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Estimating absolute aortic pressure using MRI and a
one-dimensional model
Maya Khalifé, Astrid Decoene, Filipa Caetano, Ludovic de Rochefort,
Emmanuel Durand, Dima Rodríguez
To cite this version:
Estimating absolute aortic pressure using MRI and a
1one-dimensional model
2Maya Khaliféa, Astrid Decoeneb, Filipa Caetanob, Ludovic de Rocheforta,
3
Emmanuel Duranda, Dima Rodrígueza
4
aImagerie par Résonance Magnétique Médicale et Multi-Modalités (IR4M), Université 5
Paris-Sud - CNRS, UMR 8081, Orsay, France
6
bLaboratoire de Mathématiques d'Orsay, Université Paris-Sud - CNRS, UMR 8628, Orsay, 7
France
8
Abstract
9
Aortic blood pressure is a strong indicator to cardiovascular diseases and mor-bidity. Clinically, pressure measurements are done by inserting a catheter in the aorta. However, imaging techniques have been used to avoid the invasive procedure of catheterization. In this article, we combined MRI measurements to a one-dimensional model in order to simulate blood ow in an aortic segment. Absolute pressure was estimated in the aorta by using MRI measured ow as boundary conditions and MRI measured compliance as a pressure law for solv-ing the model. Model computed pressure was compared to catheter measured pressure in an aortic phantom. Furthermore, aortic pressure was estimated in vivo in three healthy volunteers.
1. Introduction
10
To date, blood pressure (BP) is one of the most useful clinical indicator of
11
cardiovascular disease. Hypertension, more specically, is a leading predictor
12
of death in atherosclerosis diseases worldwide Cohn et al. [13], Collaboration
13
[14]. Therefore, measuring BP is of great interest for diagnosis and risk
pre-14
vention of cardiovascular events. An elevated pressure gives information about
15
the aortic state, the presence of atherosclerotic plaques, stenosis, calcication
or aneurisms. In a clinical routine, a sphygmomanometer is used to measure
17
systolic and diastolic brachial pressure. However, due to reexion in the distal
18
arteries, the aortic pressure waveform is altered while traveling through the
vas-19
cular system. Thus distortion of the wave shape as well as systolic amplication
20
occur on the systolic pressure measured in the brachial artery O'rourke et al.
21
[32], Park and Guntheroth [34], Salvi [37]. Although models and transfer
func-22
tions to link brachial BP to aortic pressure exist Chen et al. [12, 11], Liang [26],
23
wave reection in the arterial system makes it dicult to reproduce the wave
24
contour with great delity from such methods. Until now, the gold-standard of
25
aortic pressure measurement is catheterization, which is invasive and not
repeat-26
able in a routine procedure Murgo et al. [30], Skinner and Adams [40]. In recent
27
years, imaging techniques have been used to assess pressure gradients from
ve-28
locity or acceleration maps and its combination with uid mechanics equations
29
has been exploited in order to measure the BP non-invasively. Doppler
Ultra-30
sound (US) used to measure blood velocity in the arteries was associated to the
31
standard simplied Bernoulli equation in order to determine pressure dierences
32
between two measurement sites. This latter technique is reported to be
user-33
dependent and error-prone due to the wave angle of incidence Zananiri et al.
34
[51], Muhler et al. [29], hence its accuracy in determining the maximum velocity
35
in the artery is debatable. Also, extending US to other situations is limited
36
by the inapplicability of Bernoulli equation to unsteady ows Yang et al. [50].
