported to
give tool lives of 1.1 M and 1.0 M for 16MnCr5E(AISI 5117)
and 31CrMo12 workpiece materials, respectively [28].
Tapping is regarded as one of the most difficult machining
operations. Literature available on the tapping of hardenedsteels is extremely limited, however, a number of cutting
tool manufacturers have recently provided details of TiCN
coated carbide taps which they suggest are suitable for tool
steels hardened to 4963 HRC [3335]. Cutting speeds
range from 3 to 5 m/min and quoted tool life is typically
530 holes, depending on hole diameter and depth.
3. Experimental work
The aim of the present work was to assess the drilling and
tapping of AISI D2 and H13 with carbide cutting tools, in
terms of tool life, workpiece quality, productivity and costs.
A secondary aim was to assess the performance of a number
of water-based dielectric fluids, intended primarily for EDM
operations, against a standard soluble oil cutting fluid, in
order to assess the feasibility of a duplex machining arrange-
ment involving HSM and EDM on one machine tool [36]. In
addition, a number of demonstration components were
produced in hardened AISI D2 employing HSM techniques.
These were partly EDM wire machined and then completed
using HSM techniques, instead of traditional manufacturing
operations involving machining in the annealed condition,
grinding and hand polishing.
3.1. Equipment, cutting tools, workpiece materials
and methodology
3.1.1. Drilling of AISI H13
Drilling tests were carried out in two phases. Phase 1
employed a Matsuura FX-5 vertical HSM centre with a
continuously variable spindle speed of 20020,000 rpm, amaximum spindle power of 15 kW and feed rates of up to
15 m/min, phase 2 tests were conducted on a Bridgeport
VMC1000 vertical machining centre with a maximum
spindle speed of 10,000 rpm, a power output of 11 kW
and feed rates of up to 12 m/min. In all tests, the maximum
flank wear and/or chipping on the flank face was measured
using a CCD video microscope equipped with an XY table
employing Mitutoyo digital micrometers. A Somicronic
Surfascan-3D machine was used to measure the surface
roughness of the holes and a Mitutoyo 3-point micrometer
was employed to assess hole size. Roundness and cylindri-
city were measured using a Taylor Hobson Talyrond 300.
In phase 1 tests, cutting force and torque were measured
using a Kistler type 9273 drilling dynamometer and asso-
ciated charge amplifiers connected to a Gould two-channel
oscilloscope.
All tests employed commercial 8 mm stub length AlTiN
coated solid micrograin carbide drills with a 1358 point
angle and 308 helix angle. Through holes were drilled to a
depth of 16 mm. Swarf packing did not occur, therefore,
pecking was not adopted. Cutting fluid (water-soluble oil at
5% by volume) was applied at a pressure of 70 bar and a flow
rate of 17 l/min via two external nozzles directed down the
flutes of the drill. The workpiece consisted of 16 mm thick
discs, which had been EDM wire cut from a bar of AISI H13hardened to 5455 HRC.
Phase 1 investigated the effect of varying cutting speed
and feed rate, the test matrix is given in Table 2. Tests were
stopped when the maximum flank wear/chipping on the drill
reached 0.3 mm or when breakage occurred. As far as
possible, thrust force and torque were measured for the first,
middle (0.15 mm flank wear) and last hole, together with
corresponding workpiece Ra. Sample measurements were
made of hole cylindricity and out-of-roundness. Using the
parameters established in phase 1 that yielded the longest
tool life (in terms of length cut, i.e. cutting speed of 30 m/
min and feed rate of 0.1 mm/rev), phase 2 tests were under-
taken to compare the performance of a standard water-
soluble oil cutting fluid, coded A (at 5% by volume), with
Table 2
Phase 1 test matrix
Cutting speed (m/min) F eed rate (mm/rev)
0.1 0.2
20 @ @ @
30 @ @@
45 @ @@
@ One test performed.
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three other water-based fluids, principally intended for use
as EDM dielectrics: these were coded B, C and D. Com-
mercial considerations preclude disclosure of the actual
fluids. Each test was performed either two or three times
in order to gauge process variability, whilst hole diameter,
surface roughness, cylindricity and out-of-roundness was
measured for the first and last holes.
