The Relationship of Binder Delta Tc (ΔTc) & Other Binder Properties to
Mixture Fatigue and Relaxation
Gerald ReinkeMTE Services, Inc
Binder ETG MeetingMay 10, 2018
Fall River, MA
INTRODUCTION
• Great deal of information has been presented on the ΔTc parameter
• Not going to go into much detail about ΔTc or other parameters because that is not the focus of this presentation
• Goal is to show the relationship between binder and mix relaxation and measured properties of aged binders– R-Value, Glover-Rowe, cross over frequency, ΔTc, Tm-Critical
ΔTc Determination & Sources of Error1. ΔTc=(Ts-critical – Tm-critical) ✓2. To obtain an accurate value for ΔTc the BBR needs to be performed at enough
temperatures so thata. BBR stiffness values < 300 MPa and > 300 MPab. BBR m-values < 0.300 and > 0.300c. Extended aging of binders , high levels of RAP and/or RAS, the use of high levels of
additives such as REOB might require BBR testing at 3 or more temperatures ✓3. If BBR stiffness is less than ≈ 125 MPa when BBR m-value barely exceeds 0.300 then
generally a 3rd BBR test temperature will be required to meet the requirements of 2.a and 2.b ✓
4. If you perform BBR at 2 temperatures where stiffness is <200 MPa so that Tm-criticalwill be <0.300 and >0.300 you can end up with an incorrect Ts-critical ✓
5. Linear extrapolations based on 2 test temperature over 100 to 150°C can result in incorrect predictions. Not all binders are linear (m value) or log linear (S value) with temperature
When a binder exhibits a ΔTc of < -4 or -5 the S critical temperature increases at a substantially slower rate than does the m-critical temperature and this will necessitate the need for a 3rd BBR Test
Ts-Critical ΔTc=-7.2y = -0.5581x - 33.709
Tm-Critical ΔTc=-7.2y = -1.5581x - 33.709
Ts-Critical ΔTc=-2.5y = -1.02x - 28.229
Tm-Critical ΔTc=-2.5y = -2.0482x - 28.234
-40
-35
-30
-25
-20
-15
-10
-8 -7 -6 -5 -4 -3 -2 -1 0 1 2 3
S or
m C
ritic
al T
empe
ratu
res
ΔTc
Rate of Change of ΔTc Depending on Binder Composition and Aging Severity
PG 64-22 + 20% Shingle Binder, 5% REOB, SCritical PG 64-22 + 20% Shingle Binder, 5% REOB, m-CriticalPG 64-22 SCritical PG 64-22 m-CriticalLinear (PG 64-22 + 20% Shingle Binder, 5% REOB, SCritical) Linear (PG 64-22 + 20% Shingle Binder, 5% REOB, m-Critical)Linear (PG 64-22 SCritical) Linear (PG 64-22 m-Critical)
Unaged
20 hr. PAV
RTFO
Unaged
RTFO
40 hr. PAV
40 hr. PAV
20 hr. PAV
Slope Ts-Critical for ΔTc of -7 is 50% that of the binder with ΔTc of -2.5
Slope of Tm-Critical for ΔTc of -7.5°C is 75% that of the binder with ΔTc of -2.5
JUST WHAT IS ΔTc?1. Reasons that we should all know are ✓
a. As binders age they become more m-controlled; Tm-critical increases more rapidly than Ts-critical ✓
b. As binders become more m-controlled they are more brittle and lose ability to relax stress ✓
c. As pavements age they are more prone to cracking distress ✓d. As ΔTc becomes more negative pavements become more prone to top down
fatigue cracking ✓e. It may not appear intuitively obvious that a value derived from low temperature
testing should be associated with distresses that are associated with intermediate service temperatures ✓
f. Based on research, some of which goes back 50+ years, research has shown the connections between pavement surface distresses and several parameters the most recent of which is ΔTc ✓
ΔTc can quantify the aging propensity of a binder
WHY IS AN UNDERSTANDING OF ΔTc IMPORTANT?
IN THE FINAL ANALYSIS ΔTc, R-Value, GR COMES DOWN TO 1 THING
IN THE FINAL ANALYSIS ΔTc, R-Value, GR COMES DOWN TO 1 THING
NO! NOT THAT 1 THING
IN THE FINAL ANALYSIS ΔTc, R-Value, GR COMES DOWN TO 1 THING
NO! NOT THAT 1 THINGRELAXATION
IN THE FINAL ANALYSIS ΔTc, R-Value, GR COMES DOWN TO 1 THING
NO! NOT THAT 1 THINGRELAXATIONSPECIFICALLY BINDER
RELAXATION
TIME TO GET SERIOUS• As with most advances in technical research developments are
the result of cumulative increase in knowledge ✓• I will briefly reference the work of three individuals, but
reading their research will show many other contributors along the way
• Prithvi (Ken) Kandhal – Pennsylvania DOT Bituminous Engineer• Dr. Charles Glover—Research Professor Texas Transportation
Institute at Texas A&M• Mike Anderson—Director of Research at the Asphalt Institute
References1. Kandahl, Low Temperature Ductility in Relation to Pavement Performance, ASTM STP 628,
Marek, Ed., 19772. Glover, Charles J, Davison, Richard, Domke, Chris, Ruan, Yonghong, Juristyarini, Pramitha, Knorr,
Daniel, Jung, Sung, “Development Of A New Method For Assessing Asphalt Binder Durability With Field Validation”, FHWA/TX-05/1872-2, August 2005
3. Anderson, R. M, King, G.N., Hanson, D.I., Blankenship, P.B. "Evaluation of the Relationship between Asphalt Binder Properties and Non-Load Related Cracking." Association of Asphalt Paving Technologists, 2011 Volume 80, pp 615-663, 2011
4. TRB papers in 2010, 2011 and 2012 by Sui and Farrar, et al from Western Research Institutre5. EECongress in Istanbul, 2012, Farrar, et al
In the interest of time I have hidden several background slides which will be available when
this presentation is provided to the ETG members
Ductility and Pavement Condition of 1961 and 1962 Pennsylvania Pavements Reported by Kandhal (Kandhal 1977)
Ductility value at 60°F (15.5°C), 5 cm/min, cm
Pavement Condition Observed
More than 10 Satisfactory8 to 10 Loss of fines (matrix)5 to 8 Raveling3 to 5 Cracking, needs resurfacing
Less than 3 Very poor, extensive crackingSOME COMMENTS REGARDING KANDHAL’S WORK1. At 10 cm ductility there is no cracking reported, however when it takes longer than 3
years to reach 10 cm loss of fines and some raveling is noted2. Regardless of the time it takes to reach less than 5 cm of ductility that ductility value
is associated with the onset of cracking ✓
Extent of binder aging is the key factor and not the time of binder aging
What Can We Infer From This Data?• There is a point in the aging of a binder when cracking begins to
develop• Binder aging rate is not the same for every binder (crude source
impacts performance) or perhaps it is not the same time point for the same binder depending on the conditions of the job– Time of year constructed– % bitumen in the mix– Air voids – Aggregate type and/or gradation– Other factors e.g. RAP, RAS, polymer or ???
