1. The document analyzes tool wear and inclusion behavior during turning of a calcium-treated steel using coated carbide tools. 2. It finds that inclusions like MnS, mixed sulphides (Mn,Ca)S, and duplex calcium aluminates deform significantly in the flow zone near the tool. MnS deforms the most while mixed sulphides deform less. 3. The behavior and deformation of inclusions in the flow zone influences tool wear and formation of protective layers on the tool surface. Certain inclusions like mixed sulphides are more likely to form protective layers due to their deformation characteristics.

1. 209
TOOL WEAR AND INCLUSION BEHAWOUR DURING
TURNING OF A CALCIUM-TREATED QUENCHED AND
TEMPERED STEEL USING COATED CEMEmD
CARBIDE TOOLS*
Tool wear, layer formation and deformation behaviour of difkrent inclusion
types in the flow zone of the chip and in the chip-tool interface have been
studied during turning of a calcium-treated quenched and tempered steel
SS2541 (En24, SAE4337) using Tic-Al&-_-coated cemented carbide
inserts. The analysis of inclusions in the flow zone was based on semiautomatic
image anaIysis in a scanning electron microscope. A large adherence in
deformation behaviour between different incfusion types was observed. The
iniluence of Merent inclusions on tool wear and on the forma&m of protective
layers on the tool surface is discussed along with the active wear mechanisms
on tool surface. Dissolution of the coatings into adhered inclusion phases
is indicated as an important wear mechanism, especially when machining
calcium-treated steel with high amounts of calcium-rich sulphides.
1.Intmductiun
It is well established that inclusions in steel have a strong influence on
tool wear in Mach. The effects of sulphur addition and calcium treatment
have been studied extensively during the last two decades fl-S]. These
investigations have led to a qualitative understanding of how different types
of inclusions participate in the wear process. The information has been gained
through studies of the static properties of inclusions or of the corresponding
substances, of their morphologies in the as-rolled steels and through the
wear patterns on the tools. It can be expected that the effect of the inclusions
during wear is controlled by their behaviour in the heavily sheared zones
of the chip or the workpiece facing the tool and on the chip-tool contact
surfaces. This has, however, not been studied previously to our knowledge.
Instead, the deformation behaviour of the inchrsions just before tool contact
*Paper presented at The fnsttute af Met& 1st InternationalConference on the Behaviour
of Materials in Machining, Stratford-upon-Avon,U.K., November S-IO, 1988.
Elsevier Sequoia/Printedin The Netherlands

2. 210
has been estimated from their defo~ab~~ during hot rolling. This has been
evaluated through the shape factors of inclusions in the work material. This
means that the large differences in forming conditions during hot working
and chip formation were not considered. The action of the inclusions during
the tool contact was studied through the wear pattern on the tools and
through the possible presence of protective layers caused by the inclusions
on the tool surfaces. No direct observations of inclusion behaviour in tool
contact were thus made. This means that information is missing on the actual
behaviour of inclusions inside the chip and on the contact surfaces between
the chip, the workpiece and the tool.
The purpose of the present paper is f%stly to describe in a qu~ti~tive
way how different inclusion types in a calcinm-treated quenched and tempered
steel deform in the heavily sheared zone of the chip close to the tool surface,
the secondary deformation zone or the flow zone. This is accomplished by
shape factor determination for inclusions in sections of chips. An image
analyser based on the scanning electron microscope @EM) is utilized, Chips
from turning tests using coated cemented carbide cutting inserts have been
studied. The behaviour of different inclusions in actual contact with the tool
surfaces, both rake and flank, is examined primarily on the side of the chip
contacting the tool and on the machined workpiece. The influence on tool
wear and layer formation is discussed for different inclusion types.
Secondly, the tool surfaces are studied for traces of inclusions and wear
marks. The wear of the coatings at different positions of the cutting insert
is examined and the active tool wear mechanisms during machining are
identified. This paper is devoted to wear mechanisms rather than to tool life
data.
2. Work material
The present study is performed on a calcium-treated quenched and
tempered steel of the type SS2541 (En24, Sm4337). The composition of
the steel is given in Table I. The steel was chill cast and hot rolled to a
diameter of 85 mm and studied in quenched and tempered con&tion. The
mechanical properties are given in Table 2.
3. Inclusions
The amount of different types of inclusions in the work material is shown
in Fig. 1. Mixed sulphides (Mn,Ca)S make up the largest part of the incl~ion
TABLE 1
Chemical composition of the cat&m-treated quenched and tempered steel SS2541 used in
the machining tests
Element c si Mn P S Cr Ni MO Al
AWWWG?(wt.%) 0.38 0.30 0.76 0.005 0.024 1.45 1.30 0.20 0.013