3.1.2. Drilling and tapping of AISI D2
Limited tests were conducted to establish tool life when
drilling and tapping hardened AISI D2 (60 HRC) as a
precursor to industrial use. Drilling tests were carried out
on a Mori Seiki SV-500 vertical machining centre, with a
maximum spindle speed of 20,000 rpm, a power output of
18.5 kW and feed rates of up to 16 m/min. The machine was
equipped with through-the-tool cutting fluid application.
Tapping tests were conducted on the previously mentioned
Bridgeport VMC1000.
Solid carbide drills (short and long series) with diameters
of 6.87.0 mm and a multilayer TiCN TiN coating wereused. These featured holes for cutting fluid supply. Through
holes were drilled to a depth of 28 mm, with a peck at14 mm. A water-soluble oil (10% by volume) was employed
at a pressure of 10 bar. Cutting speeds of 5 and 10 m/min and
feed rates of 0.05 and 0.08 mm/rev were employed, see
Table 3. Each test was performed once. A screech criterion
was used to determine the end point of the test, which
occurred prior to catastrophic failure of the drill. In addition,
the maximum flank wear was measured at the end of tests.
In tapping tests, M8 TiCN coated solid carbide taps were
used at a cutting speed of 3 m/min (rotational speed
120 rpm) with an appropriate oil lubricant. The workpiece
was a 25 mm thick plate. The tapping length was 16 mm and
each test was performed only once. The size of the pre-
drilled through holes was 6.8 mm (test 1) and 6.9 mm (test
2). Tests were stopped when chipping/general fracture wasobserved on the tap. A go/no-go plug gauge was used to
determine thread quality.
3.2. Results and discussion
3.2.1. Drilling of AISI H13
In phase 1 experimental work, the mechanism of tool
failure differed between tests, depending on the combination
of operating parameters. Failure occurred either by small
scale chipping on the flank, progressive wear or large-scale
chipping/fracture at the web. Fig. 1 details tool life results in
terms of length cut. Tool life was significantly better when
operating at the lower feed rate, however, cutting speed
appeared to have little influence over the range tested. The
parameters which gave the longest length cut (42 holes)
were a cutting speed of 30 m/min and a feed rate of 0.1 mm/
rev. Large variations in the thrust force and torque values
were observed between tests, see Figs. 2 and 3 which detail
peak values for the first hole using a new drill. The highest
values were recorded when using the higher feed rate of
0.2 mm/rev. Although not detailed, thrust force and torque
increased with tool wear, however, the difference in thrust
force between the first and last holes was typically only
$20%.
Hole surface roughness (Ra) was in the range 0.140.48 mm. This was better than anticipated, typically drilled
holes in standard steels etc. range between 1.6 and 6.3 mmRa[37]. Cylindricity is a measure of the difference between
the radii of two concentric circles that are centred on the
axis of a hole. Stated values refer to the peak-to-valley
distance, which is the minimum radial separation of these
co-axial cylinders which totally encloses all the data points.
Table 3
Drilling of AISI D2 test matrix
Parameter Test (i) Test (ii) Test (iii) Test (iv)
Cutting speed (m/min) 10 5 5 5
Feed rate (mm/rev) 0.08 0.05 0.05 0.05
Drill type/diameter (mm)a A A B C
a A: short series/6.9 mm diameter; B: long series/6.8 mm diameter;
C: long series/7.0 mm diameter.
Fig. 1. Tool life results in terms of length cut when drilling of hardened AISI H13.
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Three holes were tested for cylindricity at each of the three
cutting speeds (20, 30 and 45 m/min) when operating at
0.1 mm/rev feed rate. The results were 20.40, 35.45 and
45.30 mm, respectively. Out-of-roundness results ranged
from 2.85 to 17.75 mm. These values are the mean peak-
to-valley height from 10 measurements made at equal
intervals down the drilled hole.
Phase 2 tool wear against length cut results are given in
Fig. 4. The variability in tool wear was too high to provide a
definitive ranking of fluids, however, it was evident that the
water-based dielectrics could be used effectively as a cutting
fluid, operating at a pressure of 70 bar. The tool life results
for phase 2 (up to 210 holes) were much higher than phase 1
and it was confirmed subsequently by the cutting tool
Fig. 2. Peak thrust force against cutting speed when drilling hardened AISI H13.