• Extent of Binder Aging is the Key Driver• How can we age binders and mixtures sufficiently in the lab to
tell us something useful about long term performance?
Taken from Glover, et al 2005, plot shows1. Linear correlation between
G’/ η’/G’ and 15°C ductility for ductility values < 10 cm✓
2. Based on Kandhal’s data when ductility drops below 10 pavement distress begins ✓
3. Glover used this data to develop relationship between ductility and binder rheology at 15°C ✓
4. Glover used time temperature superposition principles to adjust the DSR test to 44.7°C and 10 rad/sec ✓
NOTE: ALL THESE ARE CONVENTIONAL BINDERS
Moving from Ductility to ΔTc• Mike Anderson, et al AAPT 2011—introduced ΔTc concept ✓• Rheological & ductility of PAV binders and binders recovered from
aged airfield mixtures• Established Relationship of ΔTc to non-load associated distress• Key findings ✓
1) Glover @ Texas A&M had shown ductility @ 15°C & 1 mm/min correlated to long term pavement distress ✓
2) G’/(η’/G’) correlated to ductility @ 15°C & 1 mm/min ✓3) Also showed G’/(η’/G’) correlated to ΔTc (difference between the BBR Tm-
critical – BBR Ts-critical ✓
4) ΔTc of 2.5°C = cracking warning limit, ΔTc = 5°C point where binder durability lost ✓
ΔTc and 4 mm DSR Testing
• Much of the data to be discussed next was generated at MTE using a 4 mm DSR test developed at Western Research Institute (see reference list)
• Requires very little material to perform test ✓• Results correlate well to BBR, but there is a learning curve ✓• Provides a broader temperature range (-36°C to +30°C or
+40°C) of data collection in less time than BBR test at 3 temperatures ✓
The size advantages are obvious for performing tests on field samples and other forensic workWhen the main mixture layer that needs testing is binder recovered from the top ½ inch of a 6 inch diameter core very little binder is obtained and the 4 mm test requires only one core to provide sufficient binder for a 25 mm and 4 mm test
Just How Does ΔTc Relate to Mix Performance?• Need to get back to RELAXATION• As binders age their ability to relax stress diminishes ∴ BBR
result becomes increasingly m-controlled (poor relaxation) ✓• Some binders have inherently poor relaxation properties, BBR
will show this and ΔTc can quantify impact of poor relaxation✓
• Relaxation is not just a low temperature (i.e. sub 0°C) problem– Ductility decreases when binder cannot relax fast enough to prevent
the binder thread from breaking (Kandhal & Glover at 15°C)– The DSR data shows similar behavior (Glover’s DSR vs Ductility Plot
another test performed at 15°C)
Just How Does ΔTc Relate to Binder Relaxation and Ultimately Mix Performance?
• How many of you have really looked at or compared the BBR data plot for different binders?
• BBR test is not just a single data point at 60 seconds• In that plot is the story of how the binder relaxes (or doesn’t) due
to the imposition of load
100.0
1,000.0
10 100 1000
BBR
Stif
fnes
s, S
(t),
& 4
mm
Stif
fnes
s G
(t),
MPa
Reduced Time, sec's
BBR S(t) mastercurve @ -18° Ref Temp, Binder A, ΔTc = -5°C
BBR S(t) mastercurve @ -18° Ref Temp, Binder B, ΔTc= 1°C
Relaxation time = 60 seconds
60
COMPARISON OF BBR MASTERCURVES @ -18°C FOR TWO DIFFERENT BINDERS
If you only look at the 60 second results from the BBR test you are blind to the relaxation behavior of the binder
1. If you only focus on the slope at 60 seconds you will see a difference, but it is just a comparison of 2 numbers
2. When you look at the complete BBR mastercurve you see how much more readily the binder with a ΔTc of 1°C relaxes stress compared to the binder with a ΔTc of -5°C
10.0
100.0
1,000.0
10,000.0
0.001 0.01 0.1 1 10 100 1000 10000 100000 1000000
BBR
Stif
fnes
s, S
(t),
& 4
mm
Stif
fnes
s G
(t),
MPa
Reduced Time, sec's
BBR S(t) mastercurve @ -18° Ref Temp, Binder A, ΔTc = -5°C
BBR S(t) mastercurve @ -18° Ref Temp, Binder B, ΔTc= 1°C
Relaxation time = 60 seconds
COMPARISON OF BBR MASTERCURVES @ -18°C FOR TWO DIFFERENT BINDERSCOMMENTS1. Binder sample A has a ΔTc of
-5°C compared to sample B with a ΔTc of +1.