3. 211
TABLE 2
Mechanical properties of the work material in quenched and tempered condition
Yield strength 870 MPa
Ultimate tensile strength 1000 MPa
Fracture elongation (5d) 19%
Area reduction 61%
Hardness HB5/750 300
0.10 -
Pfllr//lAOthers
Duplex
Ca-
aluminate
7
r
I5
Mixed
%OPS-
sulphide
z (Mn.b)S
0
2
=
z
MnS
Fig. 1. The amount of different inclusion types in the work material.
volume in the steel. The other main types are manganese sulphides and
duplex calcium aluminates. The deformation behaviour during chip formation
has been analysed for these three inclusion types. Mn3 is very common in
both untreated and calcium-treated steels. MnS and CaS are completely soluble
in each other at high temperature. In the same steel, mixed sulphides with
very low calcium content can be found as well as almost pure CaS. Although
the relative number of mixed sulphides with very high calcium content is
often low, they are assumed to be very important for the wear of the coatings
on the tool surface. Hardness and deformability of the mixed sulphides
depend on the calcium content. Duplex inclusions are typical for calcium-
treated steels. In most cases they are made up of an oxidic inclusion surrounded
by (MnCa)S. The composition of the oxidic core may vary, depending on
pre-deoxidation.
The plastic deformation of an inclusion can be quantified using the
length-to-thickness ratio (shape factor). The value of this shape factor depends
on inclusion type, applied load, temperature and also particle size. For
inclusions with high deformability, such as Mn3, the shape factor value
increases with increasing particle size. In Table 3 examples are given of
shape factor values for inclusions in longitudinal sections of rolled bar prior
to machining. When the inclusions pass through the different deformation
zones during chip formation, they may be further deformed.

4. 212
TABLE 3
Examples of experimentally determined shape factor values (length f thickness) for different
types of inclusions in rolled bar prior to machining
Inclusia type Shape factor
Mns 6
(Mn,Ca)S 3.5
Duplex calcium aluminate 3.4
TABLE 4
Machining test conditions and tool material data
mg
Speed v=208 m min-’
Feed s=O.3 mm rev-’
Depth of cut a=2 mm
Tic -A1203 -TiN-coated cemented carbide
(GC415 from Sandvik Coromant)
Geometry IS0 TNMM 160408
4. Machining tests
Chips from turning tests were used in the inclusion studies. Cutting
conditions and tool material data are listed in Table 4. The cutting inserts
were coated with three different types of coatings: next to the cemented
carbide matrix a Tic coating 5 pm thick, followed by an AlsO coating 3
pm thick and finally by a very thin (0.1 pm) TiN coating. The identification
of the different types of coatings on the worn cutting inserts was based on
energy-dispersive X-ray (EDX) analysis in the SEM.
5. Image analysis of inclusions in the flow zone
For the analysis of inclusion deformation behaviour in the flow zone,
an SEM-based automatic image analyser has been used. The system combines
automatic image analysis (geometrical classification) with a qualitative EDX
analysis of individual inclusions. The system description, working principles
and examples of practical applications in inclusion analysis are given in
ref. 9.
Software and a methodology for the analysis of inclusions in the flow
zone have been developed. The analysis is based on the study of chips from
the machining tests. Therefore no special types of experiments (e.g. quick
stops) have to be performed and large amounts of test samples are easily
available. The chips were normally coated with nickel to prevent edge rounding
during grinding and polishing. Specimen preparation included mounting,

5. 213
Free
/
surface of chip
structur;l
line
SHAPE FACTOR = XLlYL SHEAR :AXIAY=cot Q
Fig. 2. Schematic view of inclusion appearance in the image analyser during the analysis of
inclusion deformation behaviour in the flow zone.
grinding and diamond polishing according to conventional methods. Lon-
gitudinal, tmetched sections of the chips were studied.
The appearance of the inclusions in the image analyser is shown sche-
matically in Fig. 2. The chip surface facing the tool is included in the image
frame in order to calculate the shear strain and the distance from the tool
rake face to the inclusion. The high resolution of the SEM makes it possible
to detect very small and heavily deformed particles. The evaluation of
geometrical parameters (inclusion size, shape, position and shear) and the
X-ray analysis of each inclusion are performed fully automatically.
6. Deformation of different inclusion types in the flow zone
In this section the deformation behaviour in the flow zone will be
discussed for the different inclusion types in the work material. For each
inclusion type the shape factor values are given as a function of the shear
in the flow zone (or distance from the tool) and of the inclusion size. Shape