Fig. 4. Tool wear against length cut when drilling hardened AISI H13 with a cutting fluid and water-based dielectrics. Note: The legend shows cutting fluid
codes and test numbers in brackets.
Fig. 3. Peak torque against cutting speed when drilling hardened AISI H13.
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manufacturer, that the micro grain carbide used for the drills
had been upgraded over the intervening period to an ultra
micrograin product, designed to give superior performance.
Figs. 58 show hole diameter, surface roughness (Ra),
cylindricity and out-of-roundness values for first and last
holes. The hole diameter values were a mean of three
measurements, taken approximately half way down the hole.
The majority of hole diameters were within 5 mm of the
Fig. 5. Hole diameter of first and last hole for each cutting fluid tested when drilling hardened AISI H13.
Fig. 6. Surface roughness of first and last hole for each cutting fluid tested when drilling hardened AISI H13.
Fig. 7. Cylindricity of first and last hole for each cutting fluid tested when drilling hardened AISI H13.
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nominal value. The water-based dielectrics (B, C and D)
were not as effective as the conventional cutting fluid (A) in
producing accurate holes. With respect to surface roughness
values, the range bars in Fig. 6 indicate the 95% confidence
limits. The data show that a lower workpiece surface rough-
ness could be achieved when using a conventional cutting
fluid (i.e. A) rather than a water-based dielectric, however,
cutting fluid C produced a consistently low surface rough-
ness. As in phase 1, hole quality was exceptionally good for
all the cutting fluids tested, fluids A and C, however,
consistently produced the highest quality holes. Cutting
fluid B generally produced holes of highest (worst) cylin-
dricity while cutting fluids A and D produced the best
results. All of the values recorded for the first and last holeswere within the range recorded for the first holes in phase 1.
The range bars in Fig. 8 indicate the maximum and mini-
mum out-of-roundness values recorded at the 10 equidistant
depths. For fluids A, C and D, the out-of-roundness values
were within the range recorded for phase 1, however, higher
values were found when using cutting fluid B.
3.2.2. Drilling and tapping of AISI D2
When drilling AISI D2 hardened to 60 HRC, it was found
that more favourable results were obtained with shorter
series drills, even though they were used to drill to a depth
6 mm over their recommended maximum. Table 4 sum-
marises the results. With the use of through-the-tool cutting
fluid application and a short series drill, it was possible to
obtain a length cut of 0.168 m (six holes). This is compar-
able with published data for the drilling of 10 mm
diameter 20 mm deep through holes in JIS SKD11($AISI D2) hardened to 60 HRC, where an average toollife of six holes (0.12 m length cut) was obtained [31]. In the
present research, the wear observed on the drill land was
higher on the longer series drills (tests (iii) and (iv)) and it
was concluded that this was probably due to tool deflection
as a result of a small core diameter.
When tapping AISI D2, a cut length of 0.08 m (five holes)
was achieved in test 1 before catastrophic tool failure
occurred. All of the tapped holes were within tolerance
and no significant wear/chipping was observed on the toolprior to failure. Increasing the pre-drilled hole size to
6.9 mm in test 2 nearly doubled the tool life to 0.144 m
(nine holes) before chipping occurred, see Fig. 9. Further
validation is obviously required: however, the use of this
technique was shown to be feasible for one-off/modification
work on pre-hardened press tools.
Direct comparisons between the drilling results for AISI
H13 and AISI D2 are not possible due to the differences in
operating parameters employed. Generally, however, tool
performance for H13 was far better than that obtained
for D2. For example, when drilling H13 (50 HRC) tool
life values in excess of 3 m were achieved in comparison
with less than 0.2 m for D2 (60 HRC), despite the higher
Fig. 8. Out-of-roundness of first and last hole for each cutting fluid tested when drilling hardened AISI H13.
Table 4
Results from drilling AISI D2 (60 HRC)
Test
no.
Cut length
(m)
Maximum flank
wear (mm)
Observations
(i) 0.056 $0.1 Wear on the land(ii) 0.168 $0.1 Wear on the land
Some micro chipping
(iii) 0.028 $0.1 Wear on the land(iv) 0.028 $0.1 Wear on the land
Fig. 9. Minor chipping on tap used for test ii after tapping 0.144 m.
