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2. LITERATURE SURVEY
2.1 Organization of Literature Survey:
The researchers after carrying out their work publish the same. This published work forms
the base for getting information about the current status of the work carried in that area. It
also helps in providing guidelines for the further work to be under taken. Literature review
helps in knowing the present trend in a particular area of the research and is useful for
planning the future work.
With this objective in mind the available literature on cryogenic treatment and its effect on
properties on various materials in general and tool steel in particular, tool wear, forms of tool
wear, measurement of tool wear, work carried by different researchers on tool wear/ tool life
models, optimization of parameters for yielding maximum tool life etc. is reviewed in this
chapter.
The research carried out by various researchers on effect of cryogenic treatment on the
properties of tool steels, die steels, stainless steel, cast iron, tungsten carbide, copper
electrodes etc. is discussed in section 2.2.
The tool wear, basic forms of tool wear, measurement of tool wear, tool life, research work
carried out by various researchers on different tool work combinations, models proposed for
evaluating tool wear or tool life using different techniques etc. are discussed in section 2.3.
Based on the literature review, the observations made and objectives of the present work are
discussed in section 2.4
2.2 Cryogenic Treatment:
2.2.1. Background on cryogenic processing:
To understand the effects of cryogenic processing it is essential that one should be acquainted
with the heat treating of metals. The primary reason for heat treating steel is to improve its
wear resistance through hardening. Gears, bearings and tooling for example are hardened
because they need excellent wear resistance for extended reliability and performance. The
8
steps in heat-treating are frequently explained in a simplistic manner but it takes significant
skill and experience to execute heat treatments successfully [5].
Steel is normally raised to the austenizing temperature, usually 1200 0C or higher for heat
treating. Austenite is a soft phase of steel and malleable, hence it is very easy to wear the
structure down with repeated use, therefore the need for heat-treating. Gears and other
tooling are often rough machined or formed in the austenitic state. After a predetermined
period of time at the elevated temperature, which is determined by the phase diagram of the
alloy in question, the material will be quenched in a bath that may be oil, water, brine or
polymeric compounds. The rapid cooling (quenching) of the steel in the quenching medium
will cause the atoms in the microstructure to rearrange in the atomic structure that is called
martensite [5]. The maternsite is harder material and hence gives material a good wear
resistance. Hence more is martensite in matrix of material; more is the hard material and thus
possesses higher wear resistance.
2.2.2 How it all started:
Cryogenic processing has been around for many years but is truly in its infancy when
compared to heat-treating. For centuries the Swiss would take advantage of the extremely
low temperatures of the Alps to improve the behavior of their steels. They would allow the
steel to remain in the frigid regions of the Alps for long periods of time to improve its
quality. Essentially, this was a crude aging process accelerated by the very low temperatures.
What we now understand to have happened was the reduction of the retained austenite and
the increase in martensite. By performing this once secret process the Swiss obtained the
reputation for producing a superior grade of steel [5].
The process of experimentation and understanding of the cryogenic treatment of steels really
got under way during World War II at the Watertown Arsenal in Watertown, Mass. It was
under the direction of Clarence Zener who would later go on to develop the Zener diode. At
that time there were no computer controls so the steel tooling would be immersed in liquid
nitrogen for a brief period of time, allowed to warm up, then placed into service. This method
was crude and uncontrolled. Many of the tools would chip and break immediately upon use
because the immersion process would create a very high thermal gradient in the tool and this
would produce micro-cracks in the body. It was also later learned that the cryo-treatment
9
would convert the retained austenite into un-tempered martensite. But the tools that would
not break would experience a greatly enhanced service life [5].
In the 1960’s cryogenic processors used multi-stage mechanical coolers along with insulated
‘cold-boxes’ to gently remove the latent heat from tooling thereby achieving a much slower
cooling rate, concurrent with longer wear lives. Performing a standard wear test (pin-on-disk)
showed that the wear resistance for these steels could be increased by more than 600%. At
this time it was theorized that the increase in wear resistance was a direct result of the
reduction in the amount of retained austenite [5].
Resistance to abrasive wear was investigated in a parametric study. Five tool steels were
tested after conventional heat treatment, after cold treatment at –84 °C (–120 °F), and after
being cryogenically treated at –190 °C (–310 °F). Figure 2.1 shows the results of these
abrasive wear tests. Cold treatment at –84 °C (–120 °F) improved the wear resistance by 18
to 104%, but the cryogenic treatment results show 104 to 560% improvement [6].
0
1
2
3
4
5
6
7
52100 D2 A2 M2 O 1
Wea
r re
sist
ance
(R
wtr
eate
d/R
wun
trea
ted
) -84 C
-190 C
Figure 2.1: Comparison of Wear Resistance Ratios for Five High Carbon Steels Soaked at -840C and -1940C [6]
A study by the IIT Research Institute [7] published in November 1995 for the Instrumented
Factory for Gears sponsored by the US Army ManTech was conducted to study the effects of
the carburizing process and cryogenics treatments in modifying the microstructure of the
material. The results of the tests as presented at the INFAC Industry briefing, June 13, 2000
were that the deep cryogenic treatment gave 50% extra pitting resistance, 5% more load
10
carrying capacity, and a 40 0F to 60 0F higher tempering temperature. Although these
experiments were performed on AISI 9310 material (standard helicopter transmission gear)
the conclusions show promising results, which may be applicable to the general subject of
mechanical and chemical wear resistance.
2.2.3 Cryogenics defined:
Cryogenics is defined as that branch of physics, which deals with the production of very low
temperatures and their effect on matter, a formulation, which addresses both aspects of
attaining low temperatures, which do not naturally occur on Earth and of using them for the
study of nature or the human industry. In a more operational way, it is also defined as the
science and technology of temperatures below 120 K. The reason for this latter definition can
be understood by examining characteristic temperatures of cryogenic fluids given in Table
2.1 the limit temperature of 120 K comprehensively includes the normal boiling points of the
main atmospheric gases, as well as of methane, which constitutes the principal component of
natural gas. Today, liquid natural gas (LNG) represents one of the largest and fast-growing
industrial domains of application of cryogenics, together with the liquefaction and separation
of air gases. The densification by condensation and separation by distillation of gases was
historically – and remains today - the main driving force for the cryogenic industry,
exemplified not only by liquid oxygen and nitrogen used in chemical and metallurgical
processes, but also by the cryogenic liquid propellants of rocket engines and the proposed use
of hydrogen as a “clean” energy vector in transportation [8].
Table 2.1: Characteristic Temperatures of Cryogenic Fluids [K] [8]
Cryogen Triple point Normal boiling point Critical point
Methane 90.7 111.6 190.5
Oxygen 54.4 90.2 154.6
Argon 83.8 87.3 150.9
Nitrogen 63.1 77.3 126.2
Neon 24.6 27.1 44.4
Hydrogen 13.8 20.4 33.2
Helium 2.2 4.2 5.2
11
Cryogenics is basically a derivative of two Greek words - "Kryos" which means cold or
freezing and "genes" meaning born or one that is produced. Technologically, it means the
study and use of materials (or other requirements) at very low temperatures. Deep Sub-zero
treatment of metals and alloys is a deep stress relieving technology. Whenever material is
subjected to any manufacturing operation, it is subjected to stresses. The stress manifests
itself in the nature of defects in the crystal structure of materials. The most commonly
observed defects are in the form of vacancies, dislocations, stacking faults etc. As the level
of stress increases, the density of these defects increases, leading to increase in inter atomic
spacing. When the distance between the atoms exceeds a certain critical distance, cracks
develop and failure takes place [9].
The third law of thermodynamics states that entropy is zero at absolute zero temperature.
Deep subzero treatment uses this principle to relieve stresses in the material. The materials
are subjected to extremely low temperatures for a prolonged period of time leading to
development of equilibrium conditions. This leads to ironing out of the defects in the
material and also attainment of the minimum entropy state. Grain shape and size gets refined
and is made uniform. Defect elimination takes place and inter atomic distance is reduced.
When the material is brought back to room temperature, the defect level reflects an
equilibrium concentration. Compaction of the crystal structure leads to much superior
abrasive, adhesive and erosive wear resistance and enhances corrosion resistance as well as
fatigue strength and resilience [10].
2.2.4 Effects of cryogenic treatment on properties of materials:
Over the past 50 years, large number of reports have been published regarding substantial
benefits that can be realized by treating steel tools at a low temperature, usually near that of
liquid nitrogen, -196 0C.
Despite the fact that several investigations conducted in the 1940’s failed to confirm any
substantial benefits of cold treatments when used as an integral part of the thermal treatment
cycle, reports of large beneficial effects in production operations continue to appear. Today,
the emphasis is on using cryogenic treatment after the conventional heat treatment.