6. 214
factor values in the workpiece before machiniug are indicated on the left-
hand side of the diagrams (W).
Of vital importance for tool wear and layer formation is the behaviour
of the inclusions when they are coming in contact with the tool surfaces.
Inclusions which have been sliding against the rake and flank faces of the
inserts have been studied on the chip surface and on the workpiece surface
respectively. For the chips investigated the thickness of the flow zone was
approximately 30% of the chip thickness.
MnS inclusions close to the tool surface are heavily deformed because
of the high shear strain in the flow zone. Especially for relatively large
inclusions, extremely high shape factors (greater than 20) were recorded
close to the rake face (Fig. 3(a)). When the particle size decreases, so does
1
OISTANCTFROMRAJCE WRFACE
Fig. 3. (a) Shape factor values for MnS as a function of the shear in the flow zone. (b) Heavily
deformed manganese sulphides in the now zone.

7. 215
the shape factor value. Close to the tool the shape factors for small MnS
are relatively low. This is due to fragmentation of long, heavily deformed
sulphides into smaller particles with low shape factor. The plastic deformation
of the sulphides is much higher in the flow zone compared to the primary
shear zone. This can be concluded by comparing the recorded values with
the shape factors for inclusions in the workpiece prior to machining (W).
MnS inclusions in the flow zone are shown in Fig. 3(b). Close to the
tool surface the sulphides are so elongated that they are hard to resolve,
even when using SEM. The high deformability of the sulphides makes them
very hard to observe on the chip surface. Occasionally, traces of thin sulphide
hlms can be detected.
MnS probably causes no mechanical, abrasive wear of the tool surface.
The hardness of the inclusions is too low. At low cutting speed (V< 150 m
nun-‘) MnS layers can be detected on carbide tools. These layers may protect
the tool and decrease the diffusion type of wear. However, at high cutting
speed the strength of the sulphide is too low to withstand the contact load
during machining. Adhered sulphide phase will therefore be tom away and
no layer build-up will occur.
6.2. Mixed s&phi&, (Mn,Ca)S
The shape factor values for (Mn,Ca)S are generally lower than for MnS
when data for the same inclusion size are compared. Large (Mn,Ca)S inclusions
can reach high values (X,/u,= 15), but in most cases the values lie in the
internal X,/Y-- = 4-6 (Fig. 4(a)). Probably (Mn,Ca)S inclusions with different
calcium content are included in the analysis, which explains the unexpected
variations in shape factor value for small inclusions.
Fig. 4. (a) Shape factor values for (Mn,Ca)S as a function of the shear in the flow zone. (b)
Comparison of the deformability in the flow zone between an (Mn,Ca)S and sn Mns. (c) An
(Mn,Ca)S and a calcium-containing oxide on the chip surface.