37
Phase-Contrast (PC) MRI allows accurate encoding of the blood velocity in the
38
arteries in the three directions; hence, it has been largely used for non-invasive
39
pressure estimation. Some authors computed pressure dierences using Poisson
40
equation Yang et al. [50], others integrated the Navier-Stokes (NS) equations
41
using MRI velocity maps Tyszka et al. [45], Thompson and McVeigh [44], Bock
42
et al. [8], Ebbers et al. [17] or acceleration maps to avoid computational errors
arising from velocity derivation Buyens et al. [10]. These methods compute a
44
pressure gradient, and to estimate an absolute pressure, require a zero-pressure
45
reference point which has to be measured with a catheter, or user-dened in
46
a gross assumption. Consequently, these methods are not an alternative to
47
catheter measurements, which remain more accurate. In this work, we propose
48
a non-invasive technique to extract absolute pressure in a straight artery from
49
MR velocimetry using a biomechanical one-dimensional (1D) model as proposed
50
by Formaggia et al. Formaggia et al. [18]. Although a three-dimensional (3D)
51
model gives a more complete and realistic reproduction of the aortic ow, 1D
52
models are able to describe the non-linear ow behavior in larger elastic vessels
53
Hughes and Lubliner [22]. As these models are reasonably accurate, they are
54
widely used for aortic ow simulations. Their accuracy has been assessed by
55
comparison with experimental data acquired in a tube phantom Bessems et al.
56
[7], in a distributed arterial model Olufsen et al. [31], Alastruey et al. [2] and in
57
vivo Reymond et al. [36], Alastruey et al. [3]. Furthermore, the 1D model relies
58
on the establishment of a pressure law consisting of a relation between pressure
59
and vessel section area. The pressure laws used in 1D model equations are
deter-60
mined experimentally with invasive measurements or estimated using complex
61
algorithms. Additionally, these pressure laws are complicated and involve the
62
determination of multiple parameters. Here, we propose a pressure law based
63
on the aortic compliance which reects arterial elasticity and can be determined
64
non-invasively with MRI. Using this pressure law, we coupled the 1D model with
65
realistic boundary conditions measured by MRI to estimate absolute pressure
66
in the aortic segment. The derived model was tested on a straight compliant
67
phantom and computed pressure was compared to experimental pressure
mea-68
surements recorded simultaneously with the MRI acquisition. The model was
69
also tested on a real-sized compliant aortic phantom Then, the model is used to
estimate BP on healthy volunteers.
71
2. Methods
72
The 1D-model, studied in Formaggia et al. [18], is a reduced model
describ-73
ing blood ow in arteries and its interaction with wall motion. The artery is
74
considered as a cylindrical compliant tube of length L and radius R (R L).
75
The model derivation approach consists of integrating the NS equations on a
76
generic section S. Some simplifying assumptions are made:
77
• the model assumes axisymmetry
78
• the wall displacement is supposed to solely be in the radial direction
79
• pressure is assumed to be uniform in each section
80
• the axial velocity uzis predominant.
81
For large arteries such as the aorta, it is a safe assumption to consider a at
82
velocity prole for the boundary layer is very thin compared to the vessel radius
83
Olufsen et al. [31].
84
The main variables of the problem are (Figure 1):
85
• axial section area A
86 A(t, z) = ˆ S(t,z) dσ (1) • mean ow Q 87 Q(t, z) = ˆ S uzdσ (2) • blood pressure P (t, z), 88
where dσ denotes the area element. Their evolution is described by the
mo-89
mentum conservation and the mass conservation equations, while considering a
constant viscosity: 91 ∂A ∂t + ∂Q ∂z = 0 (3) ∂Q ∂t + ∂ ∂z Q2 A +A ρ ∂P ∂z + Kr Q A = 0 (4)
Kris the friction coecient; for a at prole in blood ow problems, Kr= 22πν,
92
where ν is the vessel wall kinematic viscosityFormaggia and Veneziani [19]. ρ is
93
the blood density.
94
Pressure law
95
To close the system, a relation between the section area A and the pressure
96
Pis dened. This pressure law depends on section area A0(z) = πR2
0(z)at time
97
t = 0 and on a set of parameters β = (β0, β1, ...βn) related to the vessel wall
98
physical and mechanical properties. Pextis the external pressure exerted by the
99
environment of the vessel whereas P is the intravascular pressure. The pressure
100
law should meet these conditions:
101
• ∂P ∂A > 0
102
• when A = A0, P = Pext.
103
Some pressure laws are proposed in the literature to link the pressure behavior
104
to the section area. A frequently used relation between A and P is stated as
105
follows Quarteroni and Formaggia [35], Alastruey [1]:
106 P − Pext = β0 √ A −√A0 A0 (5) β0= √ πh0E
1−ξ2 using Young's modulus E and the vessel thickness h0and Poisson's 107
ratio ξ = 0.5 for an incompressible material deformed elastically at small strains.