2. The important point is that sample A relaxes the same applied load over the same time period at slower rate than sample B
1. When you incorporate the 4 mm data for the same binders similar ΔTc results are obtained, but you also observe how the relaxation disparity carries over to longer relaxation times
2. Longer relaxation times are a surrogate for relaxation behavior at warmer temperatures
1.0E-05
1.0E-04
1.0E-03
1.0E-02
1.0E-01
1.0E+00
1.0E+01
1.0E+02
1.0E+03
1.0E+04
1.00E-06 1.00E-04 1.00E-02 1.00E+00 1.00E+02 1.00E+04 1.00E+06 1.00E+08 1.00E+10
BBR
Stif
fnes
s, S
(t),
& 4
mm
Stif
fnes
s G
(t),
MPa
Reduced Time, sec's
BBR S(t) mastercurve @ -18° Ref Temp, Binder A, ΔTc = -5°C
BBR S(t) mastercurve @ -18° Ref Temp, Binder B, ΔTc= 1°C
4 mm DSR ,G(t) mastercurve @ -18°C Ref Temp, Binder A, ΔTc= -4.9°C
4 mm DSR ,G(t) mastercurve @ -18°C Ref Temp, Binder B, ΔTc= 0.6°C
Relaxation time = 60 seconds
COMPARISON OF BBR & 4 mm MASTERCURVES @ -18°C FOR TWO DIFFERENT BINDERS
If binders have a relaxation disparity at low temperatures they also have a relaxation disparity at warmer temperatures
An additional benefit of the 4 mm test is the ability to examine the binder’s behavior at temperatures beyond those capable by the BBR
1.0E-05
1.0E-04
1.0E-03
1.0E-02
1.0E-01
1.0E+00
1.0E+01
1.0E+02
1.0E+03
1.0E+04
1.00E-13 1.00E-10 1.00E-07 1.00E-04 1.00E-01 1.00E+02 1.00E+05 1.00E+08 1.00E+11
BBR
Stif
fnes
s, S
(t),
& 4
mm
Stif
fnes
s G
(t),
MPa
Reduced Time, sec's
BBR S(t) mastercurve @ -18° Ref Temp, Binder A, ΔTc = -5°CBBR S(t) mastercurve @ -18° Ref Temp, Binder B, ΔTc= 1°C4 mm DSR ,G(t) mastercurve @ -18°C Ref Temp, Binder A, ΔTc= -4.9°C4 mm DSR ,G(t) mastercurve @ -18°C Ref Temp, Binder B, ΔTc= 0.6°C4 mm DSR ,G(t) mastercurve @ 25°C Ref Temp, Binder A, ΔTc= -4.9°C4 mm DSR ,G(t) mastercurve @ 25°C Ref Temp, Binder B, ΔTc= 0.6°CRelaxation time = 60 seconds
COMPARISON OF BBR & 4 mm MASTERCURVES @ -18°C & 25°C FOR TWO DIFFERENT BINDERS
1.00E+00
1.00E+01
1.00E+02
1.00E+03
1.00E+04
1.00E+05
1.00E+06
1.00E+07
1.00E+08
1.00E+09
1.00E+10
1.00E-04 1.00E-02 1.00E+00 1.00E+02 1.00E+04 1.00E+06 1.00E+08 1.00E+10 1.00E+12 1.00E+14
Com
plex
She
ar M
odul
us, P
a
REDUCED FREQUENCY, rad/sec
Comparison of G* Moduli @ 25°C of 40 hour PAV residues Showing Greater R-Value for Binder That has lower crossover frequency
G* MN1-4, PG 58-28, 40 hr. PAV G* MN1-5, PG 58, 40 hr PAVMN1-4 Crossover Frequency MN1-5 Crossover Frequency
R-Value forMN1-4
R-Value forMN1-5
Illustration of Determination of R-Value (Rheological Index)1. MN1-5 binder
performed the best and has the lowest R-value
2. MN1-4 performed the worst and has the highest R-value
R = Log(Glassy modulus) – Log at G* at the crossover frequency)For practical purposes the Glassy modulus is 1 x 109 PascalsCrossover frequency is where phase angle = 45°As a binder’s ability to relax stress diminishes the binder stiffness must decrease to achieve a phase angle of 45°. As a result the R-value increases
The R-Value is another way to quantify binder relaxation by comparing the shear modulus (G*) mastercurves The method of determining
the R-value from rheological data is summarized at the left
A graphical presentation of R-Value is shown in the difference in length for the 2 sets of brackets
SOME FIELD EXAMPLES• I’ve presented this information at AI and other places such
as ETG meetings, ∴ I will only provide a couple brief comments
COMPARATIVE CRUDE SOURCE STUDY
• CTH 112 Olmsted Cty, MN; 2006 construction• 3 virgin test sections to compare 3 different crude sources of
PG 58-28 binder (MN1-3, MN1-4, MN1-5)• 1 virgin PG 58-34 PMA binder (MN1-2)• Project specified mix of a PG 58-34 + 20% RAP (MN1-1)• Substantial surface cracking began to show up between
years 4 and 5
Mathy Technology & Engineering27
28
MN1-2
MN1-3
MN1-4
MN1-5MN1-2MN1-3
MN1-4MN1-5
y = -54.788x + 151.08R² = 0.9638
y = -4.1875x + 16.721R² = 0.6744
y = -50.601x + 134.36R² = 0.9349
0.0
100.0
200.0
300.0
400.0
500.0
600.0
-7.0 -6.0 -5.0 -4.0 -3.0 -2.0 -1.0 0.0 1.0 2.0
DIS
TR
ESS
DAT
A, 2
014
SUR
VE
Y, m
eter
ΔTc OF BINDER RECOVERED FROM TOP 1/2 INCH OF 2014 CORES
Total Distress = F(ΔTc from Top 1/2''); Transverse Cracks = F(ΔTc from Top 1/2'') & (Total Distress-Transverse Cracks)=F(ΔTc from Top ½’’ Recovered
Binder)
Total Distress = F(ΔTc of Binder from Top 1/2'') Total Transverse = F(ΔTc of Binder from Top 1/2'')
(Total Distress-transverse) = F(ΔTc of Top 1/2'' Binder) Linear (Total Distress = F(ΔTc of Binder from Top 1/2''))
Linear (Total Transverse = F(ΔTc of Binder from Top 1/2'')) Linear ((Total Distress-transverse) = F(ΔTc of Top 1/2'' Binder))