8. 216
The difference in deformability between MnS and (Mn,Ca)S is illustrated
in Fig. 4(b). The size of the particles and the distance from the tool surface
are approximately the same for both inclusions. The MnS is much more
elongated. Due to their low deformability in the flow zone, (Mn,Ca)S can be
observed on the chip surface. Figure 4(c) shows an (Mn,Ca)S lying close
to a calcium ahnninate. Both particles appear to be consumed in a slicing-
off process, leaving the inclusion surface at the same level as the chip surface.
No cavities can be seen in the interface between inclusion and steel matrix.
It is assumed that in order to form layers on the tool surface, it is
necessary for the inclusions to be sliced off and smeared out in the chip-tool
interface. The mixed sulphides often play an spout role in the fo~ation
of layers on carbide tools, both as free inclusions and as part of duplex
inclusions. Their higher hardness compared to the MnS gives the (Mn,Ca)S
a suitable deformation behaviour in the flow zone and in the chip-tool
interface. Similar to MnS, the abrasive wear due to (Mn,Ca)S is thought to
be negligible. However, in some cases tool wear due to dissolution may be
increased because of an tmfavourable combination of tool material and
composition of the (Mn,Ca)S inclusions.
6.3. Duplex calcium aluminate
Duplex calcium-containing inclusions are common in calcium-treated
steels. In most cases the oxidic part of the inclusions is either a calcium
aluminate or a CaAl silicate. In this section the behaviour of duplex calcium
aluminates wiII be discussed. In the investigated materials their normal
appearance is a practically spherical, calcium and ahnninium-containing,
oxidic core surrounded by a mixed sulphide, (Mn,Ca)S.
When the shear in the flow zone is low, high shape factors can be
registered (Fig. 5(a)). Increasing shear close to the tool face results in
decreasing shape factor. No influence of inclusion size can be detected. This
somewhat confusing result is contrary to those for MnS and ~,~a)S, but
can be explained by studying Fig. 5(b). A high shape factor at low shear
levels corresponds to plastic deformation of the sulphide phase (Fig. 5@1)).
When the shear is increasing, the sulphide is separated from the calcium
aluminate, leaving the oxide with only remnants of strIphide phase. This
process results in a decrease in shape factor for the duplex particle. In Fig.
5@2) a calcium aluminate with only a thin sulphide tail is shown close to
the tool. Even though the shear and the temperature are very high in this
part of the flow zone, the spherical shape of the oxide is untiected.
In Fig. 5(c) the remaining sulphide phase can be seen on the chip
surface as a dark rim around the calcium aluminate. The duplex inclusion
appears to be sliced off without any cavity formation in the inclusion-matrix
interface, similar to the (Mn,Ca)S inclusions.
Both the calcium ahuninate and the surrounding (Mn,Ca)S phase are
thought to contribute to the layer formation on carbide tools. This conclusion
is supported by the favourable deformation behaviour in the chip -tool
interface. The absence of plastic deformation of the calcium aIuminates in

9. 217
Fig. 5. (a) Shape factor values for duplex calcium aluminates as a function of the shear in
the flow zone. (b) Duplex calcium aluminates in the flow zone: (hl) 30 q, (b2) 5 w from
the tool surface. (c) A duplex calcium aluminate on the chip surface.
the flow zone indicates that the hardness of the oxides is substantially higher
than for the mixed sulphides. The calcium-containing oxides are thought to
contribute to the abrasive wear of the tool. However, the abrasive wear is
much less than for A1203 inclusions in untreated steels. An important effect
of the calcium treatment is to eliminate the harmful, abrasive ahunina inclusions
and to replace them with more favourabIe ~~ci~-~ou~g oxides.
6.4. InclM behaviow on the tool Jkmk
The deformation behaviour of inclusions sliding against the flank face
of the tool can be studied on the workpiece surface. For calcium-containing
inclusions the deformation behaviour is simiiar to the behaviour on the chip
surface. lhe oxides are sliced off and ~~ci~~on~ sulphides are heavily
deformed and smeared out in the same way as in the flow zone.
7. Tool wear
7-f. Wear pattern
A worn cutting insert is shown in Fig. 6 after 10 mm of machining.
Several different zones with different wear of the coatings can be distinguished
along the cutting edge. The differences in wear rate and composition of the
tool surface between different parts of the tool are considerable. On the
very cutting edge (zone A) the A&O:, coating and the thin TiN coating are
still present. In zones B and E on the rake and flank surfaces respectively
the TiN and A120, coatings are completeIy consumed and only part of the
Tic coating is still left. In the nose area in zone B the Tic coating is worn
through and work material fills a crater in the cemented carbide. Adhered

10. Fig. 6. View of a worn tool after 10 min of turning with thin CaS inclusion layers on the tool
surface, especially in zones A, B and C; cutting speed 208 m min-‘. A, A1203+TiN; B, Tic;
C, Alz03; D, (Mn,Ca)S inclusion layer; E, TIC; F, A1203.
inclusion layers were observed on the tool surface. Considerable differences
in layer composition and layer thiclmess between different areas were detected.
In zones A and B the tool surface is covered with a thin CaS layer. In zone
D, 0.35475 mm from the cutting edge, the tool surface is covered with
a relatively thick (Mn,Ca)S inclusion layer. The composition of the inclusion
layers was analysed using an Auger technique. Using depth profiling it was
shown that no significant amounts of elements other than manganese, calcium
and sulphur were present in the layers. The oxygen content was negligible.
The different zones with different wear and surface composition are
clearly visible in the backscattered image in Fig. 7(a). In Fig. 7(b) the
remaining A1203 coating on the cutting edge is visible and also the narrow
section through the Al,Oa coating (zone C) marking the transition from the
worn ‘DC coating in zone B to the (Mn,Ca)S layer in zone D. Figure 8 shows
a part of the (Mn,Ca)S layer on the rake face (zone D). The thickness of
the layer is approximately 10 pm.
The cracks in the layer are probably due to thermal stresses during the
machining tests. Because of the cracks, small pieces of the layer have been
lost. The exposed tool surface under the inclusion layer displays no wear
marks and corresponds to the appearance of an unworn tool surface. The
chip is apparently not sliding against the surface of the coatings but on the
relatively thick inclusion layer. The wear of the tool is probably negligible.
Even more striking is the appearance of the flank surface (Fig. 9). Zone
E, where the AlzOa coating is completely consumed, constitutes almost the
whole contact area. In the same way as on the rake face, a thin, dark AlzOa
zone (F) indicates the transition from zone E to the unaffected tool surface
outside the contact area. Below zone F, where the contact between workpiece
and flank surface ends, small particles similar to sol.idified drops can be seen
along the whole cutting edge. Using EDX analysis, several Merent elements
can be detected in these particles: manganese, calcium and sulphur (from