In general cryogenic treatment using nitrogen as cryogen consists of following stages:
• Slow cooling (i.e., without thermal shock) at a approximate rate of 2.5 0C/min from
ambient temperature to the temperature of liquid nitrogen approximately -196 0C
12
• holding at low temperature up to prescribed period, known as soaking period
• the part is then removed from the liquid nitrogen and allowed to warm at room
temperature in ambient air and
• single-cycle tempering by reheating to a moderately elevated temperature (150 to 315
0C) for about 1 or 2 hours, is usually performed after cryogenic treatment to improve
impact resistance, reduction in brittleness of the part etc. although double or triple
tempering cycles are sometimes used.
Cryoprocessing as discussed earlier is the process of cooling a material to extremely low
temperatures to generate enhanced mechanical and physical properties. In a review carried
out by Wayne Reitz et. al. [11] on cryoprocessing of materials effect of cryogenic treatment
on properties of steel and some copper alloys is described. Research carried out by various
researchers has shown that cryogenic treatment has improved wear resistance, dimensional
stability, electrical and thermal conductivity, and hardness. The metallurgical aspects include
reducing the amount of retained austenite, increasing carbide formation, and enhancing short-
range diffusion. The processing steps in the cryogenic treatment for different materials are
critical.
The effect of cryogenic treatment on properties of different materials with respect to
literature available is discussed in following section.
a) Steels:
In case of conventional heat treatment after hardening, tempering is carried out cooling the
material up to room temperature. There remains certain austenite known as retained
austenite in the microstructure. For eutectoid HSS steel the Mf temperature is approximately
–500C and hence after cooling at room temperature retained austenite is present in the
microstructure [12]. This retained austenite can be transformed into martensite, by reheating
the material which causes distortion on its body. This non tempered martensite may cause
cracks particularly in complex shape HSS tools [13]. Instead if subzero treatment is given to
these materials the retained austenite gets transformed into martensite giving more
dimensional stability in the tool microstructure.
Initially, super cold treatment apparently converts any retained austenite into martensite, and
the martensite is tempered as the steel returns to the room temperature. The martensitic
structure resists plastic deformation much better than the austenitic structure, because the
small carbon atoms in the martensitic lattice ‘lock together’ the iron atoms more effectively
than in the more open centered cubic austenite structure. Tempering the martensite makes it
13
tougher and better impact resistant than un tempered martensite. Martensite is harder and has
more wear resistant structure. Additionally, the cryogenic treatment of high alloy steel, such
as tool steels, results in the formation of very small carbide particles dispersed in the
martensitic structure, between the larger carbide particles present in the steel. These small,
hard carbide particles within the martensite matrix help support the matrix and resist the
penetration by foreign particles in abrasive wear. Also these carbides strengthen the material
without any appreciable change in the hardness [9].
In case of steels it has been observed that wear resistance gets improved from 92 % to 817 %.
Table 2.2 shows the results obtained when the materials were treated at –80 0C and –196 0C
respectively. This increase in wear resistance is basically attributed to conversion of retained
austenite into martensite up to Mf (martensite finish) temperature and thereafter precipitation
of ultra fine carbides [14].
Table 2.2: Percent of Increase in Wear Resistance after Cryogenic Tempering [14]
Material that showed significant improvement
AISI Description At –800C At –1960C
D2 High Carbon /chromium die steel 316 % 817 %
S7 Silicon tool steel 241 % 503 %
52100 Bearing steel 195 % 420 %
O1 Oil hardening cold die steel 221 % 418 %
A10 Graphite tool steel 230 % 264 %
M1d Molybdenum HSS 145 % 225 %
H13 Chromium/molybdenum hot die steel 164 % 209 %
M2 Tungsten/moly HSS 117 % 203 %
T1 Tungsten High speed tool steel 141 % 176 %
CPM 10V Alloy steel 94 % 131 %
P20 Mold steel 123 % 130 %
440 Martensitic stainless 128 % 121 %
Material that did not show significant improvement
430 Ferritic stainless 116 % 119 %
304 Austenitic stainless 105 % 110 %
8620 Carbon steel 97 % 98 %
C1020 Graphite cast iron 96 % 97 %
T2 Tungsten High speed tool steel 72 % 92 %
14
Barron R. F. [15] has attributed the improvement of the wear resistance of these tools to
another mechanism besides the transformation of the retained austenite into martensite. He
verified that the tool steels submitted to conventional heat treatment presented only a small
amount of retained austenite, but those submitted to cryogenic treatment showed better
performance during machining. This new mechanism would be time and temperature
dependent due to the long period (8 hours or more) during which the tools would have to stay
at cryogenic temperatures. He found that the microstructure before the cryogenic treatment
had a relatively large carbides (20µm) dispersed in the matrix. However, after cryogenic
treatment these carbide particles were refined and particles up to 5 µm were observed in the
microstructure. The carbide refinement could in such a way contribute to the improvement of
the wear resistance of the tool. Barron thus attributed this achievement both to austenite
transformation and to the presence of hard and small carbide particles well distributed among
the larger carbide particles within the martensite matrix.
Collins and Dormer [16] studied the effect of deep cryogenic treatment (DCT) on D2 cold
work tool steel. It was found that the DCT samples gave lowest wear rate compared to
conventionally heat treated (CHT) samples. The results were attributed to conversion of
retained austenite into martensite, precipitation of fine carbides and finer distribution of
carbides in the tempered microstructure. This increased toughness and wear resistance both.
V. Leskovek et. al. [17] used vacuum treated M2 HSS for comparing wear resistance due to
cryogenic treatment. The specimens were cryogenically treated for – 1960C, with one hour
soaking. These specimens along with conventional specimen were subjected to sliding wear
test. Also the fracture toughness and hardness was measured. The wear resistance of
cryogenically treated specimens was better than that of conventionally treated specimen.
There was improvement in fracture toughness and hardness in case of cryogenically treated
specimens.
In another research carried out by V. Leskovek et. al. [18] the micro structure of M2 HSS
was found to be modified by combined effect of vacuum treatment and cryogenic treatment
in order to optimize the ratio between hardness and fracture toughness. It was also confirmed
by using a ‘Navy C’ ring test that the dimensional changes of this type of steel can be
controlled by this treatment.
15
Alexandru et. al. [19] carried out research on steels equivalent to M2. The specimens were
subjected to combination of quenching, tempering and cryogenic treatment up to –70 0C.
Tables 2.3 (a) and (b) show these combinations of heat and cryogenic treatment cycles. The
specimens were tested for turning operation and it was found that the life was improved from
22 minutes to 51 minutes. The microstructure was analyzed and the carbide particles were
quantified using SEM, X-ray difractometer, quantitative metallorgaphy and differential
dialometer. The results obtained confirmed that there is an increase in carbide precipitation
(form 6.9 % to 17.4 %) reduction in retained austenite (from 42.6 % to 0.9 %) and increase in
martensite content (from 66 % to 81.7 %).
Table 2.3 (a): Various Heat and Cryo Treatments [19]
A Quenching 1230 ◦C
B Quenching 1230◦C+ double tempering 560 ◦C
C Quenching 1230◦C + sub-zero (−70◦C)
G Quenching 1230 ◦C + sub-zero (−70◦C) + tempering 560 ◦C
H Quenching 1230◦C + tempering 560◦C + sub-zero (−70◦C)
M Quenching 1230◦C + tempering 560 ◦C + sub-zero (−70◦C) + tempering 560◦C
N Quenching 1230◦C + tempering 560 ◦C + sub-zero (−70◦C) + tempering 560◦C
+ sub-zero (−70◦C) + tempering 560 ◦C
Table 2.3 (b): Results of the Heat and Cryo Treatment [19]
A
(%)
M
(%)
C
(%) NC
T
(min)
A 42.6 66.5 6.9 - - B 12.8 74.6 12.5 23410.24 22 C 7.5 84.9 7.6 – 38 G 2.2 85.3 12.5 30928.49 49 H 13.3 71.2 15.5 23788.52 47 M 1.6 19.9 18.5 42869.81 51 N 0.9 81.7 17.4 69646.09 45
A: austenite; M: martensite; C: carbides
NC: amount of carbides smaller than1µm/mm;
T: tool life.
16
R. F. Baron [20] during his research carried out on cryogenic treatment to various materials
including M2 HSS observed significant improvement in the wear resistance. The M2 steel
was cryogenic treated at –84 0C and soaked for 24 hrs. He also found that the wear resistance
further increased when cryogenic temperature was -1960C.