108
A more general law proposed in Hayashi et al. [21], Smith and Hunter [41]
109
is written as:
P − Pext = β0 " A A0 β1 − 1 # . (6)
The parameters β0 and β1 values can be obtained either by tting
experi-111
mental pressure versus section measurements Smith [42], or by solving an inverse
112
problem with a 3D-model solution Martin et al. [27], Dumas [16]. Hence, these
113
laws cannot be determined non-invasively, and need knowledge about the vessel
114
properties. Additionally, they seem too complex to determine during a clinical
115
application. Finding a simple non-invasive way to determine a pressure law is of
116
great interest, consequently, we turned to the compliance. Indeed, in
physiolog-117
ical conditions, the aorta section deformation is commonly assumed to be linked
118
to the intravascular pressure by the aortic compliance Langewouters et al. [24].
119
Aortic compliance establishes a linear relation between the pressure and
120
section area; it represents the arterial wall ability to deform in response to a
121
pressure variation Conrad [15]. Also, it is clinically used and can be estimated
122
non-invasively by measuring the pulse wave velocity (PWV) in MRI. Hence, it
123
provides a simple and non-invasive pressure law that can be applied in vivo and,
124
as it includes compliance changes, is patient-specic.
125
In fact, compliance is given by the ratio of section variation to pressure
126
variation :
127
C = dA
dPt (7)
where Pt= P − Pext is the transmural pressure. The compliance is considered
128
as a local constant on an arterial segment. By integrating equation (7) and
129
knowing that when Pt = 0, i.e. P = Pext, A = A0, we write A = CPt+ A0
130
where A0 is the section area at the equilibrium state.
We write equation 7 as C = A−A0
P −Pext, thus deriving the pressure law: 132 P − Pext=A0 C A A0 − 1 (8)
In the limit of small displacements, this pressure law is equivalent to the
com-133
monly used linear law ((5)) for
134
β0 =
2A3/20
C , (9)
In fact, by linearizing ((5)) (see also Alastruey et al. [5]), we have:
135 β0 √ A −√A0 A0 = β0 2A3/20
(A − A0) + O(A − A0)2
Numerical approximation
136
System (3)-(4) is written in the conservative form :
137 ∂U ∂t + ∂F(U) ∂z = S(U) (10) where 138 • U = A Q 139 • F = Q Q A 2 + C1 ,C1(A) = ´A 0 c 2 1(τ ) dτ and c1= c1(A) = q A ρ ∂P ∂A, 140 • S = 0 −KrQA 141
Since A > 0, the matrix DF possesses two real distinct eigenvalues λ±= QA± c1
142
and system (10) is a hyperbolic system of partial dierential equations
For-143
maggia and Veneziani [19]. The blood ow is assumed to be sub-critical, thus
144
λ− < 0,and λ± have opposite signs.
Following Formaggia and Veneziani [19], system (10) is written in
diago-146
nal form, which is more suitable to understand the solution behavior and for
147 numerical purpose: 148 ∂W ∂t + Λ ∂W ∂z = L · S (11)
where W = (W1, W2)are the characteristic variables, Λ = λ+ 0 0 λ− and 149 L = `T + `T−
is a matrix of left eigenvalues ofDFsuch that L · DF = Λ · L. In
150
the case of the law (8), we have
151 c1= s A ρC, W1= Q A + 2 s A ρC, W2= Q A − 2 s A ρC. (12)
Inversely, the primitive set of variables (A, Q) is written in terms of the
152 diagonal variables (W1, W2)as 153 A = p ρCW1− W2 4 2 , Q = AW1+ W2 2 . (13)
For system (10) approximation, a nite volume scheme is dened by a grid over
154
[0, L] × [0, T ],with uniform mesh-spacing ∆z and time step ∆tn. The cells are
155
given by [zi, zi+1[×[tn, tn+1[, where zi = i∆z, i = 0, . . . , M, with M∆z = L,
156
and tn = n∆tn, n = 0, . . . , N, with N∆tN = T. We seek Un
i approximating 157 1 ∆z ´zi+1 zi U (x, t n)dz. 158
The numerical scheme is a classical nite volume scheme of Rusanov type
159
for hyperbolic problems:
161 Fi+1 2 = 1 2 h F (Uin) + F (Ui+1n ) − λi+1 2(U n+1 i − U n i ) i with λi+1 2 = max{λ−(U n i), λ+(U n
i+1)}, and where S n i = 0 −KrQni An i . Time-162
space ∆tnmust verify the well-known stability condition 2 max i |λi+
1 2|∆t
n≤ ∆z.