11. 219
A Al,O, + TiN
8 TIC
C A'203
0 (Mn,Ca)S inclusion layer
Fig. 7. (a) Overdl view of the rake face. (b) Wear of the coatings close to the cutting edge.
the inclusions in the steel); aluminium and titanium (from the coatings on
the tool); chromium, silicon and (iron) (from the steel matrix). F’igure 9
indicates that a molten inclusion phase wets the work material-tool interface
during machining. The characteristic wear pattern with a completely consumed
A1203 coating close to the cutting edge and relatively thick inclusion layers
on the rake face appears after only approximately 2 min of machining. The

12. A
A’20, + TiN
E TiC
F
A',O,
Fig. 9. The flank face in the middle of the cutting edge.
AlaO coating is thus rapidly worn through. When the Tic coating next to
the cemented carbide is exposed, the wear rate of the coating decreases.
Based on extensive machining tests and tool wear studies for several
QT steels with different inclusion content, a number of different wear me-
chanisms have been identified [lo]. The most important wear mechanisms
are thought to be the following.
(A) Abrasion due to hard oxide inclusions. This mechanism is important
when machining untreated steels containing abrasive A120s inclusions.
(B) Dissolution of the coatings into adhered inclusion phases.
(C) DSusion-controlled wear.
For the particular steel investigated in the present work, mechanism B
is thought to be most important for the wear of the coatings. The abrasive
wear is thought to be of minor importance because of the low amount of
oxide inchrsions. The calcium ahuninates in the steel are relatively favourable
compared to AlsO3 inclusions from the abrasive wear point of view. Fur-
thermore, the extensive formation of relatively thick inclusion layers on the
rake face does probably reduce the importance of diSusion-controlled
wear.
Therefore, during turning of the caM.nn-treated steel, the wear of the
coatings close to the cutting edge is assumed to occur principally in the
following way.
(1) Adhesion of calcium-rich strIphide inclusions on the tool surface.
(2) The mehing temperature of the adhered sulphide decreases to the
temperat~e in the interface between tool and work material owing to
dissolution of other elements from the coatings into the inclusion layer.

13. 221
(3) Melting of the inclusion layer and wetting of the contact surfaces,
resulting in rapid dissolution of the coatings on the cemented carbide.
The wear mechanism is illustrated schematically in Fig. 10. This type
of wear is assumed to be active on both rake and flank surfaces of the tool.
The mixed sulphides with high calcium content are assumed to be very
important for the wear of the coatings even though they are relatively few.
The strength of the sulphides and the resistance to plastic deformation
increase when the calcium content in the inclusions increases. The abilie
of the adhered inclusions on the tool surface to withstand the contact load
during machining is also increased and therefore the inclusion layer is not
tom away from the tool surface. F’ure MnS and (~n,Ca)S with low calcium
content are heavily deformed on the contact surfaces and are easily removed
from the tool surface by the action of the work material.
The melting temperature for pure CaS is approximately 2400 “C [ 111.
Addition of manganese to the sulphide decreases the melting temperature
to a minimum at approximately 1500 “C for a composition of 72 mol.%
MnS. A similar influence of other elements present in the work material -
tool interface (aluminium, titanium, iron and others) can be expected. It
seems reasonable that the melting temperature of adhered CaS inclusion
layers can come down to the temperature on the too1 surface.
F’ig_10. Schematic view of the wear of the coatings close to the cutting edge. A, unworn tool.
B, adhesion of calcium rich sulphide inclusions. C, decrease in melting temperature of the
adhered sulphide due to ~olu~on of elements from the coatings into the inclusion layer.
D, melt&g of the inclusion layer, wetting of the contact surfaces and rapid ~olu~on of the
CO&IlgS.