D. Yun et. al. [21] carried out research on cryogenically treated M2 steel specimens. Table
2.4 (a) shows the various combinations of heat treatment and cryogenic treatment (–196 0C)
with varied soaking period. The results obtained are depicted in the Table 2.4 (b), which
shows that there is an increase of 11.5 % in bending strength, 43 % in the toughness. There
is also increase in red hardness of the material ultimately resulting in improved life. When
milling cutters made of M2 steel were cryogenically treated (cycle D) and used for
machining of piston rings made of grey cast iron, 440 rings were machined with this cutter as
against 220 rings machined with conventional heat treated cutter (cycle
Table 2.4(a): Different Cycles Applied to M2 HSS [21]
A Quenching from 1250◦C + triple tempering at 560 ◦C
B Quenching from 1250 ◦C + 1 cycle 24 h sub-zero at −196 ◦C + triple tempering at 560◦C
C Quenching from 1250 ◦C+ 1 cycle 48 h sub-zero at−196◦C + triple tempering at 560 ◦C
D Quenching from 1250◦C + 3 cycle totaling 48 h sub-zero at −196 ◦C + triple tempering at
560◦C
E Quenching from 1250 ◦C+ triple tempering at 560◦C + 1 cycle 48 h sub-zero at −196 ◦C
Table 2.4(b): Results of Different Cycles Applied to M2 HSS [21]
Route Hardness
(HRC)
Red hardness (HRC) BS (MPa) IT (J/mm2)
600 0C 625 0C 630 0C
A 63.7 60.6 57.8 55.7 2583 3.5
B 64.8 62.1 57.1 57.5 2880 4.4
C 65.0 63.0 59.3 58.0 2873 4.4
D 65.4 63.1 61.7 59.5 3096 5.0
E 64.3 61.8 58.1 57.3 2611 3.9
In an experimental work Fanju Meng et. al. [22] used alloy tool steel with composition (wt
%), 1.44C, 0.3Si, 0.4Mn, 12.2Cr, 0.84Mo, 0.43V, 0.022P, and 0.008S for wear test. After
heat treatment cold treatment at 223K and cryogenic treatment at 93K were carried out.
17
Figure 2.2 shows a typical heat treatment cycle of experiments. Tempering was carried out at
453K for 600s after cold treatment and cryogenic treatment.
Figure 2.2: Heat Treatment Cycle [22] The variation of the wear rate with sliding speeds was plotted for specimens austenitized at
1293K, quenched and ultra-subzero treated at 93K, which is shown in Figure 2.3. The wear
rate of specimens after cryogenic treatment is smaller than that of as-quenched specimens
(without any subzero treatment) for whole sliding speeds. Furthermore, it decreases
dramatically at high sliding speed. The cryogenic treatment results show 110 to 600%
improvements.
0
4
8
12
16
20
0.5 1 1.5 2 2.5 3.5Sliding speed (m/s)
Wea
r ra
te (
x10
mm
/ N
-m)
Without subzero treatment
Cryogenic treatment
Figure 2.3: Wear Rate Verses Sliding Speed [22]
X-Ray Diffraction Analysis volume fraction of retained austenite against the subzero
treatment temperature was further plotted as shown in Figure 2.4 for specimens austenitized
at 1293K and 1373K. The volume fraction of retained austenite is 12% for as quenched
specimens after austenization at a 1293K and approximately 6% for specimens after cold and
cryogenic treatment. However, it decreases with treating temperature going down for
293
333
1373
223 Cold treatment
93
Tem
pera
ture
(K)
Time
Aging
1293
453
Austenization
Cryogenic treatment
Tempering
18
specimen austenitized as 1373K. Cold treatments reduce the volume fraction of retained
austenite drastically. Nevertheless, cryogenic treatment reduces it slightly relative to cold
treatment.
0
10
20
30
40
50 100 150 200 250 300 350 400Temperature (K)
Vol
ume
frac
tion
(%
)
Austenization at 1373 K
Austenization at 1293 K
Figure 2.4: Volume Fraction of Retained Austenite Verses Subzero Treatment Temperature [22]
It was concluded that cryogenic treatment increases wear resistance dramatically, especially
at high sliding speed. The specimens after cryogenic treatment show a minimum of wear rate.
Unlike cold treatment, cryogenic treatment promotes preferential precipitation of fine η-
carbides.
Flavio J. da Silva et. al. [23] carried out work on M2 tool steels. They found that the hardness
and the microhardness of the M2 HSS samples were not significantly affected by the
cryogenic treatment. The samples cryogenically treated showed a fraction very close to 0%
of retained austenite. Practically the 25% in volume of the retained austenite observed in the
untreated sample were transformed into martensite by the cryogenic treatment. A superior
performance of the cryogenically treated tools compared to the untreated ones was observed
in the Brandsma rapid facing test. This difference reached 44% in some cutting conditions.
The difference on the percentage of retained austenite of the cryogenically treated and
untreated samples did not alter the abrasive wear rate at the conditions used for the sliding
abrasion tests. This is possibly due to the ability of the austenite of the untreated samples to
harden during plastic deformation either by workhardening or by its transformation into
martensite. These phenomena may compensate the gain obtained by precipitation of fine
carbides in the cryogenically treated samples. The cryogenic treatment increased the
performance of the M2 HSS twist drills. The gain observed during drilling steels adopting
catastrophic failure as the end of tool life criterion varied from 65% to 343% depending on
the cutting conditions used. Shop floor tests with cryogenically treated coated HSS milling
19
cutters presented worse performance than untreated tools when shaping the top surface of the
teeth of gear rings. Overall the cryogenic treatment had favorable influences on the
performance of the tools tested.
D. Mohanlal et. al. [24] used T1, M2 and D3 steels for comparative study on wear resistance
improvement due to cryogenic treatment at -180 0C for 24 hours with standard heat treated
samples. There was an improvement of 110.2 %, 86.6 % and 48 % in life of T1, M2 and D3
steels respectively. The samples were subjected to flank wear tests. Cryogenic treatment was
found to be superior to TiN coatings.
Cord Henrik Surberg et. al. [25] carried out work on AISI D2 steel. The samples made of
AISI D2 material were hardened using different austenizing temperatures. It was found that
the percentage of retained austenite was increased as austenizing temperature increased.
After this hardening treatment, tempering was carried out. The samples were then subjected
to various combinations of cryogenic temperatures and soaking time. The results obtained
showed that the cryogenic treatment reduced the retained austenite present in the samples. A
single deep cold treatment followed by single tempering cycle was found to be sufficient to
reduce retained austenite below 1 %. It was also observed that colder the cold treatment
temperature and longer the treatment time, higher the hardness of the samples. The deep cold
treatment did not affect the fracture toughness or distortion.
J. Y. Huang et. al. [26] carried out work for studying effect of cryogenic treatment on M2
HSS. The samples were treated for –196 0C and soaked for one week. It was found that
cryogenic treatment improved wear resistance of the samples. The improvement in wear
resistance was attributed to conversion of retained austenite into martensite, increase in
carbide population and volume fraction in the martensite matrix and also homogenization of
carbide distribution.
A. N. Popandopulo et. al. [27] carried out dilatometry studies and microstructure analysis
during cryogenic treatment. They concluded that shock cooling of quenched steel induces
transformation not only of austenite but also martensite. For this reason, the cold treatment
should be used for parts and tools with no retained austenite in order to intensify the
processes of tempering and precipitation hardening. Tool life increases 20–30% in this case.
Cold treatment of tools with 15–20% retained austenite restores the cutting ability to almost
the same level as for tools without retained austenite. To prevent cracking and embrittlement
of tools and to increase tool life by 50–100%, it is recommended that the cold treatment be
conducted after tempering at 560 0C for 1 hour with final tempering at 400°C for 30–60 min.
20
A. Molinari et. al. [28] carried out research work for studying effect of cryogenic treatment
on AISI H13 and AISI M2 HSS steels. The samples of both steels were cryogenic treated at –
196 0C with soaking for 35 hours. Field tests were carried out on different tools. There was
improvement in wear resistance leading to improved life. Also laboratory tests were carried
out on both types of steels. It was found that wear resistance of both steels got improved due
to cryogenic treatment. The improved wear resistance in case of M2 steel was attributed to
the increased hardness and that for H13 steel was attributed to increased toughness.
M. Pellizaari et. al. [29] applied DCT to two different cold work tool steels X155CrMoV12
and X110CrMoV8. Several combinations of heat treatment cycles were used. The
combination of cycles is shown in Tables 2.5 (a) and (b). The samples were subjected to
block on disk dry sliding wear test. Wear resistance of both the cold work steels got
increased due to cryogenic treatment. In case of X110CrMoV8 the effect was found to be
more as compared to X155CrMoV12. This is due to secondary hardening through
precipitation of carbides along with the decomposition of retained austenite.