163
Numerical boundary conditions are prescribed, thus Un
in= U−1n and Uoutn =
164
Un
M +1 are given to compute U n+1 0 and U
n+1
M at z = 0 and z = L respectively.
165
Since ows involved in this model are sub-critical, the numerical scheme (14)
166
requires one condition at each boundary. An admissible condition imposes the
167
incoming characteristic and allows the wave corresponding to the outgoing
char-168
acteristic to leave the domain. As W2 remains constant along the characteristic
169
curve dened by dz
dt = λ−(U (z, t)),if we approximate λ−(U (z, t))by its
numer-170
ical value λ−(U (z, tn))in [tn, tn+1[,we consider that
171 W2(z, tn+1) ' W2(z − {λ−}n0∆t n, tn), thus 172 W2,inn+1=∆z + λ∆t ∆z W n 2,−1− λ∆t ∆z W n 2,0 where λ = λn
−0 and ∆t = ∆tn. Similarly, we impose
173 W1,outn+1 = ∆z − λ∆t ∆z W1 n M +1+ λ∆t ∆z W1 n M where λ = {λ+}n M. 174 Boundary conditions 175
We used MRI measured boundary conditions on the inlet of the tube
phan-176
tom or the arterial segment. Flow measured on the entrance was imposed as
177
a condition on the rst mesh. We extrapolated, as explained above, the inlet
178
value of W2,and A was computed by using relations (12) and (13). The outlet
boundary condition is obtained by coupling the 1D model with a 0D model that
180
consists of a system of dierential equations linking pressure to ow at the 1D
181
model exit. In fact, as shown in Alastruey et al. [4], the behavior happening
182
beyond the 1D-modeled arteries can be represented by a 0D lumped-parameters
183
model, also known as the Windkessel model, that simulates hemodynamics by
184
electrical circuit analogy. Pressure gradient is represented by a potential
dif-185
ference, blood ow by the electrical current and hydraulic impedance by an
186
electrical impedance. Hydraulic impedance combines friction loss, arterial wall
187
elasticity and blood ow inertia, which are modeled by a resistance, a capacitor
188
and an inductance respectively. A three-element (RCR) Windkessel model is
189
a good compromise accounting for wall compliance and resistance in the
pe-190
ripheral network as well as proximal aortic impedance Wetterer [48], Westerhof
191
et al. [47]. It is a combination of an R-model and an RC-model that improves
192
considerably the behavior of the original two-element model proposed by Otto
193
Frank Frank [20] by removing pressure and ow oscillations Stergiopulos et al.
194
[43], Alastruey [1]. The rst resistance Zc is the proximal aorta characteristic
195
impedance, the compliance C in parallel to the resistance R2 simulate
respec-196
tively the volume compliance and the resistance of the vascular network found
197
downstream the abdominal aorta (Figure 2).
198
The inlet ow of the R model, which is the 1D-model outlet ow (Qin−0D=
199 Qout−1D), is: 200 Qin−0D = Pin−0D− PC Zc (15)
As for the RC-model:
Pout−0D is the pressure at the 0D-model exit. We compute PC at each time
202
step by explicitly discretizing equation (16):
203
PCN +1 = f (PCN, QNin−0D, Pout−0D)
then use the relation at the 1D-model exit:
204 QN +1in−0D = P N +1 in−0D− P N +1 C Zc MRI experiments 205
A straight exible silicone tube was used as a phantom to validate the
206
1D-model. The MRI setup (Figure 3), described in a previous work Khalife
207
et al. [23], consisted of the phantom connected to a non-magnetic CardioFlow
208
5000MR pump (Shelley Automation, Toronto, Canada) that can generate a
pro-209
grammable ow pattern. We used a blood mimicking uid (BMF, 62% water
210
and 38% glycerol) with similar magnetic and physical properties as blood. It
211
has a Newtonian behavior which is a safe assumption for blood circulating in
212
large arteries Ottesen et al. [33]. Two MRI-compatible optical pressure sensors
213
(Opsens, Québec, Canada) were introduced into the phantom. These sensors
214
allow simultaneous pressure measurements used as validation for the simulation.