Transverse cracking does not correlate well with change in ΔTc, but Total Distress and Total Distress-Transverse cracking are well correlated to ΔTc
Mathy Technology & Engineering
Olmsted County, MN CTH 112, 2014 (8 yrs) COMMENTS1. ΔTc does not
correlate well with transverse cracking
2. transverse cracking level is similar for all mixes, but ΔTc varies widely
3. Substantial difference in top down cracking in the test sections does correlate well with ΔTc
Relationship of Cracking to Binder Relaxation
• For purposes of my objective in this discussion the next few slides are more important than looking at ΔTc plots correlated to cracking
1.0E+00
1.0E+01
1.0E+02
1.0E+03
1.0E+04
1.0E+05
1.0E+06
1.0E+07
1.0E+08
1.0E+09
1.0E+10
1.0E-13 1.0E-11 1.0E-09 1.0E-07 1.0E-05 1.0E-03 1.0E-01 1.0E+01 1.0E+03 1.0E+05
Rela
xatio
n M
odul
us, G
(t),
Log
Scal
ed
Reduced time, Log ScaledG(t) @15°C 1478, 08-27-14-D, MN1-5, 58-28, 40 HR. PAV, 4mm, G(t) @15°C 1478, 08-27-14-E, MN1-3, 58-28, 40 HR. PAV, 4mm
G(t) @15°C MN1-4, 58-28, 07-10-14-D, 40 HR. PAV, 4mm
MN1-5ΔTc=+0.8°C
MN1-3ΔTc= -4.2°C
MN1-4ΔTc= -7.6°C
Reduced Time VS Relaxation Modulus @ 15°C for MN1-3, MN1-4, MN1-5 of 40 hour PAV Residue
COMMENTS1. MN1-3 & MN1-5
have greater relaxation moduli than MN1-4 at short relaxation times
2.HOWEVER3. MN1-4 relaxes
stiffness so slowly that at extended time it intersects MN1-3
-1.4
-1.2
-1
-0.8
-0.6
-0.4
-0.2
0
-11 -10 -9 -8 -7 -6 -5 -4 -3 -2 -1 0 1 2 3 4 5 6
Slop
e of
Log
redu
ced
time
vs. R
elax
atio
n M
odul
us d
ata
Log Reduced time
Log Reduced Time VS. Slope (m vlaue) of Relaxation Modulus
slope MN1-5, 40 HR PAV RESIDUE slope MN1-3 40 HR. PAV RESIDUE slope MN1-4 40 HR. PAV RESIDUE
MN1-5ΔTc=+0.8°C
MN1-3ΔTc= -4.2°C
MN1-4ΔTc= -7.6°C
COMMENTS1. The first derivative of
relaxation modulus curves show more clearly what is happening
2. The 1st derivative plot is the same as determining the m-value at every point along the relaxation modulus mastercurve
3. The slope of MN1-3 decreases at a faster rate than the slope of MN1-4 and the slope of MN1-5 decreases at the fastest rate of all.
4. This rate of relaxation emphasizes the interrelation of relaxation slope and level of ΔTc
1.0E+00
1.0E+01
1.0E+02
1.0E+03
1.0E+04
1.0E+05
1.0E+06
1.0E+07
1.0E+08
1.0E+09
1.0E+10
1.0E-08 1.0E-06 1.0E-04 1.0E-02 1.0E+00 1.0E+02 1.0E+04 1.0E+06 1.0E+08 1.0E+10 1.0E+12
RELA
XATI
ON
MO
DU
LUS,
G(t
), Pa
REDUCED TIME, SECONDS
G(t) @-18°C MN1-2 (PMA), 8 yr core Top ½ in, 4mm G(t) @-18°C MN1-1, 8 yr core Top ½ in, 4mm
G(t) @-18°C MN1-4, 8 yr core Top ½ in, 4mm G(t) @-18°C MN1-3, 8 yr core Top ½ in, 4mm
G(t) @-18°C MN1-5, 8 yr core Top ½ in, 4mm
Reduced Time VS Relaxation Modulus @ -18°C of Recovered Binder from Top ½ inch of8 year Field Cores of MN1-1, MN1-2, MN1-3, MN1-4, MN1-5
COMMENTS1. Plot is of relaxation
moduli of binders recovered from the top ½ inch of 8 year field cores
2. The 3 PG 58-28 binders have relaxation moduli plots that reflect their ΔTc values;
3. The plots of MN1-1 and MN1-2 (PMA binder) appear to have worse relaxation moduli even though they have the 2nd
& 3rd best ΔTc values
ΔTc Binder Recovered from top 1/2'' of 8 Year Old Field
CoresSample
IDBinder Grade ΔTc
MN1-158-34 +20%
RAP -2.5
MN1-2PG 58-34
PMA -1.1MN1-3 PG 58-28 -3.0MN1-4 PG 58-28 -6.4MN1-5 PG 58-28 1.5
MN1-4, ΔTc= -6.4
MN1-3, ΔTc= -3.0
MN1-5, ΔTc= +1.5
-0.5
-0.45
-0.4
-0.35
-0.3
-0.25
-0.2
-0.15
-0.1
-0.05
0
-8 -6 -4 -2 0 2 4 6
SLO
PE O
F RE
LAXA
TIO
N M
OD
ULU
S M
AST
ERCU
RVE
LOG of REDUCED TIME
1st Derivative of Relaxation Modulus Mastercurves @ -18°C Versus Log of Reduced Time @ 60 seconds
Slope G(t) @-18°C MN1-4, 8 yr core Top ½ in, 4mm Slope G(t) @-18°C MN1-2 (PMA), 8 yr core Top ½ in, 4mm
Slope G(t) @-18°C MN1-1, 8 yr core Top ½ in, 4mm Slope G(t) @-18°C MN1-3, 8 yr core Top ½ in, 4mm
Slope G(t) @-18°C MN1-5, 8 yr core Top ½ in, 4mm LOG OF 60 SECONDS
TEST SECTION
Slope_at_-18°C & 60
sec
MN1-1 -0.2541MN1-2 -0.2957MN1-3 -0.2634MN1-4 -0.24845MN1-5 -0.2911
COMMENTS1. This is a zoomed plot of the
slope of the relaxation modulus mastercurve vs log of reduced time for all 5 CTH 112 binders
2. MN1-1 starts out at a slightly lower relaxation modulus than MN1-5, but relaxes more slowly and by 60 seconds is relaxing at a slower rate than MN1-2
3. MN1-4 which has the lowest relaxation modulus at short times relaxes so slowly that it eventually crosses over all of the other binders and has the worst slope of all materials
Relationship of Tm-Critical to Several Parameters
MN1-1
MN1-2
MN1-3
MN1-4
MN1-5
y = 108.57x + 2.3376R² = 0.9829
-34
-33
-32
-31
-30
-29
-28
-27
-26
-25
-24
-0.3 -0.29 -0.28 -0.27 -0.26 -0.25 -0.24
Tm-C
ritic
al, °
C
Slope of Relaxation Modulus at 60 seonds, -18°C