Table 2.5 (a): Heat Treatment Variants Investigated [29]
Code Treatment
A Q + T1 + T2
B Q + T1 + C + T2
C Q + C + T1 + T2
D Q + C + T1 + D
E Q + C* + T1 + D
Table 2.5 (b): Heat Treatment Variants Investigated [29]
(Q=quenching, T= tempering C* =controlled DCT for 35h,
C=direct immersion in liquid nitrogen for 14h, D= stress relieving treatment)
Treatment X155CrMoV12 X110CrMoV8
Q 980◦C ×35min 1040 ◦C ×1.5h
T1 500 ◦C ×3h 500 ◦C ×3h
T2 510◦C ×3h 540 ◦C ×3h
D 240 ◦C ×3h 300 ◦C ×3h
21
Firouzdor V. et. al. [30] used M2 HSS drills for studying the influence of deep cryogenic
treatment on wear resistance and tool life in high speed dry drilling configuration of carbon
steels. The experimental results indicated 77% and 126% improvement in cryogenic treated
and cryogenic and temper treated drill lives, respectively. The results of wear rate test were
in agreement with drill life test. Wear resistance improvement was mainly attributed to the
resistance of cryogenically treated drills against diffusion wear mechanism, due to the
formation of fine and homogenous carbide particles during cryogenic treatment.
Additionally, transformation of retained austenite to martensite played an effective role, i.e.
improved hardness values.
It is well known that the durability of tool steel could be improved by deep cryogenic
treatment. It has been assumed that the increase of service life of tool steel caused by
decrease of retained austenite and/or by formation of nano-scale fine η-carbide. But the
principles of deep cryogenic treatment remain unclear yet. In this research, to manifest the
effect of deep cryogenic treatment on wear resistance, the specimen was emerged in liquid
nitrogen for 20 hours for deep cryogenic treatment after austenitizing and the following
tempering temperature was varied. The microstructure of specimens was observed using
TEM and the mechanical properties and wear resistance were examined. As the tempering
temperature increased, the carbides became larger and fine carbides were formed above
certain temperature. In the case of deep cryogenic treated specimen, the number of carbides
increased while the carbides size was decreased, furthermore, the fine carbide forming
temperature was lowered also. It was considered that the deep cryogenic treatment increased
the driving force for the nucleation of carbides. As tempering temperature increased,
hardness decreased, while wear resistance and impact energy increased. The deep cryogenic
treated specimens showed this tendency more clearly. It was considered that the wear
resistance is affected not only due to the hardness but also due to the precipitation of fine
carbides, and this carbide evolution can be optimized through the deep cryogenic treatment
[31].
Moore, K et. al.[32] carried out experiments on three types of heat treated tool steels to
determine the effects of various parameters on the hardness by cryogenically treating these
steels as compared to those only quenched to room temperature. The three tool steels used for
experimentation were H13, D2 and Vanadis 4. It was found that increase in hardness was
very dependent on cryogenic temperature and that stabilization can affect obtainable
22
hardness. It was confirmed that for two of the steels the hardness was independent of
treatment time. The optimum austenitizing temperatures and cryogenic temperatures within
the liquid nitrogen range were identified.
P. Cohen et. al. [33] used M1 and T15 HSS materials for studying effect of cryogenic
treatment. They conducted the drilling tests on four commonly machined materials: 1018
low-carbon steel (165 BHN), 340 alloy steel (390 BHN), A-2 tool steel (175 BHN), and 304-
S stainless steel (126 BHN). M-1 HSS drills were used with 118° point angles. For all
materials, there was significant increase in tool life, which was measured as the number of
holes produced before drill failure. Better hole finish and roundness complemented this
improved tool performance. In addition, turning tests were conducted on AISI 4340. T-15
tool-steel inserts were used at cutting speeds of 200 and 300 sfm, a constant feed of 0.0075
ipr, and a 0.050" depth of cut. The cryogenically treated and untreated inserts had a tool
signature of (0°, 5°, 11°, 11°, 15°, 15°, and 1Ú32"). At both speeds, tool life was
significantly longer, with flank wear being the dominant wear mode. At 200 sfm, the
cryogenically treated inserts lasted 127.0% longer than the untreated inserts (2180 min. vs.
960 min.), and at 300 sfm, the cryogenically treated inserts lasted 91.4% longer than the
untreated inserts (155 min. vs. 81 min.). After complete testing in the laboratory, laboratory
data was compared with field data. Compared to untreated drills, cryogenically treated M-1
tool-steel drills used by tool-and-die, automotive, and job shops lasted 200% to 300% longer
in the machining of 304-S, 100% longer in the machining of 4340, and 425% longer in the
machining of 1018-CR material.
Chia-Hung Sun [34] carried out research for studying effects of deep cryogenic treatment on
properties of AISI D2 tool steel. The result demonstrates that decrease in the cold treatment
temperature increase the hardness of the specimens, which were attributed to the greater
under-cooling to create greater activation energy to enhance the transformation of retained
austenite to martensite. The hardness derived from cryogenic treated specimens was slightly
higher than that of the sub-zero treated. This is attributed to the finer carbides precipitation
rendered from greater under- cooling of cryogenic treatment. The results demonstrate that the
content of retained austenite treated from either sub-zero or cryogenic presented almost the
same extent of reduction after they were single or double low temperature tempered.
However, the retained austenite was significantly reduced when they were tempered at high
temperature following a cryogenic treatment or sub-zero treatment. It is accepted that a major
23
factor contributing to wear resistance improvement through sub-zero or conventional heat
treatment is the removal of retained austenite. In the process of cryogenic treatment at
-196 0C, the retained austenite is transformed into martensite while martensite is decomposed
and ultra-fine epsilon-carbides are diffusively precipitated. The mechanism that cryogenic
treatment contributes to wear resistance is attributed to the precipitation of epsilon-carbide,
which enhances the strength and toughness of martensite matrix, rather than the removal of
the retained austenite only, which exhibited the better wear resistance by a minimum of flank
wear.
V. Soundarajan et. al. [35] used hardened carbon tool steel AISI1095 for research purpose.
In this study as a part I hardening was carried out on AISI1095 carbon tool steel of different
L/D ratio with conventional quenching media like purified water, aqueous solution and hot
mineral oil. As part II, the specimens were hardened in which quenching was carried out as
in part I and then these hardened specimens were quenched in liquid nitrogen at subzero
condition. The specimens were tested for hardness and wear loss. The result showed
improvement in wear resistance of the cryo quenched specimens than the conventional.
M. Kalin et. al. [36] have investigated the effect of four different tempering temperatures of
vacuum and cryogenically treated ESR AISI M2 high-speed steel on the resulting
combinations of microstructure, hardness and toughness and their effect on the wear
mechanisms at different loads. The results showed that at relatively high loads the different
treatments resulted in an order-of-magnitude difference of wear resistance, while at low loads
the selected treatments were efficient enough to keep the wear within the mild wear regime
and small variations between the samples. However, the overall wear transition did not occur
at any load used or any sample treatment, although some small differences in wear
mechanisms can be seen, primarily depending on the fracture toughness of the samples.
Nadig D.S. et. al. [37] had conducted an experiment to study the effect of cryogenically
treated HSS tool made of M42 with composition as Carbon 1.1%, Molybdenum 9.5%,
Vanadium 1%, Cobalt 8%, Chromium 4% and Tungsten 1.5%. The square tool of dimension
3/16″x 3/16″x 4″ length which was cryogenically treated at -80oC was subjected to a standard
sliding wear testing pin on disk apparatus. For comparative study a non-cryogenically treated
HSS tool (M42) was tested for wear resistance and frictional force. From the experiments, it
was observed that the Cryo-treated tool has developed higher wear resistance property. The
24
improvement in the wear resistance was around 33%. This improvement in wear resistance is
caused due to the conversion of soft retained austenite to hard martensite, formation of Eta-
carbide and development of a uniform and refined micro structure.
P Sekhar Babu et. al. [38] studied the improvement in wear resistance of M1, EN19 and H13
tool steels after cryogenic treatment. The materials were tested for improvement in abrasive
wear resistance after cryogenic treatment at different temperatures below 0°C. All the
samples were first heat treated as per standard norms and re tempered after cryogenic
treatment. The samples were treated at 0 0C, -20 0C, - 40 0C, -80 0C and -190 0C. It was
observed that the wear resistance improved by 382% for M1 steel, 335% for H13 steel and
by 319 % for E19 steel samples. The improvement in wear resistance in all these materials
showed incremental increase depending on the cryogenic treatment temperature.
Mahmudi, R. et. al. [39] also carried out research on effect of cryogenic treatment on M2
HSS. They compared the levels of hardness, impact toughness and wear resistance of M2
high-speed steel after conventional heat treatment with those imparted by additional sub-zero
and deep cryogenic processing.
Franjo Cajner et. al. [40] used PM S390 MC high speed steel for studying effect of cryogenic
treatment. The samples were subjected to different austenizing temperatures and thereafter
for triple tempering at higher temperatures, i. e. 540 0C. The samples were then subjected to
the deep cryogenic treatment at -196 0C with a soaking time of 25 hours. The cryo treated
samples were subjected to tempering at a temperature of 540 0C for 2 hours. The results
showed that there is an improvement in wear resistance of the material. There was no
significant improvement in toughness due to cryogenic treatment.