215
To test the 1D-model application on a curved segment and estimate the
216
error, the tube phantom was replaced with an aortic phantom (Elastrat, Geneva,
217
Switzerland) comprising an ascending aorta branch (AAo) and a descending
218
aorta branch (DAo). Pressure sensors were introduced at the AAo entrance and
219
at the DAo exit.
220
A sinusoidal waveform of amplitude 150mL.s−1was applied in the tube
phan-221
tom setup. In the aorta phantom setup, a ow wave similar to the one measured
at the left ventricle exit was programmed on the pump control system with an
223
amplitude of 250mL.s−1 and a period of 0.8s (75bpm).
224
Experiments were performed on a 1.5T MRI system (Achieva; Philips, Best,
225
the Netherlands) using SENSE Flex-L coils. Phase-Contrast (PC) ow-encoded
226
gradient-echo multiphase sequences were performed to assess through-plane
ve-227
locity on two slices, one situated at the phantom entrance with the rst pressure
228
sensor and the second at the phantom exit, with the second pressure transducer.
229
Scan parameters: spatial resolution: 1 × 1 × 8mm3, echo time/repetition time
230
TE/TR = 5.75/9.59ms, velocity encoding Venc = 80cm.s−1 for a owrate of
231
150mL.s−1 and Venc = 100cm.s−1 for a owrate of 250mL.s−1, 40 time frames
232
per cardiac cycle with ECG-triggering on the pump signal.
233
For the in vivo feasibility of the 1D-model, 3 healthy subjects (male, ages 27,
234
30 and 33) were included in our study after having lled out a written consent
235
form. All measurements were performed on a 1.5T MRI system with SENSE
236
cardiac coil. PC ow-encoded sequence covering the thoracic aorta was acquired
237
during breath-hold and ECG-gated gradient echo sequence (spatial resolution:
238
1.1 × 1.1 × 8mm3, TE/TR = 3.0/5.1 ms, Venc= 180cm.s−1, 40 time frames per
239
cardiac cycle). Data were acquired in an axial plane to measure through-plane
240
velocity in the descending and the abdominal aorta (AbAo). A coronal plane of
241
the aorta was acquired to measure the distance between velocity encoding sites.
242
Arm pressure was measured before and after MRI acquisitions and used as
243
a reference for the 1D-model pressure simulations.
244
Compliance measurements
245
MRI images were processed using an in-house code. Aorta section was
seg-246
mented semi-automatically and visually assessed by the operator on the
magni-247
tude image then ow waveforms were computed from velocity data provided by
248
the corresponding phase images. The inlet ow is thus used as the model input
condition.
250
MRI non-invasive measurements were used to determine phantoms and
aor-251
tic compliance through PWV. The method, described in a previous work Khalife
252
et al. [23], is based on the transit time (TT) method commonly used for the
253
PWV estimationMurgo et al. [30], Avolio et al. [6] (Figure 4).
254
For each experiment, the linear compliance is determined from PWV based
255
on the Bramwell-Hill theory: C = A
ρ(P W V )2 Bramwell and Hill [9], Vulliémoz 256
et al. [46], where A is the vessel lumen area and ρ the uid density.
257
Simulations
258
Simulations were performed on an in-house program using Matlab (the
Math-259
works, Natick, USA) by setting the domain geometry, uid properties and MRI
260
measured compliance for the pressure law. FlowQ, section area A and
pres-261
sure P are computed on the whole domain as functions of time and space, then
262
compared to measured data on the corresponding nodes.