Tm-critical = F(slope @ -18°C), for top 1/2'' Recovered Binder
Low temp grade is controlled by Tm-critical for all bindersIt is logical that the slope of the binder relaxation modulus at 60 seconds is strongly corelated to the low temperature binder grade because the Tm-
critical value is derived from the 60 second slope values.However, it is not as obvious that relaxation modulus slopes for PMA, RAP and plain binders would all plot on the same correlation line versus Tm-criticalespecially when ΔTc and Tm-Critical are not strongly correlated for the same binders
MN1-1
MN1-2
MN1-3MN1-4
MN1-5
y = -0.6866x - 28.679R² = 0.6456
-34
-32
-30
-28
-26
-24
-22
-20
-7 -6 -5 -4 -3 -2 -1 0 1 2
Tm-C
ritic
al, °
C
ΔTc of the Binder
Tm-critical = F(ΔTc), for top 1/2'' Recovered Binder
ΔTc does not strongly correlate to the binder low temperature grade
MN1-158-34
20% RAPCanadian
MN1-258-34PMA
Canadian
MN1-358-28
Canadian
MN1-458-28
Mid East + REOB
MN1-558-28
Venezuelan
-32
-30
-28
-26
-24
-22
-20
0 50 100 150 200 250
T m-c
ritic
al
Glover-Rowe
Tm-critical=F(Glover-Rowe)
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5y = -4.1659x + 16.279R² = 0.6582
0
10
20
30
40
50
60
-7 -6 -5 -4 -3 -2 -1 0 1 2
Tran
sver
se C
rack
s (m
)
ΔTc
Transverse Cracks = F(ΔTc )
Transverse Cracks = F(ΔTc) Olmsted CTH 112 Crude Source Study
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5y = -4.1659x + 16.279R² = 0.6582
0
10
20
30
40
50
60
-7 -6 -5 -4 -3 -2 -1 0 1 2
Tran
sver
se C
rack
s (m
)
ΔTc
Transverse Cracks = F(ΔTc ) Even if you eliminate the polymer only (MN1-2) & polymer + RAP (MN1-1) data there is still not a linear correlation of transverse cracking with ΔTc
R2 was not determined, but it is easy to discern that there is no good correlation
Transverse Cracks = F(ΔTc) Olmsted CTH 112 Crude Source Study
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5
y = 488.81x + 158.4R² = 0.5519
0
10
20
30
40
50
60
-0.3 -0.29 -0.28 -0.27 -0.26 -0.25 -0.24
Tran
sver
se C
rack
ing,
m
Slope of Relaxation Modulus, -18C, 60 sec
Transverse Cracking (m) = F(slope of Binder Relaxation modulus, -18°C, 60 sec)
There is not a linear relationship between the slope of the binder relaxation modulusand the level oftransverse cracking
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5
y = 488.81x + 158.4R² = 0.5519
0
10
20
30
40
50
60
-0.3 -0.29 -0.28 -0.27 -0.26 -0.25 -0.24
Tran
sver
se C
rack
ing,
m
Slope of Relaxation Modulus, -18C, 60 sec
Transverse Cracking (m) = F(slope of Binder Relaxation modulus, -18°C, 60 sec)
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5
y = 488.81x + 158.4R² = 0.5519
0
10
20
30
40
50
60
70
-0.3 -0.29 -0.28 -0.27 -0.26 -0.25 -0.24
Tran
sver
se C
rack
ing,
m
Slope of Relaxation Modulus, -18C, 60 sec
Transverse Cracking (m) = F(slope of Binder Relaxation modulus, -18°C, 60 sec)
Y=14.013+7.15E16*Exp(-X/(-0.00706)
The exponential relationship fits the data, but I suspect that this functionreally fits the physical reality of transverse cracking as a function of binder relaxation modulus
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5
y = 488.81x + 158.4R² = 0.5519
0
10
20
30
40
50
60
-0.3 -0.29 -0.28 -0.27 -0.26 -0.25 -0.24
Tran
sver
se C
rack
ing,
m
Slope of Relaxation Modulus, -18C, 60 sec
Transverse Cracking (m) = F(slope of Binder Relaxation modulus, -18°C, 60 sec)
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5
y = 488.81x + 158.4R² = 0.5519
0
10
20
30
40
50
60
70
-0.3 -0.29 -0.28 -0.27 -0.26 -0.25 -0.24
Tran
sver
se C
rack
ing,
m
Slope of Relaxation Modulus, -18C, 60 sec
Transverse Cracking (m) = F(slope of Binder Relaxation modulus, -18°C, 60 sec)
Y=14.013+7.15E16*Exp(-X/(-0.00706)
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5
y = 488.81x + 158.4R² = 0.5519
y = 195.71x + 73.702R² = 0.7215
0
10
20
30
40
50
60
-0.3 -0.29 -0.28 -0.27 -0.26 -0.25 -0.24
Tran
sver
se C
rack
ing,
m
Slope of Relaxation Modulus, -18C, 60 sec
Transverse Cracking (m) = F(slope of Binder Relaxation modulus, -18°C, 60 sec)For the non-REOB binders the linear correlation between slope of the binder relaxation modulus and transverse cracking is reasonable. Keep in mind thatMN1-2 was a virginPMA PG 58-34 mix and MN1-1 was a 20% RAP mix with PG 58-34 binder. MN1-5 and MN1-3 were virgin PG 58-28 mixes. I think the most wecan conclude from thisdata is that binderrelaxation plays a rolein transverse cracking, but is certainly not the whole story
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5
y = 505.36x + 162.66R² = 0.5542
0
10
20
30
40
50
60
-0.3 -0.29 -0.28 -0.27 -0.26 -0.25 -0.24
Tran
sver
se C
rack
ing,
m
Slope of Relaxation Modulus, -18C, 60 sec