C. L. gogte et. al. [41] used M2 and T42 tool steel samples for their research work. The M2
and T42 HSS samples were austenized at 1210 0C and 1240 0C respectively. The austenized
samples were then subjected to triple tempering at a temperature of 560 0C. The samples of
both the materials were then cryo treated at different temperatures and different soaking time.
The samples were subjected to optical, SEM, TEM and x-ray micrography to see the results
and also to quantatively note the changes those are taking place in the steels. It was found
that there is a distinct change in the dispersion of carbide and also in the density of carbide
suggesting a dissolution of carbide into the matrix during the deep subzero treatment.
25
In a research carried out by Fanju Meng et. al. [42] Fe-1.4Cr-1C bearing steel was cryogenic
treated at –500C and –1800C. These cryogenically treated specimens were subjected to wear
test. The wear test was carried out on sample on wheel type. The wear resistance of the
specimens treated at –500C and –1800C showed improvement in wear resistance. In case of –
1800C specimen wear resistance improvement was higher than that of in case –50 0C treated
specimens. Also volume fraction of retained austenite was 66 %, 4.4 % and 4 % in case of
nontreated, –50 0C and –180 0C treated specimens respectively.
A. Bensely et. al. [43] used case carburized steel (En353) specimens for studying effect of
cryogenic treatment on wear resistance. The samples were cryogenically treated for –50 0C
(SCT) and –180 0C (DCT). These samples were soaked for 5 hrs and 24 hrs at –50 0C and –
180 0C respectively. These three types CHT, SCT and DCT samples were subjected to dry
sliding wear test. The wear resistance improvement amounted to 85 % in case of SCT
samples over CHT samples and 372 % in case of DCT samples over CHT samples.
In another research carried out by A. Bensely et. al. [44] case carburized 815 M17 steel was
studied for tensile behavior due to cryogenic treatment. Tensile test specimens were
conventionally heat treated and then Shallow Cryogenic Treatment (SCT) (–50 0C) with
soaking for 5 hours and Deep Cryogenic Treatment (DCT) (–196 0C) with soaking for 24 hrs
was given to samples. The CHT, SCT and DCT samples were subjected to tension test. The
results obtained indicate reduction in tensile strength for SCT and DCT samples over CHT
by a factor of 1.5 % and 9.34 % respectively.
S. Zhirafar et. al. [45] used 4340 steel for studying effect of cryogenic treatment on
mechanical properties. The 4340 steel samples were conventionally heat treated and
thereafter cryogenically treated at –196 0C with soaking for 24 hrs. Mechanical testing
involved hardness and charpy impact tests for specimens. The results obtained showed an
improvement in hardness, slightly detrimental effect (14.3 % decrease) in impact energy
toughness and improvement in fatigue limit. The increase in fatigue limit was attributed to
higher hardness and strength of the material due to cryogenic treatment.
It is well known that the wear resistance of tools can be improved using deep cold treatment
to produce nucleation sites for the nano-sized carbides that form in the martensite during low
temperature tempering following the extended treatment times. However, inconsistencies in
26
the processing techniques used, particularly the soaking time at very low temperature and the
steel’s previous thermal history, have led to different conclusions as to the exact mechanisms
involved. This paper reviews current thinking and attempts to explain the different results
obtained in terms of the processing parameters and to elucidate the implications for the
practical application of the technique to obtain optimum properties. An optimized process
route using liquid nitrogen as the coolant is recommended and a possible technique to make
further improvements in the process is suggested. As part of an optimized heat treatment
cycle, deep cold treatment can dramatically improve measured wear by the precipitation of
nano-sized carbides in the primary martensite. The transformation of retained austenite to
martensite is a minor additional benefit. In many practical uses of tools this increase in
measured wear translates into longer tool life [46].
b) Stainless steel:
Load-carrying cruciform joints with LOP were prepared by P. Johan Singh et. al. [47] using
6-mm thickness AISI 304L austenitic stainless steel cold rolled plate. The initial joint
configuration in the case of the cruciform joint was obtained by securing the long plates and
stem plate in a cruciform position by tack welding in a fixture. Subsequently, fillets were
made between the long plate and stem plate using semiautomatic gas metal-arc welding
process, argon shielding gas and 308L electrode. Great care was taken to obtain the best
possible joint alignment. After welding, the fatigue samples were cut into required sizes. The
cut samples were again machined for better surface finishing. Cryogenic treatments were
given to half of the specimens prepared. In general the basic steps in a cryogenic treatment
were as follows:
1. Ramp down: The ramp down in temperature to -185 0C with ramp-down time of 4 to 10
hours range.
2. Hold: At-185 0C, the material was soaked for 20–30 hours.
3. Ramp up: The chamber was then warmed to +150 0C to temper the primary martensite,
after which it was returned slowly back to room temperature.
Two types of cruciform samples with LOP were tested (i) as-welded condition (non treated)
(ii) after cryogenic treatment (treated). The fatigue properties of cryogenically treated
samples have shown improvement. The strain-induced martensite formed during the
cryogenic treatment and the associated generation of compressive stresses in the weld metal
is considered to be effective in fatigue life extension of welded joints in the high cycle
regime.
27
J. D. Darwin et. al. [48] used Taguchi’s method for optimization of cryogenic treatment to
maximize wear resistance of chrome silicon spring steel. Sample of piston rings made of
chrome silicon spring steel SR10 were cryogenic treated using different factors such as
cooling rate, soaking temperature, soaking period, tempering temperate and tempering
period. L9215 array was used for the first experiment set up and L93
4 for the second set up.
All samples were subjected to sliding wear test. The results obtained indicated that soaking
temperature was the most significant factor for improvement in wear resistance. The
optimum soaking temperature which gave maximum wear resistance was –1840C. The
soaking period also affected wear resistance. 24 hours soaking yielded maximum
improvement. The wear resistance was improved by 48 %.
Also 18 % Cr martensite stainless steel SR34 piston rings were cryogenic treated using
different factors using Taguchi’s method and it was found that wear resistance got improved
by 43.8 % by using optimum conditions [49].
c) Cast iron:
Hao-haui-Liu et. al. [50] carried out investigation on 3Cr13Mo1V1.5 high chromium cast
iron due to cryogenic treatment. The testing high chromium iron was cast from 1450 0C as ф
80 mm balls by chilled mould. The ball was cut into sub-critical treatment samples,
cryogenic treatment samples and X-ray diffraction samples. The test samples were subjected
to sub-critical treatment at serials of test temperatures. The holding time was 1hr for each
temperature. After sub-critical treatment, the samples were air-cooled to room temperature or
put into liquid nitrogen directly and held for 3 hrs. The samples were subjected for abrasion
resistance experiments. The investigation had lead to conclusions as
1. Cryogenic treatment can effectively reduce further the austenite content after the sub-
critical heat treatment, but cryogenic treatment can not make retained austenite transform to
martensite completely. Cryogenic treatment can markedly boost hardness and abrasion
resistance of high chromium.
2. Cryogenic treatment accelerates the precipitation of secondary carbides and makes the
secondary hardening peak advanced at a lower temperature.
3. When there was about 20% retained austenite in matrix, abrasion resistance reaches the
maximal, and decreases sharply, if retained austenite content is less than 20%.
28
d) Tungsten carbide inserts:
Seah et. al. [51] did some study on the effect on cryogenic treatment on tungsten carbide and
found that the treatment improved the wear resistance. The increase in wear resistance was
attributed to increase in number of η-phase particles after cryogenic treatment.
A.Y.L.Yong et. al. [52] used sumitomo (sumitomo SNGG 23) cutting tool inserts for
cryogenic treatment. The inserts were treated at –184 0C for a soaking period of 18 hours.
There after the inserts were tempered. The treated inserts were used for turning operation
and flank wear of the inserts was measured using Mitutoyo toolmaker’s microscope. The
results obtained showed improvement in wear resistance of inserts. He also found that the
state of cryogenically treated inserts is not a permanent state, but a metastable state as at high
temperatures wear resistance is reduced at a faster rate.
Sumitomo milling inserts were cryogenically treated to a temperature of –184 0C for a
soaking period of 24 hrs. These inserts were used for face milling of ASSAB 760 medium
carbon steel with feed, depth of cut as 0.15 mm/tooth and 0.1 mm respectively, cutting
speeds used were 294.5, 343.5, 392.7, 409.9, 540.0 and 589 m/min. Flank wear of the inserts
was measured with a toolmaker’s microscope. It was found that cryogenic treatment to the
inserts improved tool life to certain extent [53].