263
The values of the input parameters were the following:
264
• Tube phantom : L = 40cm, C = 0.0012 cm2.mmHg−1. The RCR-model
265
components were estimated from measurements: Zc= 1.24 · 108Pa.s.m−3
266
was computed using the approach proposed in Mitchell et al. [28], R2 =
267
1.63 · 108 Pa.s.m−3, Cper= 0.288 cm3.mmHg−1 and Pout−0D= 0.
268
• Aortic phantom: L = 21.5cm, C = 0.051cm2.mmHg−1, Zc = 2.63 ·
269
106Pa.s.m−3, R2= 1.07 · 108Pa.s.m−3, Cper = 0.137 cm3.mmHg−1 .
270
• In vivo : the RCR parameters at the outlet were taken from Alastruey
271
et al. [4] because of the absence of invasive measurements. The
character-272
istic impedance is Z0= ρc0
A0. The peripheral resistance is R2= RT − Zc
273
where RT = 1.89 · 108Pa.s.m−3is the complete vascular system resistance.
The simulations were performed on a 100 meshgrid on a scope of 10 periods,
275
with an average simulation time of 328 s. A and Q are computed at each time
276
step,∆t = 10−4s. To evaluate results, the root mean square error in % (RMS)
277
was calculated between computed and measured pressure waves.
278
Furthermore, to evaluate the equivalence between the pressure law (5) and
279
the compliance pressure law (8) proposed in this work, two simulations were
280
carried out with the same ow conditions, but with dierent pressure laws. The
281
ow waveform and the model parameters used were those of a physiological
282
scenario as proposed in Alastruey et al. [4]: A0= π · 10−4m2, β0= 4 3
√
πhEfor
283
the β0pressure law, with E = 0.4·106
Pa, h = 1.5·10−3m, C = 7.85·10−9m3/Pa,
284
and compliance of 2A3/20
β0 for the compliance pressure law. 285
3. Results
286
The results of the equivalence test between the pressure law (5) and the
287
compliance pressure law (8) are depicted in gure 5. Based on these curves, we
288
can say that the two pressure laws provide nearly identical results which means
289
that the β0 pressure law agree well with the linear pressure law with C = 2A3/20 β0 , 290
as in equation (9). The RMS between both pressure curves is 6.2% . Hence,
291
even if the pressure to section area relation is not perfectly linear in the range of
292
physiological pressure, the error committed by considering it linear is negligible.
293
In phantom experiments, simulated pressure was compared to pressure
sen-294
sor measurements.
295
The inlet ow and the simulated pressure within the tube phantom are
296
shown in gure 6 for the sinusoidal ow waveform of amplitude 150mL.s−1.
297
Computed pressure curves show good agreement with the measured pressure in
298
the tube phantom. RMS error computed between both is 8.15% and conrms
299
the agreement of the model results with measurements.
300
Furthermore, the simulated pressure at the DAo outlet in the aortic phantom
was compared to pressure sensor measurements acquired at the same location
302
(Figure 7b). RMS between both pressure curves is 4.97%. Velocity measurement
303
noise caused oscillations on the MR measured ow which were reported on the
304
simulated pressure. This is due to the relatively low velocity measured in the
305
descending branch. Thus, the ow was ltered before simulations (Figure 7a).
306
Beyond this, pressure curves simulated by the 1D-model on a straight
seg-307
ment formed by the DAo and the AbAo in healthy volunteers are plotted in
308
gure 8. Their contour is in good agreement with pressure curves reported in
309
vivo in the literature Schnabel et al. [38], Murgo et al. [30]. Also, according
310
to the reection principle described in Salvi [37], the systolic pressure increases
311
along the arterial tree and consequently the brachial systolic pressure
overesti-312
mates the aortic systolic pressure up to 20mmHg Levick [25]. Thus in gure 8,
313
the simulated systolic pressure in the aorta is smaller than the systolic pressure
314
measured on each volunteer. Mean arterial pressure (MAP) computed on the
315
simulated and measured pressure is added in gure 8.
316
4. Discussion
317
In this work, we showed that by combining a 1D aorta model to non-invasive
318
MRI velocity measurements, we were able to estimate aortic pressure. Flow
319
MRI had commonly been used to derive pressure dierences, so estimating a
320
local pressure without having to set a null pressure point is a step forward in
321
cardiovascular diagnosis.