14. 222
The decrease in melting temperature of the adhered inclusions is not
necessarily a diffusion-controlled process. Inclusion layer, coatings and steel
are in very intimate contact in the cutting zone. The different elements can
therefore be considered as already mixed on the contact surfaces owing to
the high contact loads and high temperatures. After initial wetting of the
contact surfaces, the dissolution of the coatings does probably proceed
rapidly. The mixture consisting of inclusions from the steel, dissolved coating
and work material is pressed out of the contact zone and follows the chip
or workpiece, or can be found on the rake or flank surfaces of the tool.
Adhered CaS has been found on all three types of coatings - Tic, AlaOs
and TiN. The proposed wear mechanism is assumed to be important for all
three coatings. However, the difference in wear rate is considerable between
different coatings. The wear rates have been estimated to be approximately
3 pm mix? in the AlaO coating and less than 1 pm min-’ in the Tic coating
for the machining conditions used. The tool wear studies indicate that turning
of a calcium-treated steel containing calcium-rich mixed sulphides using an
AlaO,-coated tool is unfavourable from the tool wear point of view.
8. Summary and conclusions
Tool wear, layer formation and inclusion behaviour have been studied
during turning of a calcium-treated quenched and tempered steel using coated
cemented carbide inserts. The deformation behaviour of different inclusion
types in the flow zone of the chip has been analysed using semiautomatic
image analysis. The following conclusions can be drawn.
(1) The deformation behavior-u in the flow zone is different for different
inclusion types. Manganese sulphides, MnS, and mixed sulphides, (Mn,Ca)S,
are plastically deformed. This is opposite to the behaviour of oxidic inclusions.
Calcium aluminates do not deform inthe flow zone even though the temperature
and shear strain are very high.
(2) The ability to deform plastically in the flow zone is not a prerequisite
for an inclusion type to contribute to the layer formation on the tool. Of
vital importance for tool wear and layer formation is the behaviour when
the inclusions are sliding against the tool surfaces.
(3) Manganese sulphides become extremely deformed in the flow zone
and in the chip -tool interface. No layers of MnS are formed on the tool
surface at high cutting speed (V= 208 m ruin-‘). The strength of the sulphide
is probably too low to withstand the contact load and the adhered sulphide
layers are tom away. The soft MnS inclusions do not cause any mechanical,
abrasive wear of the tools.
(4) Harder, calcium-containing inclusions such as (Mn,Ca)S and calcium
aluminate are continuously sliced off and smeared out during inclusion contact
with the tool. This behaviour is assumed to be favourable from the abrasive
wear point of view and to be a prerequisite for an inclusion type contributing
to layer formation.

15. 223
(5) Turning of the calcium-treated steel resulted in inclusion layers on
the tool surface. The differences in layer thickness and layer composition
between different areas were considerable. Thin CaS layers were adhered to
the coatings close to the cutting edge. Relatively thick (Mn,Ca)S layers were
formed further out on the rake surface.
(6) For the investigated calcium-treated steel the wear of coatings close
to the cutting edge is assumed to be mainly due to dissolution of the coatings
into adhered CaS inclusion layers. A relatively low amount of calcium-rich
sulphides in the steel is assumed to be important for the wear of the coatings.
(7) The results show that the inclusion layers on the tool surface do
not act as passive ditfusion barriers between steel and tool. Instead, the
inclusion layers interact with the coatings and the combination of inclusion
layer and coating composition are of importance for the wear rate. In particular,
the machining of a calcium-treated steel containing calcium-rich sulphides
using an AlsOa-coated tool is an unfavourable case.
Acknowledgments
This research work has been carried out with financial support from
Sandvik Coromant AB, Kloster Speedsteel AB, Ovako Steel AB, Bofors AB
and the National Swedish Board for Technical Development, which is gratefully
acknowledged. The authors would also like to thank the members of the
research committee, namely Rainer Lepp5nen (Ovako Steel AB), Bjijrn Olsson
(Sandvik Coromant AR), Lennart Sibeck (Bofors AB) and Henry Wisell (Kloster
Speedsteel AR), for valuable discussions.
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