Transverse Cracking (m) = F(slope of Binder Relaxation modulus, -18°C, 60 sec)
Even if you eliminate the polymer only (MN1-2) & polymer + RAP (MN1-1) data there is still not a linear correlation of transverse cracking with Relaxation Modulus slope
R2 was not determined, but it is easy to discern that there is no good correlation
Transverse Cracks = F(Slope of Binder Relaxation Modulus) Olmsted CTH 112 Crude Source Study
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5
y = 5710x + 1761.4R² = 0.7915
y = 8523.2x + 2518.7R² = 0.9939
0
50
100
150
200
250
300
350
400
450
-0.3 -0.29 -0.28 -0.27 -0.26 -0.25 -0.24Tota
l Dis
tres
s = F
atig
ue a
rea
+ lo
ngitu
dina
l + T
rans
vers
e
Slope of Relaxation Modulus Mastercurve @ -18℃ & 60 sec
Total Distress (Excludes CL cracks)=F(Slope of Binder Relaxation Modulus, -18°C, 60 sec)
Total Distress (Non CL)=F(Slope of Relaxation Modulus, -18°C, 60 sec) all Binders
Total Distress (excludes CL)=F(slope of Binder Relaxation Modulus @ -18C, 60 sec PG 58-28 only)
Total Distress = F(Slope Binder Relaxation Modulus) Olmsted CTH 112 Crude Source Study
The relationship between total fatigue distress and the slope of the binder relaxation modulus master curve has a R2 value of 0.79for all binders, including the REOB binder mix MN1-4. Considering that this relationship includes the virgin PMA mix (MN1-2) and the 20% RAP containing PMA mix (MN1-1) this is a good result. When the PMA mixes are removed the relationship is nearly perfect. Both relationships indicate that binder relaxation plays a greater role in fatigue cracking than in transverse cracking
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5
y = 335.57x - 603.22R² = 0.6106
0
50
100
150
200
250
300
350
400
450
1 1.2 1.4 1.6 1.8 2 2.2 2.4 2.6 2.8 3Tota
l Dis
tres
s =
Fatig
ue a
rea
+ lo
ngitu
dina
l + T
rans
vers
e
R-Value Binder from top 1/2 inch of 8 year Field cores
Total Distress (Excluding Center Line Cracks) =F(R-Value of Binder from Top ½ inch of 8 year Field Core
There is not a good correlation of Total Distress as a function of Binder R-Value when the data for all mixes are evaluated
Total Distress = F(R-Value) Olmsted CTH 112 Crude Source Study
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5
y = 335.57x - 603.22R² = 0.6106
y = 393.42x - 705.98R² = 0.9052
0
50
100
150
200
250
300
350
400
450
1 1.2 1.4 1.6 1.8 2 2.2 2.4 2.6 2.8 3Tota
l Dis
tres
s =
Fatig
ue a
rea
+ lo
ngitu
dina
l + T
rans
vers
e
R-Value Binder from top 1/2 inch of 8 year Field cores
Total Distress (Excluding Center Line Cracks) =F(R-Value of Binder from Top ½ inch of 8 year Field Core
There is not a good correlation of Total Distress as a function of Binder R-Value; however when the polymer mix (MN1-2) and the polymer + RAP mix (MN1-1) data are removed there is a linear correlation with the non modified PG 58-28. Binder R-Values differ when polymer and/or reclaimed binders are included in the mix.The base binder for MN1-1 and MN1-2 are from the same crude source as MN1-3
Total Distress = F(R-Value) Olmsted CTH 112 Crude Source Study
MN1-1
MN 1-2
MN 1-3
MN 1-4
MN 1-5
y = -47.508x + 106.49R² = 0.9578
0
50
100
150
200
250
300
350
400
450
-7 -6 -5 -4 -3 -2 -1 0 1 2
Tota
l Dis
tres
s =
Fatig
ue a
rea
+ lo
ngitu
dina
l + T
rans
vers
e
ΔTc
Unlike relaxation modulus or other parameters such as R-Value, crossover frequency and Glover Rowe which are impacted by binder additives or crude source and therefore do not correlate well with pavement distress the ΔTc parameter appears to be blind to the presence of polymer or RAP when looking at the correlation to pavement performance.ΔTc may not correlate this well for all mixtures with a wide variety of binder types, but it appears it will always correlate better than other parameters.
Total Distress = F(ΔTc) Olmsted CTH 112 Crude Source Study
MnROAD TEST OF 3 BINDERS
1. CONSTRUCTED IN SEPT 19992. 3 BINDERS
a. PG 58-28b. PG 58-34c. PG 58-40
3. TRAFFICED UNTIL APRIL 20074. ANNUAL OR NEARLY ANNUAL PAVEMENT DISTRESS
SURVEYS CONDUCTED
Mathy Technology & Engineering
58-28
58-34
58-40
PG 58-28
PG 58-34
PG 58-40
0
200
400
600
800
1000
1200
1400
1600
1800
-9.0 -8.0 -7.0 -6.0 -5.0 -4.0 -3.0 -2.0 -1.0 0.0
Tota
l Cra
cks (
Non
CL
), fe
et
ΔTc, °C
4 Year Total Cracks (Non CL)= F(ΔTc @ 40 hr. PAV) 5.5 Year Total Cracks (Non CL) = F(ΔTc @ 40 hr.)
7.5 Year Total Cracks (Non CL) = F(ΔTc @ 40 hr. PAV)
Mathy Technology & Engineering
Total Crack Length (Non CL) @ years 4, 5.5 & 7.5 =F(ΔTc 40 hr PAV)
COMMENTS1. Between years 4 and 5.5 a
substantial increase in cracking took place for the PG 58-40 section. While the increases for the other 2 sections were not as severe they also showed an increase after 5.5 years