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operating levels employed with H13. It is likely that the
difference in tool life reflects material hardness/composition
differences, especially with respect to the significantly
higher carbon and chromium content of D2, which in the
hardened state, has a microstructure containing large chro-
mium carbide inclusions. For H13, the composition (weight
%) is typically 0.320.45 C and 4.755.50 Cr, whereas forD2 the values are typically 1.401.60 C and 11.013.0 Cr
[38].
4. Machining of demonstration components in
hardened AISI D2 (60 HRC)
The following case studies detail the production of press
tool components using traditional and HSM techniques.
After an in-depth data collection study in a press tool
company involving machine times and cost metrics, four
components were chosen as representative of press tool
parts, which could potentially be produced using HSM
techniques, see Fig. 10.
4.1. Equipment, cutting tools, workpiece materials
and methodology
The Bridgeport VMC1000 vertical machining centre was
used to manufacture the component shown in Fig. 10(a). The
other three components, (b), (c) and (d), were machined on a
Deckel Maho Gildemeister DMC125U universal machining
centre with a maximum spindle speed of 8000 rpm, a power
output of 15 kW and a capability of employing feed rates of
up to 10 m/min. The cutting tools used for the experiments
are detailed in Table 5. The AISI D2 workpiece material was
hardened between 58 and 60 HRC.
HSM tests were conducted using a variety of solid and
indexable insert coated-carbide tools operating at cutting
Fig. 10. Hardened AISI D2 demonstrator components.
Table 5Cutting tools employed to machine demonstrator components
Tool
no.
Description Diameter
(mm)
No.
inserts/teeth
Format ISO classification Coating and thickness
1 Round insert face/end mill 20 2 Indexable insert Tungsten carbide (P20) TiCNAl2O3 6 mm TiN2 Ball nose indexable end mill 16 2 Indexable insert Tungsten carbide (P05-P20) TiCN 3mm TiN3 Ball nose indexable end mill 12 2 Indexable insert Tungsten carbide (P05-P20) TiCN 3mm TiN4 Solid ball nose end mill with
negative rake angle
10 2 Solid carbide Tungsten carbide (K10-K30) TiAlN (3 mm)
5 Solid ball nose end mill with
negative rake angle
6 2 Solid carbide Tungsten carbide (K10-K30) TiAlN (3 mm)
6 Short series drill 6.9 2 Solid carbide Tungsten carbide AlTiN
7 M8 machine tap 5 Solid carbide Tungsten carbide (K10/20) TiCN
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speeds of up to 200 m/min and feed rates of 0.1 and 0.2 mm/
tooth. Tool paths with minimum changes in feed direction
were employed as far as possible and down milling/dry
cutting was used throughout. The operating parameters were
based on results from machinability experiments previously
carried out by the authors [10] and on recommendations
from cutting tool manufacturers [39]. Components (a) and(b) in Fig. 10 were form dies used to produce radii of 3 and
5 mm, respectively, on automotive brackets. Overall dimen-
sions of the components were 170 mm 45mm 50mmand 100 mm 75mm 52 mm, respectively. The work-pieces were cut to shape using electrical discharge wire
machining. Traditionally, these radii would be produced by
hand. It was estimated that a skilled toolmaker would take
6 h to grind and polish the radii on component (a) while
component (b) would take 5 h. The HSM test for component
(a) employed cutting tool 3 at a cutting speed of 200 m/min
and a feed per tooth of 0.2 mm. Similarly, for component (b),
cutting tools 3 and 5 were used at cutting speeds of 200 and
100 m/min and feed per tooth values of 0.2 and 0.1 mm,
respectively.
Component (c) was a die used to form a strengthening
web on a bracket for securing electronic components. The
overall dimensions of the component were 107 mm50mm 50 mm. As before, the component was machinedto shape using electrical discharge wire machining. It was
estimated that CNC milling of the notch (workpiece in the
annealed state) would normally take 3 h. The HSM test
involved use of cutting tools 3 and 5 on a hardened work-
piece at cutting speeds of 200 and 100 m/min and feed per
tooth values of 0.2 and 0.1 mm, respectively. Component (d)
was a complex die cavity used to form another mountingbracket. The overall dimensions were 106 mm 100 mm51 mm with a maximum cavity depth of 9 mm. Previously,
the component was machined in the annealed state, which
took approximately 2 h followed by hardening and hand
finishing. Table 6 details the tool numbers, operations
performed and the corresponding cutting parameters for
the HSM test.