B. S. Ajaykumar et. al. [54] carried out work on cryogenically treated P-30 tools. A statistical
model is developed to find the correlation between the temperatures induced during
machining process with the life of the tool. The purpose of the research was to determine
how cryogenic treatment responded to P-30 inserts by improving its life during machining
process. The result of the experiments indicated an increase in the tool life by an amount of
20 % when job is made to run at a speed of 71.62 m/min for different feed rates. To compare
the changes in temperature between treated and untreated as well as the tool life, analysis of
the variance was applied and it is found that they are statistically significant and all means
are different from one another. The mean tool life between the treated (22.385) and untreated
(19.79) was compared using independent t- test and it is found that the mean difference
between them is statistically highly significant. This shows that the tool life of treated
specimen is much higher compared to the untreated group. It was found that correlation
coefficient between tool life and temperature was negative. Relation between the two through
statistical modeling indicates that an increase in temperature affects the tool life.
29
e) Nickel-Titanium instruments:
Nickel titanium k-files were cryogenically treated at a temperature of –196 0C with soaking
period of 10 min. These files were subjected to a test for evaluating cutting efficiency.
Cryogenic treatment resulted in increased microhardness, but this increase was not detected
clinically. There was no measurable change in elemental or crystalline phase composition
[55].
f) Cr-Zr-Cu alloy spot welding electrodes:
W u Zhisheng et. al. [56] in their investigation used Cr-Zr-Cu alloy spot welding electrodes
for studying effect of cryogenic treatment. The spot welding electrodes were treated at
–150 0C and –170 0C for a soaking period of 2 and 4 hours. The investigation concluded that
electrode life was improved from 550 to 2234 welds by deep cryogenic treatment. The
capacity of heat transmission and the electrical conductivity of electrodes were improved by
deep cryogenic treatment. The improvement in life was attributed to finer grains in case of
deep cryogenic treated electrodes.
g) Cryogenic cooling effects in turning:
Machining of steel inherently generates high cutting temperature, which not only reduces
tool life but also impairs the product quality. Conventional cutting fluids are ineffective in
controlling the high cutting temperature and rapid tool wear. Further, they also deteriorate the
working environment and lead to general environmental pollution. Cryogenic cooling is an
environment friendly clean technology for desirable control of cutting temperature.
Experimental investigation of the role of cryogenic cooling by liquid nitrogen jet on cutting
temperature, tool wear, surface finish and dimensional deviation in turning of AISI-4037
steel at industrial speed feed combination by coated carbide insert was studied by N. R. Dhar
et. al. [57]. The results when compared with dry machining and machining with soluble oil
as coolant indicated substantial benefit of cryogenic cooling on tool life, surface finish and
dimensional deviation. This was attributed mainly to the reduction in cutting zone
temperature and favorable change in the chip–tool interaction.
A tool was modified by Ahsan Ali Khan et. al. [58] to apply liquid nitrogen as coolant
through a hole made in the tool so that liquid nitrogen can be directly applied to the
30
machining zone during machining of stainless steel SUS 304 with carbide tools coated with
titanium carbonitride. It was found that the tool life increases more than four times by
applying liquid nitrogen using the modified tool. Application of this cryogenic cooling was
found to be more effective at higher cutting speeds. It was also observed that cryogenic
cooling is efficient at a higher feed rate rather than a higher depth of cut.
Titanium alloys are being increasingly sought in a wide variety of engineering and
biomedical applications. Machining and grinding of these alloys imposes lot of constraints.
Rapid tool wear encountered in machining of titanium alloys is a challenge that needs to be
overcome. Researchers in order to reduce the cutting zone temperatures and enhance the tool
life investigated a process of cryogenic machining with liquid nitrogen as a coolant. The
effects of cryogenic cooling were studied on growth and nature of tool wear while turning Ti-
6Al-4V alloy bars with microcrystalline uncoated carbide inserts under dry, wet and
cryogenic cooling environments in the cutting velocity range of 70–100 m/min. Cryogenic
cooling by liquid nitrogen jets enabled substantial improvement in tool life through reduction
in adhesion–dissolution–diffusion tool wear through control of machining temperature
desirably at the cutting zone. It was concluded that proper application of cryogenic cooling in
machining Ti-6Al-4V alloy provides reduction in tool wear, which can lead to enhancement
of productivity along with environmental friendliness [59].
The work carried out by various researchers on effect of cryogenic treatment on properties of
different materials as discussed above indicates that some materials give good response to the
cryogenic process and their properties are altered. Some materials show less or no response
to the cryogenic treatment. Tool steels come under the category of good response to the
cryogenic treatment and the basic property improved in case of tool steels is wear resistance.
The improvement in wear resistance of one such newly developed tool steel is the work
undertaken in the present research.
In next section tool wear, types of tool wear, measurement of tool wear, tool life and a brief
review of the literature available on tool wear models, tool life models, optimization of
parameters for maximizing tool life etc. are discussed.
31
2.3 Tool Wear:
2.3.1 Introduction:
As discussed earlier, this section contributes towards literature review related to tool wear.
Tool life is the most important criterion for assessing the performance of a tool material,
machinability of work material and for determining cutting conditions. Flank wear is
generally considered as the decisive factor of the tool life. However, at higher cutting speeds
and metal removal rates, the tool failure may also be caused by cratering [2]. Different types
of tool wear are discussed in the following section.
2.3.2 Geometry of tool wear:
The progressive wear of the cutting tools can take three forms as shown in Figure 2.5:
(i) Wear on the tool flank characterized by the formation of a wear land as a result of the
newly cut surface rubbing against the tool flank, known as flank wear.
(ii) Tool wear on the rake face characterized by the formation of a crater or a depression, as a
result of chip flowing over the tool rake face known as face wear; and
(iii) Wear on the nose of the tool as a result of the work surface rubbing against the tool nose
known as nose wear.
Figure 2.5: Forms of Tool Wear
2.3.3 Flank wear:
As a rule, the extent of flank wear is considered a dependable criterion for judging the life of
the cutting edge. The flank wear is obtained on the flank of the tool. The flank wear can be
more easily observed and measured than other types of wear. It is relatively easy to predict
when a given amount of wear will be reached once the wear rate has been established. The
development of flank wear initially assumes a high rate followed by a more or less linear
increase and finally rises rapidly when the amount of wear crosses beyond the critical value
[2].
32
A typical case of flank wear development with respective to time is shown in Figure 2.6. It
can be seen from this figure that the graph can be divided into three definite regions A, B and
C. In the region A, the wear grows rapidly within a short period of time because during the
initial contact of the sharp cutting edge with the work piece, the peaks of the micro
unevenness at the cutting edge are rapidly broken away. In the region B, the wear progresses
at a uniform rate. In the region C, the wear rate is rapid and may lead to a catastrophic
failure of the tool. In general, it has been found that the most economical wear land at which
the tool needs to be removed and re-sharpened is just before the start of the rapidly increasing
portion of the curve. In the case of high-speed steels, the linear rate of wear section of the
curve is quite flat and the final failure occurs suddenly [2].
0
0.01
0.02
0.03
0.04
0.05
0 20 40 60 80
Tool life, min
Too
l wea
r, in
Figure 2.6: Wear verses Cutting Time [4]
The wear land on the flank will not be generally uniform along the entire cutting edge length.
Depending upon the machining conditions, the following types of wear lands or
combinations of them are generally observed [2].
1. Excessive wear at the nose end of the flank is brought about by deformation of the
tool material which reduces the relief in the area, thus increasing the rate of wear.
This can also be brought about if the crater on the rake face breaks through the nose
area.
2. Irregularities in the wear along the whole cutting edge length due to minute chipping
or attrition of the cutting edge
3. Excessive wear at the line of depth of cut. This can be either due to the work
hardened surface caused by the previous cut or heat treat scales or by other abrasive
materials on the work piece [2].
C A B
C
33
2.3.4 Face wear:
As the cutting speed increases, the tendency of the cutting tool to fail by cratering increases.
The tool-chip interface temperature increases with cutting speed and at the higher
temperatures the rate of material removed from the tool increases. The pattern of crater wear
indicates that the wear in this region is primarily due to the diffusion or chemical reaction
between the tool and chip material. At low cutting speeds a crater may be formed owing to
the action of the chip flowing over the tool rake face. The narrow region close to the tool
cutting edge is protected from the action of the chip by the presence of stable built-up edge.
This cavity of crater has its origin not along the cutting edge, but at some distance away from
it and within the chip contact area. It is to be noted that the maximum tool-chip interface
temperature occurs at a distance from the cutting edge, and in this region the crater is
initiated. As the crater wear progresses with time, it becomes wider, larger and deeper, and
approaches the edge of the tool. If the crater wear is allowed to proceed too far, the cutting
edge becomes too weak and breaks down suddenly. The depth of the crater and the distance
of the center line of the crater from the cutting edge are measured for the quantitative
assessment of the crater wear [2].