322
The MR-measured ow was used as input for the 1D-model and a coupled
323
0D-model was used as an output condition. The pressure law, which relies on
324
invasive measurements in formal studies, is replaced by a non-invasive pressure
325
law based on the aortic compliance. This compliance was measured from MRI
326
assessed PWV. The model simulations were successfully validated on an MRI
327
setup with a straight phantom, an aortic arch phantom and in vivo.
At rst, the simulations were applied on a simple straight tube to respect the
329
model conditions and simplications. Pressure values obtained with simulations
330
were in good agreement with measurements and showed satisfactory results as
331
in previous studies Alastruey et al. [2]. Then, simulations were applied on an
332
aortic phantom and results showed a negligible error when compared to pressure
333
measurements, meaning that, in the physiological range of blood velocity, the
334
1D-model coupled with MRI ow measurements and subject-specic compliance
335
pressure law would be enough to describe the aortic ow behavior. Results in
336
vivo showed that it can estimate realistic pressure curves in the DAo, in
agree-337
ment with the brachial pressure measured in the clinical routine. A bias was
338
observed between the two brachial measurements carried out before and after
339
the MRI exam due to the subject changing state going from agitated prior to
340
the exam to rested state after the exam was completed. Another explanation
341
could be the dierence in the subjects position (seated vs. supine) during
mea-342
surements. Consequently, the measured arm pressures might have been dierent
343
than what the simulations would yield.
344
This 1D-model, which is frequently used to model the aorta, is based on
345
strong assumptions, considering only radial and axisymmetric wall
deforma-346
tions, constant pressure on a section along the tube axis, thus only depending
347
on time and on the axial coordinate z, dominance of axial velocity, absence of
348
turbulence and neglecting the vessel wall inhomogeneities. Nevertheless, the
349
model serves its initial role of estimating an absolute pressure in a simple and
350
fast non-invasive manner, thus it is widely used in large artery modeling for
351
its fair reproduction of the physiological conguration. Even if the model is
352
one-dimensional and must be applied to a straight segment, its application to a
353
curved aortic phantom did not greatly aect the agreement of simulated
pres-354
sure and measured pressure at the phantom outlet. However, the eect of an
inertance in the 0D-model represented by an inductor in the electrical circuit
356
could be considered. The inertance element as proposed in Segers et al. [39]
357
could absorb the oscillations which appear on the pressure curve.
358
The compliance based pressure law is simple, non-invasive and widely
an-359
chored in clinical practice and its association to the 1D-model may be more
360
advantageous than the previously used pressure laws reported here. The model
361
showed satisfactory results and good reproduction of invasive measurements
362
recorded on a tube phantom. Additionally, we have shown that this
simpli-363
ed linear pressure law is in good agreement with the√Alaw proposed in the
364
literature.
365
Some improvements could be made to the 1D-model in the future. The model
366
could be made more patient-specic by adapting the 0D-model parameters to the
367
patient at the outlet boundary condition. Since these parameters are taken from
368
the literature and are not patient-specic, previous work Willemet et al. [49] has
369
proposed to measure peripheral resistance by introducing pressure catheters in
370
the femoral artery. However, this is a disadvantage to a method which oers to
371
be strictly non-invasive. Further studies are needed to propose a non-invasive
372
way to measure the RCR parameters. Also, the model supposes a constant
373
compliance along the artery which is a non-realistic condition when studying
374
aortic disease or stenosis. This problem will be addressed in future studies.
375
In the future, it would be interesting to compare the pressure estimation
376
found in our model with catheter measurements in an animal experiment. Also,
377
more in vivo experiments would allow assessing the reliability and the
repeata-378
bility of such estimation techniques in the aorta and to study pressure changes
379
in patients suering from cardiovascular diseases or under various stress
condi-380
tions.
Conict of interest statement
382
The authors declare that there are no conicts of interest.
383
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Figure 1: The 1D model simplied geometry. It assumes that the artery is a straight cylinder of length L with a circular cross section A(t, z) that deforms in respect to the radial vector.