4.2. Results and discussion
Figs. 11 and 12 show the times and costs, respectively,
for each component when employing HSM and traditional
techniques. Despite the low tool life demonstrated in
machinability experiments [10], the use of HSM was shown
to be feasible and beneficial for the AISI D2 press tool
components. Overall, it was found that the savings with
HSM were approximately 60%. As the volume of material to
be removed increased, however, the cost and time savings
reduced. For the tooling used with components (a), (b)
and (c), the maximum flank wear did not exceed 0.3 mm.
Fig. 11. Times for traditional and HSM of hardened AISI D2 demonstrator
components.
Table 6
Cutting tools and machining parameters used for component (d)
Operation Roughing
face
Finishing
face
Roughing
cavity
Roughing
cavity
Roughing
cavity
Finishing
cavity
Finishing
radii
Tool no. 1 1 1 2 3 4 4
Cutting speed (m/min) 100 100 60 120 120 100 100
Feed per tooth (mm) 0.2 0.2 0.2 0.1 0.1 0.1 0.1
Axial depth of cut (mm) 2 0.3 0.4 1 0.5 0.2 0.2
Radial depth of cut (mm) 1 0.5 0.2 0.2
Fig. 12. Costs for traditional and HSM of hardened AISI D2 demonstrator
components.
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For component (d), the inserts employed with tool 1 had to
be indexed several times during the machining operation,
which increased the cost of manufacture and resulted in more
modest time and cost savings of 35 and 44%, respectively.
In an associated industrial application, a modification was
made to a component in a progression tool. The component
required the additional drilling and tapping of four blindholes. Using traditional manufacturing techniques, the part
would have been annealed before drilling and tapping by
hand and then rehardened, typically over a period of 5 days.
Using HSM techniques, the part was drilled and tapped in
the hardened state using a solid carbide coated drill and
tap. Cutting tool 6 (see Table 5) was employed at a cutting
speed of 11 m/min and a feed rate of 0.04 mm/rev. Cutting
tool 7 was employed at a cutting speed of 3 m/min. The
modification took less than 2 h to complete, including setup
and programming time and resulted in an estimated cost
saving of 2000.
5. Conclusions
1. The drilling of AISI H13 (52 HRC) was shown to be
successful using AlTiN coated carbide tools with both
soluble oil cutting fluid and water-based dielectrics
applied at high pressure (70 bar). Chipping was the
prevalent mode of failure.
2. The use of water-based dielectrics as an alternative to
standard soluble oil cutting fluid when drilling hardened
AISI H13 was shown to be possible, allowing the use of a
hybrid EDM/HSM machine tool utilising a single fluid.
3. Tool life values when ball nose end milling and drillingof AISI D2 (5860 HRC) were considerably lower than
for AISI H13 tool steel (4855 HRC), due to the
difference in workpiece hardness and microstructure, the
D2 structure incorporating large undissolved chromium
carbide particles. Typically, the lower carbon and
chromium content of H13 results in much finer and
more uniformly distributed carbides.
4. Tool life when drilling and tapping AISI D2 (60 HRC)
was low and unpredictable, however, in one-off produc-
tion situations it was demonstrated to be highly
advantageous.
5. HSM of press tool demonstrator components in AISI D2
(5860 HRC) was shown to be viable for workpieces
requiring a relatively small amount of machining, for
example the production of radii and notch features.
Time and cost savings of$60% were achieved.
Acknowledgements
The authors would like to thank the School of Engineering/
IRCin Materials Processing at the University of Birmingham,
the TCD/DTI/EPSRC, Portway Tool and Gauge Ltd.,
Bridgeport Machines Ltd., Charmilles Technologies Ltd.,
De Beers Industrial Diamonds Ltd., Delcam Plc, GTI
Corporation Ltd., the GTMA, HR Pearce & Co. (Tools)
Ltd., Rolls-Royce Plc, Sandvik Coromant UK, Spark Tec
International Ltd., and TRT Manufacturing Ltd., for the
provision of funding, equipment and consumables. Thanks
also go to Richard Fasham, John Wedderburn, Julian Price,
Bob Aston and Peter Thornton, University Technicians, fortheir help during the experimental work.
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