2.3.5 Measurement of flank wear:
Tool wear is determined by observing and measuring the wear as it develops, specifying the
effective cutting time elapsed before a stipulated degree of wear is reached. The flank wear
can be measured readily on a toolmaker’s microscope or a calibrated magnifying glass
having about 10 x magnifications. The flank wear is generally measured from the original
cutting edge. If the flank wear is uniform along the three zones as shown in Figure 2.7 the
mean value VB is determined. If more wear develops in any one part of the cutting edge, the
maximum value VBmax is recorded and for the calculation of the mean value of wear, the
zone containing the maximum value is not considered [2].
Figure 2.7: Regions of Flank Wear [2]
Zone A
Zone B
Zone C
VB
L/4 L/2 L/4
L
34
2.3.6 Tool life:
Tool life may be defined as the effective cutting time between two consecutive re-
sharpening. When the wear reaches a certain value the tool is not capable of further cutting
unless it is re-sharpened. Tool life is the most important criterion for assessing the
performance of a tool material, machinability of work material and for determining cutting
conditions. Flank wear is generally considered as the decisive factor of the tool life [4].
Tool life is an important practical consideration in selecting cutting tools and cutting
conditions. Tool wear and fracture rates directly influence tooling costs and product quality.
Due to these reasons tool life is the most common criterion used to rate cutting tool
performance and the machinability of materials.
In 1977 the International Standards Organization (ISO) introduced the ISO: 3685 [60],
aiming at unifying tool life testing procedures and measured parameters in turning. The
standard defines tool life as the time elapsed until a definite amount of wear has occurred in
the rake face or flank of the cutting tool. This parameter is less useful in practical terms, as it
does not provide information about has many good pieces can be produced, but it provides
definition of tool life, which is independent of workpiece geometry and quality requirements.
More standards followed in 1989, covering tool life testing procedures in face milling and
end milling and a revised edition of ISO: 3685 appeared in 1993 [61]. The aim of these
standards is to unify testing procedures in order to increase reliability and comparability of
test results when making comparisons of cutting tools, work materials, cutting parameters,
cutting fluids, treatments given to cutting tool materials etc.
Tool life of a cutting tool is dependent on various factors such as tool material, process
parameters, tool geometry, work material, cutting fluid and treatments given to cutting tool
materials.
2.3.7 Literature review on tool wear and tool life models:
Various researchers have made efforts to optimize tool life of tools using different
optimization techniques. Taguchi’s orthogonal array technique also has been made use of for
optimizing process parameters to yield higher tool life or lower tool wear. Also efforts have
been made to optimize process parameters used during turning operation to have lowest
values of surface roughness. The response obtained and the input parameters were used to
find out relationship between them using regression analysis.
35
S.K. Choudhary et. al.[1] developed an empirical mathematical model for measurement of
tool wear using cutting parameters such as cutting speed, feed, depth of cut and the force
ratio in case of turning operation. A series of experiments were conducted using C45
workpieces and HSS tool. The mathematical model developed is
w = 0.324 (Ft / Fc) 0.601 + 0.000003N 1.623 f 0.912 d 1.162 D 1.01
where w is flank wear in mm, Ft trust force in N, Fc is cutting force in N, N spindle
revolutions, f is feed in mm/rev, d is depth of cut in mm and D is diameter of work in mm.
This model clearly depicts that flank wear of the tool is a function of cutting speed (as V is
dependent on N and D), feed and depth of cut parameters used in turning operation. Wear
from this experimental model developed was compared with experimental wear values,
which showed a good agreement.
Dragos A. Axinte et. al. [62] proposed a method to allow an experimental determination of
the extended Taylor’s equation with a limited set of experiments and to provide a basis for
the quantification of tool life measurement uncertainty. The model proposed by them is
TL = f (Cp, f, V, VB) = G apa f b V c VB d
where TL is tool life in min, ap is depth of cut in mm, f is feed in mm/rev, V cutting speed in
m/min, VB is flank wear in mm. G, a, b, c and d are constants, which were found out by
regression analysis for different cutting fluids. The method was applied for evaluation of
efficiency of cutting fluid efficiency in turning. Experiments were run in a range of cutting
parameters, according to a 2 3–1 factorial design, machining AISI316L stainless steel with
coated carbide tools. An extended Taylor’s equation for each fluid was found from regression
analysis.
In another research, S. K. Choudhary et. al. [63] used an optimization technique for
machining EN 24 and HSC materials with HSS tool. The cutting speed and feed values were
optimized for a given metal removal rate. The optimized values of cutting parameters showed
sustained improvement in tool life for both work materials. The models proposed for tool
wear of HSS tool with HSC and EN 24 materials respectively are as follows:
hf = 6.64.10-3 V 1.69 f 1.77 t 0.96 and
hf = 5.45.10-4 V 1.86 f 1.36 t 0..87
where hf is height of flank wear of tool, V is cutting speed in m/min, f is feed in mm/rev and t
is machining time in min. This indicates that tool wear is a function of process parameters
and machining time.
36
A.M.A. Al-Ahmari [64] has established empirical models for tool life, cutting force and
surface roughness based on turning experiments. The developed machinability models can be
utilized to formulate an optimization model for the machining economic problem to
determine the optimal values of process parameters for the selected material. Data of 28
experiments when turning austenitic AISI 302 have been used to generate, compare and
evaluate the proposed models of tool life, cutting force and surface roughness for the
considered material.
Mozher [65] conducted 28 experiments on austenitic AISI 302 material having 50 mm
diameter and 500 mm length. He considered four machining parameters (cutting speed (v,
m/min), feed rate (f, mm/rev), depth of cut (d, mm) and tool nose radius (r, mm)). The
considered outputs were tool life (T, min), cutting force (Fc, N) and surface finish (Ra, µm).
The experiments have been done on 16K20 lathe machine using throw away carbide inserts
IN.2, IN.3 and IN.4 based on the design levels of tool nose radius with tool holder T2. He
constructed three models of tool life, cutting force and surface finish using RA technique and
the logarithmic transformation of their first order models and evaluated these models using
the analysis of lack of fit. The model obtained for tool life is as follows:
T = 406.423 r0.038/ v1.051 f 0.289 d 0.219
Guey Jiuh Tzou et. al. [66] used Nickel base super alloy Inconel 718 as a work material for
optimizing cutting parameters for turning operation. Using Taguchi’s L18 Orthogonal Array
cutting speed, feed, different cutting tool inserts, working temperature and ultrasonic power
parameters were optimized. Flank wear of the tools was the response variable. S/N analysis
and ANOVA were employed for optimizing the parameters, which were confirmed by
carrying out confirmatory test.
Non-linear regression analysis techniques were used by S.E. Oraby et. al. [67] for
establishing models for wear and tool life determination in terms of the variation of a ratio of
force components acting at the tool tip. The ratio of the thrust component of force to the
power, or vertical, force component has been used to develop models for (i) its initial value
as a function of feed, (ii) wear and (iii) tool lifetimes. Predictions of the latter model have
been compared with the results of experiments, and with predictions of an extended Taylor
model. In all cases, good predictive capability of the model has been demonstrated. It is
argued that the models are suitable for use in adaptive control strategies for centre lathe
turning.
37
In work carried out by Yahya Isik [68] a series of tests were conducted in order to determine
the machinability of tool steels. In these tests the effects of tool material, type of coating on
the insert (for coated tools) and the cutting parameters that affect the machinability were
taken into considerations. The cutting force data used in the analysis were gathered by a tool
breakage detection system that detects the variations of the cutting forces measured by a
three-dimensional force dynamometer. The workpiece materials used in the experiments
were cold work tool steel AISI O2, hot work tool steel AISI H10 and mould steel AISI
improved 420. The cutting tools used were HSS tools, uncoated WC and coated TiAlN and
TiC + TiCN + TiN inserts (ISO P25). No cutting fluid was used during the turning
operations. During the experiments cutting forces, flank wear and surface roughness values
were measured throughout the tool life and the machining performance of tool steels were
compared. As a result of the experiments conducted. The conclusions concerning the tool life
are as follows:
• Cutting speed (V) is the most influential parameter on tool life, feed rate (f) is the
second most one, and cutting depth (d) is the least influential parameter. The
influence of cutting depth is negligible compared with those of the other cutting
parameters
• At the end of the tool life, considerable increase in cutting forces (Fs) is observed, but
the increase rate varies according to the cutting tool and the workpiece
• The amount of flank wear and the cutting force are appropriate parameters to
determine the tool life
• Prediction of tool wear becomes possible on condition that the cutting speed range,
recommended for the tools, is employed.
Theoretical and experimental studies were carried out by X. Luo et. al. [69] for investigating
the intrinsic relationship between tool flank wear and operational conditions in metal cutting
processes using carbide cutting inserts. A new flank wear rate model, which combines
cutting mechanics simulation and an empirical model, is developed to predict tool flank wear
land width. A set of tool wear cutting tests using hard metal coated carbide cutting inserts
were performed under different operational conditions. The wear of the cutting inset was
evaluated. The results of the experimental studies indicate that cutting speed has a more
dramatic effect on tool life than feed rate. The wear constants in the proposed wear rate
model are determined based on the machining data and simulation results. A good agreement
38
between the predicted and measured tool flank wear land width show that the developed tool
wear model can accurately predict tool flank wear to some extent.