Figure 2: Coupling the 1D model outlet with the 0D model: a three-element Windkessel model (RCR) forms the outlet boudary condition of the 1D model. (Qin−0D, Pin−0D) =
(Qout−1D, Pout−1D) and (Qout−0D, Pout−0D) are ow and pressure at the inlet and the
outlet of the RCR model respectively. To solve the RCR model, two sub-models, RC and R, are considered and then combined. PC is the pressure across C at the exit of the RC model
and at the entrance of the R model.
AAo DAo (a) AAo DAo (b) ∆t 0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0 50 100 150 200 250 300 350 400 450 Time(s) Flowra te (mL /s) DAo AAo (c)
Figure 4: Transit time estimated on MR ow waves in subject A. (a) magnitude image of the acquired axial plane. (b) AAo and DAo are visible in hypersignal; through-plane velocity image in AAo and DAo : ow waveforms are extracted from the encoded velocity. (c) The TT method for PWV measurement. The TT, which is the delay ∆t that a waveform needs to travel a distance L, is used to compute the wave velocity: P W V = L
∆t. Here, ∆t was
6.4 6.5 6.6 6.7 6.8 6.9 7 7.1 0 50 100 150 200 250 300 Time (s) F l o w r a t e ( m L / s ) β 0law 0m β 0law 0,2m β 0law 0,4m C law 0m C law 0,2m C law 0,4m (a) 6.4 6.5 6.6 6.7 6.8 6.9 7 7.1 0.1 0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 Time (s) V e l o c i t y ( m / s ) β0law 0m β0law 0,2m β0law 0,4m C law 0m C law 0,2m C law 0,4m (b) 6.4 6.5 6.6 6.7 6.8 6.9 7 7.1 70 80 90 100 110 120 130 Time (s) P r e s s u r e ( m m H g ) β0law 0m β0law 0,2m β0law 0,4m C law 0m C law 0,2m C law 0,4m (c)
Figure 5: Results of the 1D model using pressure laws with β0 in equation (5) (straight
line) vs. with compliance C =2A3/20
β0 (dotted line). Simulations are performed with a pulsed
0.9 1 1.1 1.2 1.3 1.4 1.5 50 0 50 100 150 Time(s) Flowra te(mL/ s) (a) 0.8 0.9 1 1.1 1.2 1.3 1.4 1.5 20 0 20 40 60 80 100 120 140 Pressu re (mm Hg) Simulated-sensor 1 Simulated-Mesured Mesured (b)
Figure 6: Pressure curves in the tube phantom with a sinusoidal ow waveform of amplitude 150 mL.s−1. Boundary conditions used are the measured ow at the inlet (a) and given by
0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8 −50 0 50 100 150 200 250 300 Time (s) Flowrate (mL/s) measured fitted (a) 0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8 −2 0 2 4 6 8 10 12 14 16 18 Time (s) Pressure (mmHg) simulated− DAo measured− DAo (b)
Figure 7: (a) Flow mesured at the entrance of the aorta phantom (solid line). Due to the motion of the phantom and the low velocity amplitude, oscillations are visible at the measure-ments curves and are reported in the 1D model simulation results. Hence, the tted measured ow (dashed line) is used for pressure calculation. (b) Simulated vs. measured pressure at the exit of the aorta phantom with a ventricular ow of amplitude 250 mL.s−1. Boundary
7 7.2 7.4 7.6 7.8 8 8.2 60 70 80 90 100 110 Time (s) Pressu re (mm Hg) DAo 0cm DAo AbA
(a) subject A, 27 years old
6.8 6.9 7 7.1 7.2 7.3 7.4 7.5 7.6 7.7 75 80 85 90 95 100 105 110 115 120 Time (s) Pressu re (mm Hg) DAo 0cm DAo AbA
(b) subject B, 30 years old
7.1 7.2 7.3 7.4 7.5 7.6 7.7 7.8 7.9 8 70 80 90 100 110 120 130 Time (s) Pressu re (mm Hg) DAo 0cm DAo AbA -- 9cm - 18cm
(c) subject C, 33 years old
Figure 8: Healthy volunteers' aortic pressure simulated in a straight segment going from the descending aorta (DAo) to the abdominal aorta(AbAo). The horizontal dashed lines in orange show the averaged brachial diastolic and systolic pressure (Pdiastand Psyst) measured for each