2. Regardless of the years in service, the cracking trended with the ΔTc of the 40 hour PAV residue.
3. No binder was recovered from field cores over the course of the project.
58-40REOB & PMA
58-34PMA
58-28Straight
0
200
400
600
800
1000
1200
1400
1600
1800
0 50 100 150 200 250
Crac
king
at 7
.5 y
ears
, Fee
t
Glover-Rowe, kPa
Cracking @ 7.5 yrs VS F(Glover-Rowe 40 hr. PAV)
MnRoad Comparative Binder Study
0.0518369258-40 REOB & PMA
0.886362258-28 Straight
0.166357558-34 PMA
0
200
400
600
800
1000
1200
1400
1600
1800
0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 1
Crac
king
Dist
ress
, Fee
t
Crossover Frequency
Cracking @ 7.5 yrs VS (Crossover Freq @15°C 40 hr. PAV)
MnRoad Comparative Binder Study
Evaluation of Relaxation of Mixes Aged for 10 and 20 Days @ 85°C
1. Six Mixturesa) PG 52-34 + 5% RAS, PG 52-34 + 5% ADD#1+5% RAS, PG 52-34 + 5%
ADD#1, 2.5% ADD#2 +5% RASb) PG 58-28 +5% RAS, PG 58-28 + 5% ADD#2 +5% RAS, PG 58-28 + 5%
ADD#3 +5% RAS
2. Binders recovered from aged mixes and characterized3. Relaxation modulus determined for mixes and binders4. Relationship between mixes and binders evaluated
1.00E+05
1.00E+06
1.00E+07
1.00E+08
1.00E+09
1.00E+10
1.00E+11
1.00E-13 1.00E-11 1.00E-09 1.00E-07 1.00E-05 1.00E-03 1.00E-01 1.00E+01 1.00E+03
RELA
XATI
ON
MO
DULU
S, G
(t),
Pa
REDUCED TIME, sec's
Log Relaxation Modulus (G(t)) vs Log Reduced Time for 10 day aged mix
MODEL: G(t) @25°C Summary 1531, 07-05-16-BA, 58-28 Straight, 4, 10d85MODEL: G(t) @25°C Summary 1531, 07-05-16-AU, 58-28 5% RS 1100 Arizona, 3, 10d85, RSSMODEL: G(t) @25°C Summary 1531, 07-05-16-AX, 58-28 5% Cargill 1103, 3, 10d85, RSSMODEL: G(t) @25°C Summary 1531, 07-05-16-AO, 52-34 Straight, 3, 10d85, RSSMODEL: G(t) @25°C Summary 1531, 07-05-16-AL, 52-34 w5% Sterol, 3, 10d85, RSS, HR3-3 (2)-3MODEL: G(t) @25°C Summary 1531, 07-05-16-AR, 52-34 5% Sterol 2.5 Cargill 1103, 3, 10d85, RSS
AO & AP PG 52-34 + 5% RAS
AL & AMPG 52-34 + 5% ADD#1+5% RAS
AR & ASPG 52-34 + 5% ADD#1, 2.5% ADD#2 +5% RAS
BA & BB PG 58-28 +5% RAS
AX & AYPG 58-28 + 5% ADD#2 +5% RAS
AU & AVPG 58-28 + 5% ADD#3 +5% RAS
These are relaxation moduli for the mixture NOT the binderNOTE the moduli at low values of time are > 1E10 Pa
1.00E+05
1.00E+06
1.00E+07
1.00E+08
1.00E+09
1.00E+10
1.00E+11
1.00E-14 1.00E-12 1.00E-10 1.00E-08 1.00E-06 1.00E-04 1.00E-02 1.00E+00 1.00E+02 1.00E+04 1.00E+06
Rela
xatio
n M
odul
us fo
r 20
day,
85°
C ag
ed m
ix T
orsi
on B
ars
Reduced Time, Seconds
Relaxation Modulus of Commpacted Mix aged 20 days @ 85°C all mixes contained 5% RAS, different Binders and Additives were employed
G(t) @+25°C 1531, 07-05-16-BB 58-28, 5% RAS 20D aged @ 85°C
G(t) @25°C 1531, 07-05-16-AV, 58-28,5% RAS, R% BO#2, 20D aged @ 85°C.
G(t) @25°C Summary 1531, 07-05-16-AY, 58-28,5% Cargill 1103, 20d85, RSS.