In a research work carried out by E. Usui et. al. [70] an analytical method is presented, which
enables the crater and flank wear of tungsten carbide tools to be predicted for a wide variety
of tool shapes and cutting conditions in practical turning operations based only on orthogonal
cutting data from machining and two wear characteristic constants. A wear characteristic
equation is first derived theoretically and verified experimentally. An energy method is
developed to predict chip formation and cutting forces in turning with a single-point tool
from the orthogonal cutting data. Using these predicted results, stress and temperature on the
wear faces can be calculated. Computer simulation of the development of wear is then
carried out by using the characteristic equation and the predicted stresses and temperatures
upon the wear faces. The predicted wear progress and tool life are in good agreement with
experimental results.
Hong-Tsu Young [71] carried out work on workpieces made of annealed carbon steel AISI
1045. The wokpieces were machined on a lathe. The cutting speed and depth of cut used in
turning operation were 100 m/min and 1.3 mm respectively. Tool wear was measured using
tool maker’s microscope. The graph plotted between tool verses chip back maximum
temperature indicted that as chip back maximum temperature increased, flank wear of tool
increased. Thus, it was concluded that tool wear is strongly temperature dependent.
F. Boud [72] performed experiments in single point turning. Factors such as cutting speed,
feed rate, tool material, etc. are well known to have an effect on tool wear in metal turning.
He performed experiments on solid carbon steel, by using uncoated HSS insert for studying
effect of bar diameters on tool wear. All experiments were performed under identical cutting
conditions, i.e. cutting speeds were constant as well as the feed rate and depth of cut, also the
same bar was used except for varying the bar diameter. The findings are analyzed in three
separate ways. The conclusion of the research work is that bar diameter has an influence on
tool temperature and, by implication, on tool wear. Thus, a factor not previously considered
in wear theories in turning is shown to be significant.
Lee et. al. [73] carried out work for obtaining the optimal tool life with the ratio of cutting
speed to flank wear value. He claimed that the results have shown a good correlation between
the dynamic tangential force and flank wear.
39
In a research work P. Vamsi Krishna et. al. [74] conducted cutting tests under dry, wet and
solid lubricant conditions to study the process performance in terms of cutting forces, tool
wear, tool temperature and surface roughness in turning. For this purpose, cemented carbide
tool and EN8 steel workpiece were selected. The cutting tests were performed on PSG-124
lathe. Process parameters selected for turning were cutting velocity 110 m/min, feed rate 0.25
mm/rev and depth of cut 1.0 mm. One of the conclusions of the work is that cutting forces
and tool flank wear are reduced because of the formation of a boric acid film on the surfaces.
Thus tool wear is affected by cutting fluid used in turning operation.
Yong Huang et. al. [75] evaluated tool performance as a function of cutting conditions based
on the flank wear criterion using the calibrated tool wear model in finish turning of hardened
52100 bearing steel. A satisfactory match has been reached when comparing model
predictions and experimental measurements. Further, an analysis of variance was carried out
to investigate statistical significance among cutting conditions, and it shows that cutting
speed plays a dominant role in determining the tool performance in terms of tool life,
followed by feed and depth of cut, and overall tendencies agree with predictions from the
general Taylor tool life equation as well as experimental observations.
Kaye et. al. [76] developed a technique for on line prediction of the tool flank wear in turning
using the spindle speed change. A series of cutting tests were performed by them using
various combinations of cutting speed, feed rate, depth of cut and material hardness. It was
concluded that the predictions from the developed model are in well agreement with actual
flank wear measurements.
Alakesh Manna et. al. [77] worked on E0300 alloy steel for optimizing the cutting
parameters such as cutting speed, feed and depth of cut. Three levels of each parameter were
used to find out the surface roughness of the materials and using Taguchi’s approach the
cutting parameters were optimized to yield higher surface finish quality. An empirical
mathematical model for surface roughness due to cutting parameters was evolved and
confirmed.
Sumit Kanti Sikdar et. al. [78] carried out turning operation using CNMG120412N-UJ
inserts for cutting low alloy steel AISI 4340. Flank wear surface area was measured with
help of surface texture instrument. Cutting forces were measured with help of kislter piezo
40
electric dynamometer. Mathematical model between tool flank wear area and components of
cutting forces was developed.
In a research carried out by C. Y. Nian et. al. [79] proved the optimization of multiple
performance characteristics in turning S45C steel bars. Cutting parameters i.e. cutting speed,
feed and depth of cut values selected each at three levels were optimized to give better
surface finish, lower cutting force and higher tool life i.e. lesser tool wear by using Taguchi’s
L27 array.
E Daniel Karby [80] carried out turning operations on a CNC lathe using VNE versa Turn
CCGT 432 –AF inserts for turning steel bars using Taguchi’s L8 OA. The selected
parameters were feed at four levels, speed at two levels and depth of cut at two levels. The
S/N analysis and ANOVA techniques were used to optimize these parameters to yield lower
value of surface finish. Confirmation test for optimum and one of the non optimum
conditions were conducted and robustness of parameters optimization was experimentally
verified.
The brief review as discussed above, of the literature available on tool wear / tool life models
developed for the cutting tools by researchers indicate that tool wear is a criterion used for
judging the life of the tool. Tool wear is a function of the temperature developed in
machining zone, except the initial wear due to plastic deformation. The wear of the tool
increases as temperature developed in machining zone increases. In uniform wear rate zone
the temperature of machining zone is basically function of cutting process parameters i. e.
cutting speed, feed ,depth of cut , cutting fluid used, tool geometry, tool and work material
etc. In case of process parameters cutting speed is the predominant factor for the increase in
machining zone temperature followed by feed and depth of cut. The properties of tool
material such as hardness, red hardness, wear resistance etc. also play an important role in
variation of tool wear.
From the observations of the literature referred above on the cryogenic treatment effect on
material properties, especially tool steel and tool wear as a function of process parameters
and treatment provided to the tool materials, objectives of the present research are finalized.
These observations and objectives of proposed work are discussed in the next section.
41
2.4 Observations and Objectives:
The literature available on effect of cryogenic treatment on properties of materials indicates
that no systematic procedure has been followed by the researchers for studying effect of
cryogenic treatment on different materials. The temperature levels selected, soaking time
used during treatment even for the same material by various researchers varies a lot. Due to
this, the results obtained by various researchers match on gross level but minute details of the
effect are not worked out by the researchers.
Majority of the research carried out on tool steels for studying the effect of cryogenic
treatment is mainly concentrated on either M2 tool steel or die steel i.e. D2. There is very
little research carried out on T series tool steels for effects of cryogenic treatment.
The approach used by all researchers is basically oriented in metallurgical manner i. e. to
trace out the reasons for improvement/reduction in properties of material due to cryogenic
treatment. No efforts are observed to have a mathematical approach in evaluation of the
improvement / reduction in properties of the material due to cryogenic treatment. Therefore,
an attempt is made to develop empirical mathematical models for the first time for T42 tool
steel.
In order to meet out the gap in the available literature; in this present experimentation the
study is undertaken in following manner. These steps are already identified as objectives and
are mentioned in chapter 1.
• Pilot experiments shall be carried out with T42 HSS samples for studying effect
of cryogenic treatment on wear of the tools.
• A mathematical model for wear of the tool with respect to process parameters
such as cutting speed, feed and depth of cut shall be proposed.
• A mathematical model for wear of the tool with respect to cryogenic treatment
temperature, cutting speed, feed and depth of cut shall be proposed.
• To find out the effect of cryogenic treatment on wear properties of the tool by
comparing the two models proposed above.
• Experimentation as per Taguchi’s Orthogonal Array shall be carried out for
conventionally treated T42 HSS tools.
• Experimentation as per Taguchi’s Orthogonal Array shall be carried out for
cryogenically treated T42 HSS tools.
42
• An empirical mathematical model shall be evolved using regression analysis for
evaluating wear of conventionally treated tools using the data obtained from non
cryo tools experiments.
• An empirical mathematical model shall be evolved using regression analysis for
evaluating wear of cryogenically treated tools using the data obtained from cryo
treated tools experiments.
• The effect of cryogenic treatment on wear properties of the tool will be found out
by comparing the two models developed as above (point 7 and 8 above).
• Nomogarphs shall be developed for tool wear of T42 tool steel with respect to
cryogenic treatment temperature, cutting speed, feed and depth of cut, which
can be used as a ready reckoner for predicting the tool wear.
Thus, after identifying the need, objectives of present work and methodology, the
mathematical model development is discussed in the chapter to follow, i. e. Process
Modeling.