G(t) 1531 @25°C Summary 07-05-16-AP 52-34 + 5% RAS
G(t) @+25°C 1531, 07-05-16-AM. 5% RAS + 5% EP#1, 20 D aged @ 85°C
G(t) @25°C, 07-05-16-AS, 52-34, 5% RAS +5% EP#1, 2.5% BO#2, 20 D aged @ 85°C
Modulus results obtained using Torsion Bars tested on Dynamic Shear Rheometer
AO & AP PG 52-34 + 5% RAS
AL & AMPG 52-34 + 5% ADD#1+5% RAS
AR & ASPG 52-34 + 5% ADD#1, 2.5% ADD#2 +5% RAS
BA & BB PG 58-28 +5% RAS
AX & AYPG 58-28 + 5% ADD#2 +5% RAS
AU & AVPG 58-28 + 5% ADD#3 +5% RAS
These are relaxation moduli for the mixture NOT the binderNOTE the moduli at low values of time are > 1E10 Pa
1.00E+03
1.00E+04
1.00E+05
1.00E+06
1.00E+07
1.00E+08
1.00E+09
1.00E+10
1.00E-13 1.00E-11 1.00E-09 1.00E-07 1.00E-05 1.00E-03 1.00E-01 1.00E+01 1.00E+03
RELA
XATI
ON
MO
DU
LUS,
G(t
), Pa
REDUCED TIME, SECONDS
Relaxation Modulus of Binder Recovered from 20 day, 85°C Compacted Mix with 5% RAS and Different Binders
G(t) @25°C 1531, 07-05-16-BB, 58-28 straight, 2, 20d85, rec ac, 4mm, hr3-2G(t) @25°C 1531, 07-05-16-AV, 58-28, 5% BO#2 20d85, Rec AC, 4mm, HR3-2G(t) @25°C 1531, 07-05-16-AY, 58-28, 5%, BO#1, 20d85, Rec AC, 4mm, HR3-2G(t) @25°C 1531, 07-05-16-AP, 52-34 20d85, rec ac, 4mm, hr3-2G(t) @25°C 1531, 07-05-16-AM, 52-34 w5% EP#1, 20d85, rec acG(t) @25°C 1531, 07-05-16-AS, 52-34 w5% EP#1, 2.5% BO#1 20d85, rec ac
AO & AP PG 52-34 + 5% RAS
AL & AMPG 52-34 + 5% ADD#1+5% RAS
AR & ASPG 52-34 + 5% ADD#1, 2.5% ADD#2 +5% RAS
BA & BB PG 58-28 +5% RAS
AX & AYPG 58-28 + 5% ADD#2 +5% RAS
AU & AVPG 58-28 + 5% ADD#3 +5% RAS
These are relaxation moduli for binder recovered from aged mixNOTE the moduli at low values of time are > 1E9 Pa
BA
AUAX AO
AL
AR
BB
AVAY
APAM
AS
y = -0.0218x - 0.496R² = 0.8572
-0.5500
-0.5000
-0.4500
-0.4000
-0.3500
-0.3000
-0.2500
-0.2000
-9.00 -8.00 -7.00 -6.00 -5.00 -4.00 -3.00 -2.00 -1.00 0.00
Slop
e of
Tor
sion
Bar
Rel
axat
ion
Mod
ulus
at 2
5°C
@ 1
seco
nd
ΔTc of Recovered Binder from 10 and 20 Day Aged Compacted Mix @ 85°C
Slope of Torsion Bar Relaxation Modulus @ 25 °C & 1 sec = F(ΔTc of recovered Binder)
All Samples 10 day aged compacted mix20 day aged compacted mix Linear (All Samples)
AO & AP PG 52-34 + 5% RAS
AL & AMPG 52-34 + 5% ADD#1+5% RAS
AR & ASPG 52-34 + 5% ADD#1, 2.5% ADD#2 +5% RAS
BA & BB PG 58-28 +5% RAS
AX & AYPG 58-28 + 5% ADD#2 +5% RAS
AU & AVPG 58-28 + 5% ADD#3 +5% RAS
Recovered Binder ΔTc correlates well with the slope of the mixture relaxation modulus
BA
AP
AXAO
AL
AR
BB
AV
AYAPAM
AS
y = 0.0109x - 0.1058R² = 0.84
-0.60
-0.50
-0.40
-0.30
-0.20
-0.10
0.00
-38 -36 -34 -32 -30 -28 -26 -24 -22 -20
Slop
e of
Tor
sion
Bar
Rel
axat
ion
Mod
ulus
at 2
5°C
@ 1
seco
nd
Tm-critical of Recovered Binder
Slope of Torsion Bar Relaxation Modulus @ 25 °C & 1 sec = F(Tm-critical)
10 Day aged mixes 20 Day Aged Mixes
AO & AP PG 52-34 + 5% RAS
AL & AMPG 52-34 + 5% ADD#1+5% RAS
AR & ASPG 52-34 + 5% ADD#1, 2.5% ADD#2 +5% RAS
BA & BB PG 58-28 +5% RAS
AX & AYPG 58-28 + 5% ADD#2 +5% RAS
AU & AVPG 58-28 + 5% ADD#3 +5% RAS
In addition the lowtemperature Tm-Critical value of the recovered binder also correlates well with the slope of the mixture relaxation modulus
BAAPAX
AO
ALAR
BB
AV
AY
AP
AM
AS
y = -0.4855x - 17.511R² = 0.92
-9.00
-8.00
-7.00
-6.00
-5.00
-4.00
-3.00
-2.00
-1.00
0.00
-38 -36 -34 -32 -30 -28 -26 -24 -22 -20
ΔTc
Tm-critical of Recovered Binders
ΔTc = F(Tm-critical)
10 Day aged mixes 20 Day Aged Mixes
AO & AP PG 52-34 + 5% RAS
AL & AMPG 52-34 + 5% ADD#1+5% RAS
AR & ASPG 52-34 + 5% ADD#1, 2.5% ADD#2 +5% RAS
BA & BB PG 58-28 +5% RAS
AX & AYPG 58-28 + 5% ADD#2 +5% RAS
AU & AVPG 58-28 + 5% ADD#3 +5% RAS
SUMMARY COMMENTS• Parameters such as ΔTc, Glover-Rowe, R-Value, crossover
frequency are manifestations of binder relaxation• Binder relaxation largely drives mix relaxation for the aged
mixes we studied• Tm-Critical and ΔTc of recovered binders correlated to mix
relaxation• Slope of relaxation modulus mastercurves appear to
correlate well with ΔTc for a variety of binders • Slope of relaxation modulus did not correlate well with
transverse cracking on the Olmsted CTH 112 project
SUMMARY COMMENTS
• ΔTc did not correlate well with transverse cracking on CTH 112, but did correlate well with total cracking
• Slope of binder relaxation modulus at -18C correlated reasonably well (R2 =0.79) with total cracking on CTH 112 for all 5 test sections including virgin PMA (MN1-2) and PG 58-34 + 20% RAP (MN1-1)
• ΔTc correlated well with the project cracking even when modified binders were used
• Glover-Rowe, crossover frequency and R-value did not correlate well when evaluating mixtures produced with straight run and modified binders
WI STH 33 @ 4 years of age
Mathy Technology & Engineering
WI STH 33 @ 8 years of age
Mathy Technology & Engineering
At 8 years cracking has started, some transverse, some wheel path. This is more consistent with the onset of distress than the pervasive deterioration seen on some sections of CTH 112 and MnROAD
Top 1/2 inch of core extracted and recovered
Core Time after construction
S critical,°C
m critical, °C ΔTc, °C
4 year -30.2 -30.9 0.78 year -28.9 -26.6 -2.3